review of methods to enhance the …wvuscholar.wvu.edu/reports/vemulapalli_r.pdfreview of methods to...
TRANSCRIPT
REVIEW OF METHODS TO ENHANCE THE DUCTILITY AND STRENGTH OF STRUCTURES FOR RESISTING EARTHQUAKE
AND BLAST LOADING
Ravi Sudhakar Vemulapalli
Problem report submitted to the College of Engineering and Mineral Resources
at West Virginia University in partial fulfillment of the requirements
for the degree of
Master of Science in
Civil Engineering
Udaya B. Halabe, Ph.D., P.E., Chair Hema J. Siriwardane, Ph.D., P.E.
Roger H. L. Chen, Ph.D.
Department of Civil and Environmental Engineering
Morgantown, West Virginia 2007
Keywords: Earthquake, Blast, Blast Design, Seismic Design, Seismic Rehabilitation,
Blast Rehabilitation, FRP, Wrapping, Jacketing
ABSTRACT
Review of Methods to Enhance the Ductility and Strength of Structures for Resisting Earthquake and Blast Loading
Ravi Sudhakar Vemulapalli
This report presents a literature review of the methods to enhance the ductility and
strength of structures to resist earthquake and blast loadings. Enhancing the ductility of
the structural system greatly helps in minimizing the damage to the structure in the event
of earthquake or blast loading. This literature review consists of methods like wrapping
beam column joints with FRP composites, use of stay-in-place FRP confinements for RC
columns, use of shear walls, RC jacketing, base isolation and energy dissipation devices,
and retrofitting of unreinforced masonry walls. Most of the existing buildings were
designed based on earlier design codes that are no longer in practice and don’t account
for the required ductility that is needed for efficient seismic and blast resistance. The
ductility and strength of the structures can be improved through effective rehabilitation
techniques, which in turn help in effective mitigation of damage due to earthquake and
blast loading. This report also includes a review of techniques especially aimed at
retrofitting commercial buildings to resist blast loading.
All the methods that were reviewed are effective in enhancing structural resistance to
seismic and blast loading, but some of them have applicability limitations. More research
work is needed to further develop these techniques and make them more cost effective.
ACKNOWLEDGEMENTS
At the outset, I would like to express my sincere gratitude to my academic advisor, Dr.
Udaya B. Halabe for his valuable guidance and encouragement during my Master of
Science in Civil Engineering (M.S.C.E) degree program. I am thankful to Dr. Hema J.
Siriwardane and Dr. Roger Chen, members of the Advisory and Examining Committee,
for their help during my studies.
I am thankful to Shasanka Dutta, Aneesh Bethi, and Sandeep Pyakurel for their support
and encouragement during my work. I thank my family who stood beside me and
provided the impetus to do my best.
iii
TABLE OF CONTENTS
ABSTRACT ii ACKNOWLEDGEMENTS iii TABLE OF CONTENTS iv LIST OF FIGURES vii LIST OF TABLES x Chapter 1 – INTRODUCTION 1
1.1. BACKGROUND 1 1.2. OBJECTIVE 3 1.3. REPORT ORGANIZATION 3
Chapter 2 - EARTHQUAKE AND BLAST 4 2.1. EARTHQUAKE 4 2.1.1. Types of Earthquake 4 2.1.2. Quantifying Earthquake 4 2.1.3. Different Types of Structural Failures 6 2.1.4. Important Categories of Damage 9 2.1.4.1. Reinforced Concrete Members 10 2.1.4.2. Structural Steel Members 13 2.1.4.3. Masonry Structures 13 2.1.5. Previous Earthquakes 14 2.2. BLAST 16 2.2.1. Blast Resistant Design 16 2.2.2. Types of Explosions 17 2.2.3. Blast Wave Parameters 20 2.2.4. Previous Explosions 21 Chapter 3 - REHABILITAION FOR EARTHQUAKE 24 3.1. BEAM-COLUMN JOINT REHABILITATION 24 3.1.1. Experimental Program 25 3.1.1.1. Specimen Description 25 3.1.1.2. Material Properties 26 3.1.1.3. Experimental Test Set-Up 27 3.1.1.4. Loading Sequence 27 3.1.1.5. Instrumentation 29 3.1.2. Rehabilitation Scheme 31 3.1.3. Experimental Results 32 3.1.4. Summary 33 3.2. SQUARE HIGH-STRENGTH CONCRETE COLUMNS IN FRP
STAY-IN-PLACE FORMWORK 34
3.2.1. Experimental Procedure 34 3.2.2. Test Specimens 35 3.2.3. Material Properties 39 3.2.3.1. Carbon FRP composite 39
iv
3.2.3.2. Concrete Properties 41 3.2.3.3. Steel Reinforcement 41 3.2.4. Experimental Test Setup 42 3.2.5. Test Results 43 3.2.6. Deformation of HSC Columns Confined by FRP
Casing 44
3.2.7. Summary 45 3.3. REHABILITATION OF COLUMNS WITH REINFORCED
CONCRETE JACKETS 45
3.3.1. Added Longitudinal Reinforcement 45 3.3.2. Slab Crossing 47 3.3.3. Interface Surface Preparation 47 3.3.3.1. Methods to Increasing Surface Roughness 47 3.3.3.2. Surface Pre-wetting 48 3.3.3.3. Application of Bonding Agents 49 3.3.3.4. Addition of Steel Connectors 50 3.3.3.5. Testing of Different Methods 50 3.3.4. Spacing of Added Stirrups 51 3.3.5. Temporary Shoring of the Structure 51 3.3.6. Properties of Added Concrete 51 3.3.7. Structural Behavior 52 3.3.7.1. Effect of Damage on Structural Behavior 53 3.3.8. Summary 53 3.4. SEISMIC REHABILITATION BY ADDING SHEAR WALLS 55 3.4.1. Rehabilitation Method 55 3.4.2. Design criteria for seismic design 55 3.4.3. Four Story Building in Dinar 56 3.4.4. Eight Story Building in Ceyhan 58 3.4.5. Aftershock Test in Dinar 60 3.5. PASSIVE SEISMIC PROTECTION IN STRUCTURAL
REHABILITATION 61
3.5.1. Base Isolation 62 3.5.2. Energy Dissipation Devices 64 Chapter 4 - REHABILITAION FOR BLAST 66 4.1. POLYMER RETROFIT OF UNREINFORCED MASONRY WALLS 67 4.1.1. Selection of Retrofit Material 69 4.1.2. Test Procedures 70 4.1.3. Instrumentation 71 4.1.4. Test Results 76 4.1.5. Summary 76 4.2. REHABILITATION OF STRUCTURE AFTER A GAS EXPLOSION 76 4.2.1. Rehabilitation Method 77 4.2.2. Case Study of a Structure Damaged by Gas Explosion 78 4.2.3. Building Damage Assessment 79 4.2.4. Rehabilitation Scheme 81
v
4.2.5. Summary 86 4.3. BLAST RESISTANT DESIGN OF COMMERCIAL BUILDINGS 86 4.3.1. External Treatment 89 4.3.1.1. Stand off Distance 89 4.3.1.2. Lower Floor Exterior 90 4.3.2. Glazing 91 4.3.3. Facade and Atrium 92 4.3.3.1. Exterior of the Atrium 92 4.3.3.2. Interior of Atrium 92 4.3.4. Floor Slabs 93 4.3.5. Columns 96 4.3.6. Transfer Girders 99 Chapter 5 – CONCLUSIONS AND RECOMMENDATIONS 100 5.1. CONCLUSIONS 100 5.2. RECOMMENDATIONS 103 References 104
vi
LIST OF FIGURES
Figure 1.1.1: Trends of the global disasters (Adramovitz 2001) 1 Figure 1.1.2: Distribution of global deaths by disasters 1985-99 (Adramovitz 2001) 2 Figure 2.1.1: Schematic diagram of Earthquake (Booth et al. 2006) 5 Figure 2.1.2: Multi story reinforced concrete structure collapsed in Mexico City,
1985 (Booth et al. 2006) 7
Figure 2.1.3: Ground story collapse (soft story) of a building during the Turkey earthquake in Erzincan, Turkey (Booth et al. 2006)
7
Figure 2.1.4: Beginning of a soft-story collapse of a building in Erzincan during the 1992 Turkey earthquake (Booth et al. 2006)
8
Figure 2.1.5: Upper story collapse of a multi story structure during the 1985 Mexico City earthquake (Booth et al. 2006)
8
Figure 2.1.6: Intermediate story failure in Hotel Decare Building during 1985 Mexico City earthquake (Booth et al. 2006)
9
Figure 2.1.7: Parapet wall failure on a building during 2001 Gujarat, India earthquake (Booth et al. 2006)
10
Figure 2.1.8: Beam Column Joint Failure in Erzincan, Turkey during the 1992 earthquake (Booth et al. 2006)
11
Figure 2.1.9: Bursting failure of a column in Northridge, California during 1994 earthquake (Booth et al. 2006)
11
Figure 2.1.10: Shear failure of a column in St. Johns, Antigua during 1974 earthquake (Booth et al. 2006)
12
Figure 2.1.11: Out of plane failure of an unreinforced masonry wall (Booth et al. 2006)
13
Figure 2.1.12: View of the collapsed Margalla Towers after the 2005 earthquake (Pakistan earthquake web site 2007)
14
Figure 2.1.13: Damage caused by the 1994 Northridge earthquake (Northridge earthquake web site 2007)
15
Figure 2.1.14: Damage caused by the 1994 Northridge earthquake (Northridge earthquake web site 2007)
16
Figure 2.2.1: Mechanical explosion in an Industry (Explosions web site 2007) 18 Figure 2.2.2: Structure affected by sewer explosion (Explosions web site 2007) 18 Figure 2.2.3: Building affected by LP gas explosion (Explosions web site 2007) 19 Figure 2.2.4: Cloud formed after nuclear explosion (Explosions web site 2007) 19 Figure 2.2.5: Shock wave and pressure wave (ASCE 1997) 20 Figure 2.2.6: Damaged stories of the Alfred P. Murrah Federal Building, Oklahoma.
1995 (Oklahoma City web site 2007) 22
Figure 2.2.7: Damages to building and the surroundings after the 1995 Oklahoma City bombings (Oklahoma web site 2007)
22
Figure 2.2.8: WTC tower one after the 1993 explosion in the parking lot (WTC web site 2007)
23
Figure 3.1.1: Reinforcement details of the beam-column specimen (Ghobarah et al. 2001)
26
Figure 3.1.2: Experimental set up for the beam-column joint testing (Ghobarah et al. 2001)
28
vii
Figure 3.1.3: Cyclic loading applied to the free end of the beam (Ghobarah et al. 2001)
29
Figure 3.1.4: Location of strain gauges on the reinforcement. (Ghobarah et al. 2001) 30 Figure 3.1.5: Rehabilitation scheme for the beam-column joint (Ghobarah et al.
2001) 30
Figure 3.1.6: Beam-column joint with the FRP rehabilitation (Ghobarah et al. 2001) 31 Figure 3.1.7: FRP laminate failure of specimen T1R (Ghobarah et al. 2001) 33 Figure 3.2.1: Geometry of the columns specimen used in the testing (Ozbakkalogu
et al. 2007) 36
Figure 3.2.2: Reinforcement arrangement used in specimen RS-1 (Ozbakkalogu et al. 2007)
37
Figure 3.2.3: Reinforcement arrangement used in specimen RS-2 (Ozbakkalogu et al. 2007)
37
Figure 3.2.4: Reinforcement arrangement used in specimen RS-3 (Ozbakkalogu et al. 2007)
38
Figure 3.2.5: Reinforcement arrangement used in specimen RS-4 (Ozbakkalogu et al. 2007)
38
Figure 3.2.6: Reinforcement arrangement used in specimen RS-5 (Ozbakkalogu et al. 2007)
39
Figure 3.2.7: Reinforcement arrangement used in specimen RS-6 (Ozbakkalogu et al. 2007)
39
Figure 3.2.8: Wooden templates used to make the FRP casings (Ozbakkalogu et al. 2007)
40
Figure 3.3.1: Failure of the steel bars of the column and slippage of the steel bars of the added jacketing (Julio et al. 2003)
46
Figure 3.3.2: Specimens prepared by sand-blasting (Julio et al. 2003) 48 Figure 3.3.3: Application of epoxy resin on specimen (Julio et al. 2003) 49 Figure 3.3.4: Steel connectors epoxy bonded on push off specimens (Julio et al.
2003) 50
Figure 3.3.5: Concrete casting of the jacket (Julio et al. 2003) 52 Figure 3.4.1: A four story building that’s been rehabilitated in Dinar (Sucuoglu et
al. 2004) 56
Figure 3.4.2: The Rehabilitated scheme of the four stories structure in Dinar, ground floor plan (Sucuoglu et al. 2004)
58
Figure 3.4.3: Eight story damaged building in Ceyhan (Sucuoglu et al. 2004) 59 Figure 3.4.4: Rehabilitation scheme of the eight stories building in Ceyhan, ground
floor plan (Sucuoglu et al. 2004) 60
Figure 3.5.1: Different types of base isolation systems (Guerreiro et al. 2006) 63 Figure 3.5.2: Example of retro-fitting a RC building with base isolation (Guerreiro
et al. 2006) 63
Figure 3.5.3: Los Angeles City Hall rehabilitated with base isolators (Guerreiro et al. 2006)
64
Figure 3.5.4: Arrangement of a viscoelastic damper (Guerreiro et al. 2006) 65 Figure 4.1.1: Test setup for testing the effectiness of the spary-on polymer
retrofitting method (Davidson et al. 2004) 69
Figure 4.1.2: Instrumentation plan (Davidson et al. 2004) 70
viii
Figure 4.1.3: Test 1 reflected pressure: gauge R1 and R2 (Davidson et al. 2004) 71 Figure 4.1.4: View of the damaged walls after test 1 (Davidson et al. 2004) 72 Figure 4.1.5: Test 3 Result: wall panels on reaction structure (Davidson et al. 2004) 74 Figure 4.1.6: Test 3 Result: Wall panels on test cubicles (Davidson et al. 2004) 75 Figure 4.1.7: Tearing of the polymer on the inside from Test 3 (Davidson et al.
2004) 76
Figure 4.2.1: Typical floor plan of the structure (Bob 2004) 79 Figure 4.2.2: View of the damaged transverse walls (Bob 2004) 80 Figure 4.2.3: View of the damaged floor-wall connection (Bob 2004) 80 Figure 4.2.4: View of the damaged RC floor (Bob 2004) 81 Figure 4.2.5: strengthening with RC Coating (Bob 2004) 82 Figure 4.2.6: strengthening of walls with CFRP (Bob 2004) 83 Figure 4.2.7: Installation of CFRP to strengthen floors (Bob 2004) 83 Figure 4.2.8: Strengthening of floors with CFRP (Bob 2004) 84 Figure 4.2.9: Strengthening with RC sheets, columns and longitudinal beams (Bob
2004) 85
Figure 4.2.10: Local strengthening of columns and beams with RC jacketing (Bob 2004)
85
Figure 4.2.11: Strengthening of floors with CFRP (sika wrap) (Bob 2004) 86 Figure 4.3.1: Elevation view of the building (Ettouney et al. 1996) 87 Figure 4.3.2: Plan view of the building (Ettouney et al. 1996) 88 Figure 4.3.3: Isometric view of the building (Ettouney et al. 1996) 88 Figure 4.3.4: Failure mechanism of the flat slab (Ettouney et al. 1996) 93 Figure 4.3.5: Effects of blast loading on columns (Ettouney et al. 1996) 94 Figure 4.3.6: Lateral load carrying mechanism and effects after the blast (Ettouney
et al. 1996) 94
Figure 4.3.7: High and low vulnerability locations (Ettouney et al. 1996) 95 Figure 4.3.8: Flat slab improvements (Ettouney et al. 1996) 95 Figure 4.3.9: Direct lateral loading of column (Ettouney et al. 1996) 97 Figure 4.3.10: Uplifting on the columns (Ettouney et al. 1996) 97 Figure 4.3.11: Progressive collapse mechanism (Ettouney et al. 1996) 99
ix
LIST OF TABLES Table 3.1.1: GFRP material properties. (Ghobarah et al. 2001) 27 Table 3.2.1: FRP casing and crosstie details (Ozbakkalogu et al. 2007) 42 Table 3.2.1: Reinforcement details (Ozbakkalogu et al. 2007) 42 Table 4.1.1: Average tensile strength properties obtained from the tests (Davidson
et al. 2004) 67
Table 4.1.2: Properties of Polyurea (Davidson et al. 2004) 68 Table 4.1.3: Material Properties obtained for the tests (Davidson et al. 2004) 68 Table 4.1.4: Gauge measurements obtained from Test 1 (Davidson et al. 2004) 71 Table 4.1.5: Gauge measurements obtained from Test 2 (Davidson et al. 2004) 73 Table 4.1.6: Gauge measurements obtained from Test 3 (Davidson et al. 2004) 75 Table 5.1.1: Rehabilitation techniques for resisting earthquake loading 101Table 5.1.2: Rehabilitation techniques for resisting blast loading 102
x
Chapter 1
INTRODUCTION
1.1 BACKGROUND
Over the years the total number of disasters is continually increasing. During the last
century the number of deaths due to disasters, which include earthquake, flood, wind
storm, hurricane, tornado, etc., was more than 10 million. The economic losses due to the
catastrophes has also been rising, as is evident from Figure 1.1.1 where it is seen that the
economic losses rose from nearly 40 billion dollars in 1950’s to 600 billion dollars in
1990’s. Of all the disasters, earthquake accounts for nearly one-third of the total global
deaths (Figure 1.1.2).
Figure 1.1.1: Trends of the global disasters (Adramovitz 2001)
Earthquake is a very common phenomenon in many parts of the United States. The major
areas of significant seismic hazard in the US are California, the Pacific North West,
Nevada, Idaho, Montana, Utah and Colorado. There is also a significant risk in the
Central, Northeastern and Southeastern part of the country. Over the years, US has
witnessed myriads of major earthquakes that resulted in significant property loss and
1
death toll. Examples include the 1811-12 New Madrid earthquake (Richter magnitude of
8.0 – 8.6), the 1971 San Fernando Valley earthquake (Richter magnitude of 6.6), the
1979 El Centro earthquake which is also known as the Imperial Valley earthquake
(Richter magnitude of 6.6), the 1989 San Francisco California earthquake (Richter
magnitude of 7.8), and 1994 Northridge earthquake (Richter magnitude of 6.7). The 1994
Northridge earthquake resulted in a property loss of over 20 billion and over 112,000
older building were damaged. The 1989 San Francisco earthquake caused a property
damage of 524 million dollars and the death toll of 3000. The 1886 Charleston, South
Carolina earthquake killed about 60 people and the property damage was estimated to be
6 million in 1999 dollars (Adramovitz 2001).
Figure 1.1.2: Distribution of global deaths by disasters 1985-99 (Adramovitz 2001)
The design of the existing buildings that were built as per the old design codes did not
take into account the issues of ductility. Even the latest codes cannot guarantee a
complete protection against earthquakes but they do minimize the effects. Most of the
older buildings are at risk in the event of an earthquake. Since it is not economically
feasible to reconstruct all the old buildings as per the new seismic design codes, the only
feasible solution would be rehabilitating these structures. This will improve the ductility
characteristics of the structure for resisting earthquakes.
2
Over the years the number of explosions in commercial buildings and public facilities is
also increasing at a rapid rate. Examples include the Oklahoma City blast in 1995, the
Word Trade Center blast in 1993, Bombay (India) blast of 1993 and The Twin Tower
collapse of 2001. Although blast loading has not been given much importance in civil
engineering design, due to the frequency of recent occurrences it is advisable to consider
blast loading in the design of structures thereby improving their response to blast
loadings.
Many rehabilitation techniques for enhancing the ductility and strength of structures to
resist earthquake and blast loading have been developing over the years. Some of these
techniques include wrapping beam column joints with Fiber Reinforced Polymer (FRP)
composites, use of stay-in-place FRP confinements for RC columns, use of shear walls,
RC jacketing, base isolation and energy dissipation devices, and retrofitting of
unreinforced masonry walls. In this problem report an attempt has been made to review
these methods.
1.2 OBJECTIVE
The main objective of this report is to conduct a literature review on various
rehabilitation techniques used for enhancing the structural resistance to earthquake and
blast loading. The review discusses rehabilitation techniques such as wrapping beam
column joints with FRP composites, use of stay-in-place FRP confinements for RC
columns, use of shear walls, RC jacketing, base isolation and energy dissipation devices,
and retrofitting of unreinforced masonry walls.
1.3 REPORT ORGANIZATION
This problem report consists of five chapters. The first chapter presents a brief
background, objectives and scoop of the study. Chapter 2 briefly discusses earthquakes,
earthquake damages, blast, blast damages and past experiences. Chapter 3 presents an
extensive literature review of earthquake rehabilitation techniques. Blast rehabilitation
techniques are reviewed in Chapter 4. Chapter 5 summarizes the conclusion and
recommendations. This is followed by a list of references cited in the text.
3
Chapter 2
EARTHQUAKE AND BLAST
This chapter provides a brief introduction to earthquake and blast loadings and also
discusses various details like the types of earthquakes, failure during earthquakes,
examples of past earthquakes, types of explosions, pressure waves, blast wave
parameters, and examples of previous explosions.
2.1 EARTHQUAKE
Earthquakes occur due to the forces within the earth crest to displace mass of rock
relative to each other. Stress is imposed on the lithosphere when the earth plates move.
When the stress is large and exceeds the capacity, lithosphere breaks or shifts. When
these plates move, they generate forces and when the forces are large they force the crust
to break. When the crust is cracked, stress is released in the form of energy which moves
along the surface of the earth as a wave, which we feel as earthquake (Booth et al. 2006).
2.1.1 Types of Earthquake
There are different types of earthquakes: tectonic, volcanic, collapse and explosion. The
type of earthquake that occurs depends on the geographical location and the make-up of
the region. The most common type of earthquake is the tectonic earthquake. Tectonic
earthquakes are caused due to the cracking of the earth’s crust by forces created by the
movement of the tectonic plates. Volcanic Earthquakes occur in conjunction with
volcanic activity. Collapse earthquake are relatively small earthquakes and occur at
locations near to mines and cravens. The major effect of these kinds of earthquakes is the
collapse of the roof of the craven or mine. Explosion earthquake occurs when a nuclear or
chemical bomb is detonated in a bore hole underground (Booth et al. 2006).
2.1.2 Quantifying Earthquake
There are two fundamental measures of an earthquake: earthquake magnitude and
earthquake intensity. Earthquake magnitude is the fundamental property of the
4
earthquake; it is the amount of energy released as measured on a logarithmic scale
(Richter Magnitude Scale). Earthquake intensity, as measured by the Modified Mercalli
(MM) Intensity Scale, on the other hand depends on the location of measurement. It
describes the effect of the earthquake on the people and building. In other words, the MM
scale is a measure of damage caused by an earthquake. As the distance from the epicenter
increases, the intensity of the earthquake decreases. As shown in the Figure 2.1.1 an
earthquake with a specific magnitude can have different intensities at different location as
the epicentral distance changes.
The two most common scales to measure the magnitude of the earthquake are body wave
magnitude mb (suitable for small magnitude events) and surface wave magnitude Ms
(most suitable for large events). Both measurements are measured by seismographs,
which measure ground tremors from a great distance. The third scale is the moment
magnitude, Mw, this is directly related to the amount of energy released in an earthquake.
This is suitable for all kinds of earthquakes (Booth et al. 2006).
Figure 2.1.1: Schematic diagram of Earthquake (Booth et al. 2006)
The displacement of the ground is denoted by ug and the displacement of the mass
relative to the ground is denoted as u. Then the total displacement of the mass is denoted
as ut (Chopra 2005).
5
ut(t) = u(t) + ug(t)
Both displacements ug and ut refer to the same inertial frame of reference and their
positive directions coincide. The relative motion u between the mass and the base due to
the structural deformation generates elastic and damping forces. When we consider the
concept of dynamic equilibrium between inertial, damping, and elastic forces:
fI + fD + fS = 0
The inertial force on the system is related to the mass and the acceleration on the mass ü
(Chopra 2005).
fI = m ü
Thus, the equation of dynamic equilibrium changes as follows
mü + ců + ku = - müg
This equation shows that the system behaves in the same way as when an external force
of - müg(t) is applied or a ground acceleration of - üg(t) is applied. Thus the relative
displacement u(t) of the structure due a ground acceleration of -üg(t) is similar to the
relative displacement u(t) due to an external force - müg (Chopra 2005).
2.1.3. Different Types of Structural Failures
Figures 2.1.1 to 2.1.5 show some of the types of structural failure in different parts of the
world during the last decade.
6
Figure 2.1.2: Multi story reinforced concrete structure collapsed in Mexico City, 1985
(Booth et al. 2006)
Figure 2.1.3: Ground story collapse (soft story) of a building during the Turkey
earthquake in Erzincan, Turkey (Booth et al. 2006)
7
Figure 2.1.4: Beginning of a soft-story collapse of a building in Erzincan during the 1992
Turkey earthquake (Booth et al. 2006)
Figure 2.1.5: Upper story collapse of a multi story structure during the 1985 Mexico City
earthquake (Booth et al. 2006)
8
2.1.4 Important Categories of Damage
When two buildings are very close to each other, during an earthquake two adjacent sides
of the buildings may pound into each other. This may cause a major damage, particularly
when the floor levels of the adjacent buildings are different. This is shown in Figure 2.1.6
where an intermediate story of the Hotel Decare was completely damaged. Appendages
to the building such as masonry parapets, cantilevers, roof tanks and pent houses behaved
badly during an earthquake. There are two reasons for this behavior. First reason is that
these structural members were not designed with adequate ductility. Second reason is the
effect of the dynamic amplification by the building to which they are attached (Figure
2.1.7).
Figure 2.1.6: Intermediate story failure in Hotel Decare Building during 1985 Mexico
City earthquake (Booth et al. 2006)
9
Figure 2.1.7: Parapet wall failure on a building during 2001 Gujarat, India earthquake
(Booth et al. 2006)
2.1.4.1 Reinforced Concrete Members
Buildings that consists of reinforced concrete beams and columns and which are not
properly braced by lateral walls providing lateral stiffness are very vulnerable to
earthquakes, unless special measures are taken to enhance the ductility of the ductility of
the structures (Booth et al. 2006).
The main vulnerabilities in RC structures are:
Failure of Beam-Column Joints (Figure 2.1.8)
Bursting Failure in Columns (Figure 2.1.9)
Shear Failure in Columns (Figure 2.1.10)
Soft Story Failure (Figure 2.1.3)
10
Figure 2.1.8: Beam Column Joint Failure in Erzincan, Turkey during the 1992
earthquake (Booth et al. 2006)
Figure 2.1.9: Bursting failure of a column in Northridge, California during 1994
earthquake (Booth et al. 2006)
11
Figure 2.1.10: Shear failure of a column in St. Johns, Antigua during 1974 earthquake
(Booth et al. 2006)
When inadequate transverse steel reinforcement is provided in a column, during an
earthquake the longitudinal bars carrying large axial loads and lateral loads buckle due to
insufficient confinement provided by the transverse reinforcement (Figure 2.1.9). In
Figure 2.1.10 the masonry wall stops below the full height of the column thereby creating
a short column liable to fail in shear rather than bending.
When buildings are built with their lower floor serving as the parking space without any
walls, the lateral stiffness of the building at the lower level is very low compared to the
upper levels. This causes the failure of the lower floor and ultimately a complete collapse
of the building. This is normally referred as a “Soft Story Failure”. Buildings with shear
walls have proven to be much more effective in resisting earthquakes compared to the
buildings without shear walls. The lateral stiffness of the buildings increase due to shear
walls and the buildings can resist earthquake loading better (Booth et al. 2006).
Ductility and Strength of structures and structural members play an important role in
withstanding earthquake forces. All frame elements must be designed in such a way that
12
they respond to a strong earthquake in a ductile fashion. Non-ductile modes such as shear
and bond failure must be avoided.
2.1.4.2 Structural Steel Members
Structural steel members exhibit the following types of failures during an earthquake.
Brittle failure of Bolts in shear or tension.
Member buckling.
Local web and flange buckling.
Large deflection of unbraced members.
Failure of steel members and other building elements (Booth et al. 2006).
2.1.4.3 Masonry Structures
Failure of both unreinforced and reinforced masonry is common. In-plane masonry is
very stiff so the forces transmitted by the ground motion are very high and masonry walls
are also very brittle so the failure in this case is a complete collapse or diagonal cracking
in both directions in the form of an “X”. Out of plane, free standing masonry walls are
highly vulnerable to earthquake and are liable to toppling failure (Figure 2.1.11).
Masonry walls that are mechanically connected on the sides and top of the wall are less
likely to have a toppling failure. Masonry walls with continues reinforcement are more
effective in avoiding total collapse (Booth et al. 2006).
Figure 2.1.11: Out of plane failure of an unreinforced masonry wall (Booth et al. 2006)
13
2.1.5 Previous Earthquakes
The Kashmir Earthquake (also known as the Great Pakistan Earthquake) was a major
earthquake with 7.6 magnitude on the Richter scale. The epicenter of the earthquake was
in Pakistan controlled Kashmir and the earthquake occurred at 8:50:38 Pakistan standard
time on October 8, 2005. The official death toll in Pakistan was 73,276, and 1,400 in
Jammu & Kashmir and 14 in Afghanistan.
One of the buildings famously known as the Margalla Towers (Figure 2.1.12), a 10 story
building, had collapsed completely in Islamabad killing most of the occupants. Although
the Margalla Towers was completely destroyed, neighboring buildings Al-Mustafa and
Park Towers stood their ground. This clearly points to the structural deficiency of the
collapsed building to withstand earthquake loads. The total property loss in the Pakistan
earthquake was around $2.3 Billion (Kashmir earthquake web site 2007).
Figure 2.1.12: View of the collapsed Margalla Towers after the 2005 earthquake
(Pakistan earthquake web site 2007)
14
The Great Chilean Earthquake of May 22, 1960, was a major earthquake with a Richter
magnitude of 9.5. It occurred in the early afternoon 19:11 (UTC) and this resulted in a
tsunami that affected southern Chile, Argentina, Hawaii, Japan, the Philippines, eastern
New Zealand and the Aleutian Islands in Alaska. The epicenter of the earthquake was in
Valdivia, Chile 700 kilometers south of Santiago. This caused localized tsunami waves
that reached heights of 25m. These waves were 10.7 meter at a distance of 10,000
kilometers from the epicenter. The total fatalities in this earthquake as published in the
USGS citing studies state figures of 2231, 3000, or 5700 killed. The total estimated
monetary costs are 400 million to 800 million dollars (after adjusting for inflation, it
would be around 2.6 to 5.2 billion in 2005 dollars) (Chile earthquake web site 2007).
The Northridge earthquake occurred on January 17, 1994. This earthquake hit the city of
Los Angeles, California at 4:31 AM and the magnitude of the earthquake was 6.7 on the
Richter scale. The ground acceleration recorded is the maximum that’s ever recorded in
urban area in North America. This earthquake produced unusually strong ground
acceleration in the range of 1.0g. The total death toll in this earthquake was 72 people and
the estimated property damage was $12.5 billions. Damages were also caused by fire and
landslides. In terms of property damage this earthquake is one of the worst natural
disasters in the United States (Northridge earthquake web site 2007).
Figure 2.1.13: Damage caused by the 1994 Northridge earthquake (Northridge
earthquake web site 2007)
15
Figure 2.1.14: Damage caused by the 1994 Northridge earthquake (Northridge
earthquake web site 2007)
2.2 BLAST
The need and requirements for blast resistant design has evolved in the recent years, in
the wake of unexpected events, like the terrorist attacks. The main focus is on the
structural aspects of design and rehabilitation of buildings for blast loadings. The blast
resistant design of buildings is one of the measures to minimize the risk to people and
facilities from the hazards of explosions.
2.2.1 Blast Resistant Design
The primary objectives of blast resistant design are to achieve improved personnel safety
and minimize financial losses. The primary goal in blast resistant design is to provide the
personnel in the building with the same level of safety as that of people outside the
building. In the recent past we have seen that most of the casualties in an event of a blast
are due to the collapse of the buildings, collapse of structural members or the material
shattered by the blast wave. Therefore, the main aim is to reduce the probability that the
building itself becomes a hazard in an explosion. The other main concern is to prevent the
huge financial losses after a blast in terms of building reconstruction cost. Also, buildings
16
often contain important information or serve important function (e.g., hospitals, hotels).
Business information and “loss of use” often have a very high value, so destruction of
buildings could cause significant financial losses.
The requirements for the buildings are greatly influenced by factors of distance from the
source (stand-off distance) and expected occupancy. For example, a building that is
situated far enough from any potential bomb threat may not need increased blast
resistance. If maintaining high standoff distance is not possible, then a high level of blast
resistance should be provided to the building (ASCE 1997), but this increases the cost.
When a building does not have enough stand-off distance from a potential blast source,
the building is exposed to damaging overpressure, so blast resistant design is
recommended for theses structures to improve their resistance to blast loading.
2.2.2 Types of Explosions
There are four general types of explosions:
1) Mechanical explosion
2) Chemical explosion
3) Nuclear explosion
4) Electrical explosion
Mechanical explosions (Figure 2.2.1) are those in which vessel failure or rupture of the
container is created by high pressure gas. When the gas stored in the container are
flammable, then in many instances a resultant fire occurs as long as there is an ignition
source or the temperature is above the ignition temperature of the gas (Explosions web
site 2007).
17
Figure 2.2.1: Mechanical explosion in an Industry (Explosions web site 2007)
Chemical explosions occur by generation of high pressure gas as a result of exothermic
reaction resulting from initiation of chemical explosives or fuel cells. Some of the fuels
that may cause a chemical explosion are flammable gases, vapors of combustible gases,
carbon monoxide and carbon dioxide explosions.
Figure 2.2.2: Structure affected by sewer explosion (Explosions web site 2007)
18
Figure 2.2.3: Building affected by LP gas explosion (Explosions web site 2007)
Nuclear explosions occur from the high quantities of heat and gases released during a
fusion or fission processes.
Figure 2.2.4: Cloud formed after nuclear explosion (Explosions web site 2007)
High energy electric arcs may sometimes generate sufficient heat to start an explosion.
Some times the electric arcs can heat the surrounding gases to a high temperature and
cause a mechanical explosion. A typical example of this kind of explosion is an electric
panel box that has been violently dislodged from the rest of the box. This typically
19
happens during a lightening strike or a high energy arc. This reaction may or may not
cause subsequent fire (Explosions web site 2007).
2.2.3 Blast Wave Parameters
The most important feature of an explosion is the sudden release of energy to the
atmosphere and creating a pressure transient, or blast wave. The blast wave travels
outward in all direction from the source of the explosion. The magnitude and the shape of
the blast wave depend on nature of the energy released and on the distance from the
epicenter of the explosion (ASCE 1997).
There are two types of blast waves.
Shock Wave: This has a sudden rise in the pressure from the ambient pressure to a peak
free field overpressure. Then the pressure reduces gradually to the ambient pressure with
some highly damped pressure oscillations. This results in a negative pressure wave
following the positive blast wave (Figure 2.2.5a).
Pressure Wave: This has a gradual increase in the side-on pressures and reaches the peak
free field overpressure and then gradually reduces to the ambient pressure and a negative
phase (Figure 2.2.5b) in the same wave as the shock wave.
(a) Shock wave (b) Pressure wave
Figure 2.2.5: Shock wave and pressure wave (ASCE 1997)
20
The area under the pressure-time graph is called the Impulse of the wave. So, the Positive
impulse of the wave is calculated as
∫=td
O dttPI0
).(
= 0.5 PSO td, for a triangular wave
= 0.64 PSO td, for a half-sine wave
= c PSO td, for a exponentially decaying shock wave
where,
P(t) = overpressure function of time
PSO = Peak, side on, or incident, overpressure
td = duration of positive phase
c = a value between 0.2 and 0.5 depending on PSO.
When the blast wave encounters a surface it will reflect off of the surface and the surface
experiences a pressure greater than the peak overpressure. That value is called the
reflected pressure, which can be calculated by the following formula (ASCE 1997).
Pr = Cr PSO
where,
Cr = reflection coefficient (dependent on the peak over pressure, angle of incidence of the
wave front and the type of wave).
2.2.4 Previous Explosions
On April 19, 1995 the Alfred P. Murrah Federal Building in Oklahoma City was attacked
by terrorists. The explosion partially destroyed the structure (Figure 2.2.6). The attack
claimed 168 lives and almost 800 people were injured. Prior to the terrorist attack on
September 11, 2001 on the World Trade Center, this was the most deadly terrorist attack
in the US. Figures 2.2.6 and 2.2.7 show the structural damages incurred by the building.
More than the blast itself, the main cause of the casualties is the destruction of the front
part of the building. Since this building had an access road on the front of the building
there was not much stand off distance. Hence a proper blast resistant design of the rebuilt
structure will make it safer in case of an explosion (Oklahoma web site 2007).
21
Figure 2.2.6: Damaged stories of the Alfred P. Murrah Federal Building, Oklahoma.
1995 (Oklahoma City web site 2007)
Figure 2.2.7: Damages to building and the surroundings after the 1995 Oklahoma City
bombings (Oklahoma web site 2007)
22
On February 26, 1993 a truck bomb was planted in the underground parking garage in the
Tower One of the World Trade Center in New York. The original intentions of the
terrorists were to damage one side of the structure and in turn make Tower One to
collapse over the second tower destroying both the towers and causing lot of deaths and
huge financial losses. Bu the tower withstood the explosion (Figure 2.2.8). Six persons
were killed in the explosion and almost 1,500 were injured (WTC web site 2007). When
there can be an explosion at this proximity to the structure, blast resistant design must be
carried out and all the previously built structural members must be retrofitted to resist
blast loading.
Figure 2.2.8: WTC tower one after the 1993 explosion in the parking lot (WTC web site
2007)
23
Chapter 3
REHABILITAION FOR EARTHQUAKE
Although all the structures are designed for static loads such as live load, snow load, dead
load, etc. When dynamic loading is considered, ductility plays a pivotal role. It is of
paramount importance that the existing structures are retrofitted and the ductility be
improved in order to effectively dissipate the energy. This chapter evaluates some of the
effective rehabilitation techniques that improve the ductility and strength of the structure.
3.1. BEAM-COLUMN JOINT REHABILITATION There are many structures that are designed before the existence of the seismic codes.
Structures with insufficient shear reinforcement lead to a brittle behavior of the beam-
column joint. In addition to the above, due to the strong beam design the joint may be
subjected to high shear demand. It has been observer from recent earthquakes, 1995
Hanshin-Awaji (Kobe, Japan) and 1999 Kocaeli (Turkey), that the brittle failure of the
frame joints was the main cause that many structure collapsed (Mitchell et al. 1996,
Mugurama et al. 1995). Due to the large extent of this problem, it is very important to
develop an economical methodology to transfer the brittle failure of the joint to beam
flexure hinging mechanism, which is more ductile type of failure.
There were few studies conducted in view of improving the strength, stiffness, energy
dissipation and ductility of the beam-column joint. Kaun (1999) investigated a
rehabilitation procedure for damaged beam-column joints. Specimens were initially
damaged and then rehabilitated by epoxy resin injection technique. Then the specimens
were tested in cyclic loading test until failure. This method proved effective in improving
the strength and the energy dissipation of the joint. This method was not effective in
restoring the flexural stiffness of the beam and the shear stiffness of the joint.
Beres et al. (1992) proposed a rehabilitation scheme for beam-column joints. In this
method flat steel plates were added to the top and the bottom of the beam and these plates
were bolted to the continuous plate on the out side of the joint. Improvement in the
24
strengthened specimen was reported. When the results of the original specimen were
compare to the results of the specimen after retrofitting, large deterioration was observed
in the original specimen after the ultimate strength was reached. Ghobarah et al. (2001)
investigated a rehabilitating technique for RC beam-column joints. Deficient RC beam-
column joints were encased in a corrugated steel plate. This technique is very use full in
enhancing the shear strength of the joint.
Though several rehabilitation techniques are available for beam-column joint, the use of
fiber reinforced polymer (FRP) material in the rehabilitation of RC beam-column joint
offers several advantages (Ghobarah et al. 2001):
FRP rehabilitation is a fast process and is also applicable in tight locations.
FRP rehabilitation is non-disruptive to occupants and the functioning of the
building
FRP materials are resistant to corrosion
FRP materials are light compared to other rehabilitation materials.
FRP rehabilitation is simple and effective
3.1.1 Experimental Program
This section describes the work conducted by Ghobarah et al. (2001) which involved
experimental study to evaluate the effectiveness of FRP wrapping of RC beam-column
joint.
3.1.1.1 Specimen Description
Ghobarah et al. (2001) constructed a reinforced concrete column beam joint sample. The
height of the column is 3000mm (118.11 in) and has a cross section of 250 x 400 mm
(9.84 x 15.74 in). The length of the beam is 1750mm (68.89 in) from the face of the
column to the free end. The beam cross section is 250 x 400 mm (9.84 x 15.74 in). The
column has been reinforced with 6 M20 bars and 2 M15 bars in the longitudinal
direction. M10 bars are used for transverse reinforcement. M10 rectangular ties are
spaced at 200mm (7.87 in) center to center starting 80 mm above and below the beam.
The beam has been reinforced with 3 M20 bars on the top and 3 M20 bars on the bottom.
25
M10 bars are used for transverse reinforcement. The ties are spaced at 150 mm (5.9 in)
for 600 mm (23.62 in) and then spaced at 200 mm (7.87 in) for 1000 mm (39.37 in) and
ending at 75 mm (2.85 in) from the free end of the beam. The reinforcement arrangement
of specimen is shown in the Figure 3.1.1. (Ghobarah et al. 2001).
This specimen is designated as T1 and has been tested as a controlled specimen. The joint
is then repaired and rehabilitated with Glass fiber reinforced polymer (GFRP) and the
rehabilitated specimen is designated as T1R and the test were conducted on T1R.
Figure 3.1.1: Reinforcement details of the beam-column specimen (Ghobarah et al. 2001) 3.1.1.2 Material Properties
The Concrete used in the construction of the Beam-Column joint has a compressive
strength of 30.8 MPa on the day of the test. The concrete used in the repair of the joint
has a compressive strength of 38 MPa. The yield stress of the reinforcing steel is 425 and
26
454 MPa for M20 and M10 bars, respectively. The available FRP materials are carbon
and glass. Carbon fibers have higher strength and higher modulus, they are more suitable
for joint shear rehabilitation. However, carbon fibers are almost six times costlier that the
glass fibers. Considering this a GFRP has been used for this rehabilitation. The GFRP
laminate is a product of Fyfe Co. and is available commercially. Properties of the GFRP
are presented in the Table 3.1.1.
Table 3.1.1: GFRP material properties. (Ghobarah et al. 2001)
GFRP Ultimate Tensile Strength, MPa
Ultimate Elongation, %
Elastic Modulus, MPA
Thickness, mm
Bi-directional (in the 450 direction)
552 1.7-4.0 27579 1.1
After the T1 specimen is tested, the joint area had been cleaned of the fractured concrete
by an air hammer exposing all the bars. The joint was cleaned of all the debris and fine
particles using compressed air. Fresh concrete was then added to the joint. After four
weeks the surface of the column was cleaned and the edges are rounded and the fiber
laminate was wrapped. The specimen was tested after another four weeks. (Ghobarah et
al. 2001)
3.1.1.3 Experimental Test Set-Up
The beam-column is tested with column vertical position and the column supported at the
bottom and top. Restrainers are provided at the top and bottom of the column to take the
horizontal load. There is a 600 kN axial load in the column. The load is applied from the
top using a vertical jack mounted at the top of the column. The axial load is equivalent to
0.2 Agf’c where Ag is the gross area of the column section. The free end of the beam is
them applied with a cyclic load using a high capacity 1100 kN actuator of ±250mm
stroke. A schematic representation of the experimental setup is shown in the Figure 3.1.2.
3.1.1.4 Loading Sequence
Specimens were tested under reverse cyclic load applied at the beam tip. The selected
forces are indented to cause forces that simulate high level of inelastic deformations that
27
are normally experienced by the frame during an earthquake. The selected load history
consists of two phases. The first phase is load-controlled followed by a displacement-
controlled loading phase. (Ghobarah et al. 2001)
Figure 3.1.2: Experimental set up for the beam-column joint testing (Ghobarah et al. 2001) In the first phase of the loading two cycles of 15% of the estimated strength of the
specimen were applied on the specimen to check the test setup and to ensure sure all the
data acquisitions are functioning accurately. This was followed by two cycles of 22 kN
load (Concrete cracking load of the beam). These were followed by two cycles of loading
that causes initial yield of the bottom longitudinal steel bars in the beam. The yield
causing loads for the specimens T1 and T1R are 109 kN and 117 kN respectively. The
displacement at the initial displacement of the steel, δy, is used in the displacement
controlled phase. The displacement ductility factor, µ, is defined as the ratio between the
beam displacement to the displacement at the first yield (Ghobarah et al. 2001).
28
The second phase of loading starts after the steel yields in the first phase. This phase is
displacement controlled phase. The specimen was subjected to increasing displacement
starting from δ/δy= 2 using multiples of displacement previously recorded. Two cycles
were carried out at different ductility levels 2.0, 2.5, 3.0, etc., to verify the specimen
stability. The cyclic loading sequence is shown in the Figure 3.1.3.
Figure 3.1.3: Cyclic loading applied to the free end of the beam (Ghobarah et al. 2001) 3.1.1.5 Instrumentation
Different types of instruments were used to measure the displacement, load and strains.
Fourteen strain gauges were used to measure the strain in the steel reinforcement bars.
The location of the strain gauges is shown in the Figure 3.1.4. Two diagonal LVDT’s
(linear variable differential transducers) were used to measure the joint deformations as
shown in Figure 3.1.2. To monitor the relative deformation of the beam with respect to
the face of the column, two LVDT’s located above and below the beam were used. One
LVDT was used to measure the displacement of the beam tip. One LVDT is used to
measure the displacement of the top of the column. To measure the axial load applied. To
measure the axial load applied to the top and bottom of the column two load cells were
installed on the vertical jack and the cyclic load actuator.
29
Figure 3.1.4: Location of strain gauges on the reinforcement. (Ghobarah et al. 2001)
Figure 3.1.5: Rehabilitation scheme for the beam-column joint (Ghobarah et al. 2001)
30
3.1.2 Rehabilitation Scheme
The proposed rehabilitation scheme for the beam-column joint consists of wrapping the
joint with one layer of GFRP laminate in the form of a “U”. The free ends of the laminate
are tied together by steel plates and threaded steel rods driven through the joint as shown
in the Figure 3.1.5 and Figure 3.1.6. The height of the laminate is restricted to the joint
region and the potential presence of a slab will prevent extending the laminate above the
joint. The FRP is not extended to the beam because it will cause an increase in the
flexural strength and that will adversely affect the relative strength ratios of the connected
beam and column. This rehabilitation will enhance the shear capacity of the joint and
provide confinement. This method enhances the strength and ductility of the joint
(Ghobarah et al. 2001).
Figure 3.1.6: Beam-column joint with the FRP rehabilitation (Ghobarah et al. 2001)
31
3.1.3 Experimental Results
In the specimen T1, first crack was observed on the column face. A diagonal shear crack
in the form of an X-pattern was found on the column face before the yielding of
longitudinal beam steel. The joint shear capacity reduced as the beam tip displacement is
increased. These cracks extended to the back of the column at failure. A considerable
degradation in strength occurred at ductility factor of 2, test was terminated at ductility
factor 2.5 when the load carrying capacity dropped to 30% of the maximum load.
(Ghobarah et al. 2001)
The T1R specimen which had been cracked from the initial testing is tested now. At a
ductility factor of 2.5 there is a slight delamination of the fiber as a slight finger tap on
the fiber revealed a hollow sound. The delamination area increased until it covered the
whole column face. The presence of the steel jacket prevented the premature failure of
the joint. The joint has been held in place by the jacket even after fiber delamination. Due
to the intentional under design of the fiber, failure of the fabric dint until a ductility factor
of 4. It started in the diagonal direction as a tear while pushing up, further tears extended
in the other diagonal from the extremities of the original tear. When the load is reversed,
the fiber material completely separated into two pieces revealing the failure of the
concrete underneath. The crack patterns are shown in Figure 3.1.7 (Ghobarah et al.
2001).
32
Figure 3.1.7: FRP laminate failure of specimen T1R (Ghobarah et al. 2001)
3.1.4 Summary
The original sample with no retrofitting in the joint region showed rapid strength
deterioration once the longitudinal steel of the beam started yielding. This was due to the
brittle shear failure of the joint. The rehabilitated specimen showed superior energy
dissipation characteristics compared to the original specimen. Use of higher yield and
strain hardening values for steel reinforcement than the nominal design values may result
in greater strength in the beam flexural capacity. This may cause excessive shear stresses
in the joint. This should be taken into account when seismic rehabilitation of beam-
column joint is carried out.
33
3.2 SQUARE HIGH-STRENGTH CONCRETE COLUMNS IN FRP STAY-IN-
PLACE FORMWORK
High strength concrete is superior to normal-strength concrete in terms of strength and
performance. The use of high strength concrete in buildings and bridges has been
increasing over the last two decades. However, the use of high strength concrete in
seismically active zones has been limited because of the fact that the increase in the
strength and performance has been achieved by compromising deformability. In a seismic
zone inelastic deformation and efficient energy dissipation are required to resist seismic
forces. High strength concrete structural elements exhibit brittle behavior at failure which
is not recommended for seismic loading.
Inelastic deformation of concrete can be improved by providing better confinement.
Significant lateral drift can be achieved without significant strength deterioration by
providing properly designed transverse reinforcement. When conventional steel ties,
hoops, overlapping hoops or spirals are used for high strength concrete the confinement
requirements are very high and are not acceptable. Using conventional confinements with
high strength concrete will create cage congestion and concrete filling problems. FRP
laminate offer a alternative and effective method to provide confinement to high strength
concrete (Ozbakkalogu et al. 2007).
FRP used as stay-in-place formwork have several advantages:
Light and provide effective framework with superior handling characteristics
Effective and has the ability to develop high lateral confinement pressures
Acts as a protective shell against corrosion, weathering and chemical attack
3.2.1 Experimental Procedure
Considering the confinement of the concrete column it has been long proven that spiral
confinement works effectively compared to a rectangular confinement. Similarly it has
been reported that FRP jackets are effective in circular columns than in square columns
(Mirmiran et al. 1998b, Pessiki et al. 2001). This can be explained by hoop tension that
34
develops in circular columns and helps in maintaining a uniform passive confinement
force. Whereas in square columns high confinement forces develop at the corners
As the corner radius (R) is increased, it promotes hoop tension in the fiber and improves
the effectiveness of the confinement. The cross-sectional size (D) affects the flexural
rigidity of the FRP fiber between the corners and thereby affecting confinement
efficiency. These two parameters can be expressed as ration R/D. Two R/D ratios were
used for this experimental procedure 1/16 and 1/34.
Internal crossties are required in conventionally reinforced columns; they improve the
distribution of lateral loads and restrict the concrete from expanding and improving the
confinement action. A similar concept is used to provide crossties in the FRP stay-in-
place formwork (Ozbakkalogu et al. 2007).
3.2.2 Test Specimens
A total of six specimens were prepared and each of them has a 270 mm square cross
section and a 1720 mm cantilever height. The shear span of each column is 2000mm
measured to the point of load application, which is 280mm above the beam. These
specimens represent the lower half of the first story building column. The specimen
configuration is shown in Figure 3.2.1.
35
Figure 3.2.1: Geometry of the columns specimen used in the testing (Ozbakkalogu et al.
2007)
High strength concrete, with cylinder strengths 75 MPa and 90 MPa, was used to cast the
columns. A clear cover of 20mm is provided, measuring from the face of the column to
the outside of the longitudinal reinforcement. Three different sets of reinforcement
arrangements are used 4-bar, 8-bar, and 12-bar. For the latter two arrangements number
15 deformed steel bars with yield strength of 500 MPa are used and for the arrangement
with 4-bars number 20 bars are used with yield strength of 476 MPa (Ozbakkalogu et al.
2007).
Following are the description of the arrangement of the reinforcement and the FRP
formwork and crossties for different specimens.
RS-1
Specimen RS-1 has four number 20 bars for reinforcement and has five plies of FRP in
the casing. The corner radius for this specimen is 45mm.
36
Figure 3.2.2: Reinforcement arrangement used in specimen RS-1 (Ozbakkalogu et al.
2007)
RS-2
Specimen RS-2 has eight number 15 bars for reinforcement as shown in the Figure 3.2.3
and has five plies of FRP in the casing. The corner radius for this specimen is 45mm.
This specimen also has FRP crossties in both the cross-sectional direction.
Figure 3.2.3: Reinforcement arrangement used in specimen RS-2 (Ozbakkalogu et al.
2007)
RS-3
Specimen RS-3 has twelve number 15 bars for reinforcement as shown in the Figure
3.2.4 and has five plies of FRP in the casing. The corner radius for this specimen is
45mm. This specimen has two crossties in each of the cross-sectional direction separated
by a distance of 68mm, ¼ of the column dimension.
37
Figure 3.2.4: Reinforcement arrangement used in specimen RS-3 (Ozbakkalogu et al.
2007)
RS-4
Specimen RS-4 has eight number 15 bars for reinforcement as shown in the Figure 3.2.5
and has three plies of FRP in the casing. The corner radius for this specimen is 45mm.
Figure 3.2.5: Reinforcement arrangement used in specimen RS-4 (Ozbakkalogu et al.
2007)
RS-5
Specimen RS-5 has eight number 15 bars for reinforcement as shown in the Figure 3.2.6
and has two plies of FRP in the casing. The corner radius for this specimen is 45mm.
38
Figure 3.2.6: Reinforcement arrangement used in specimen RS-5 (Ozbakkalogu et al.
2007)
RS-6
Specimen RS-6 has eight number 15 bars for reinforcement as shown in the Figure 3.2.7
and has three plies of FRP in the casing. The corner radius for this specimen is 8mm.
This specimen also has FRP crossties in both the cross-sectional direction.
Figure 3.2.7: Reinforcement arrangement used in specimen RS-6 (Ozbakkalogu et al.
2007)
3.2.3 Material Properties
3.2.3.1 Carbon FRP composite
Carbon fiber is preferred over glass fiber because of the fact that carbon fibers exhibit
higher elastic modulus and tensile strength of the material, which is more compatible
with high modulus and high strength concrete. The normal thickness of the carbon fiber
39
sheet is 0.165mm/ply and this has been increased to 0.8mm/ply after the laminate has
been impregnated with epoxy resin. The same FRP composite has been used for all the
casings and the fiber is allied in the transverse direction (Ozbakkalogu et al. 2007).
The manufacturing process for the FRP casings was done by wrapping impregnated FRP
sheets around a wooden template. For the columns with 45mm corner radius, PVC tubes
were used for rounding the corners. For the columns with 8mm corner radius wooden
quarter rounds were used for rounding the corner as shown in the Figure 3.2.8.
Figure 3.2.8: Wooden templates used to make the FRP casings (Ozbakkalogu et al.
2007)
The wrapping of the casings were done layer by layer. Each layer had a overlap of
100mm in the direction of the fiber to ensure proper bonding. There is no overlap of
adjacent layers along the height of the column. Hand lay-up technique used here resulted
in good quality casings, an advanced automated method like centrifugal casting, filament
winding or pultrusion may offer better quality.
40
The crossties were also made out of the same FRP fiber that is used in the preparation of
the casings. Crossties were prepared by wrapping the FRP around a low tensile strength
phenolic bar. The phenolic bar doesn’t contribute to the strength of the crosstie, but
simple act as a template (Ozbakkalogu et al. 2007).
Two different fiber contents were used in preparing the crossties. In the specimen RS-2
and RS-3, 40mm strips of fiber are used to make the crossties. The crossties were mainly
provided to resist against lateral expansion of concrete. The contribution of crossties to
the total fiber cross-section area is very small.
In the specimens RS-5 the number of plies in the casing was reduced by one layer and the
reduced amount of fiber was used to make the crossties. The thickness of the crosstie for
RS-5 is 136mm. The total area of fiber for the specimen RS-5 with two plies in casing
and crossties is equal to that of specimens RS-4 and RS-6 with 3 plies in casing and no
crossties (Ozbakkalogu et al. 2007).
3.2.3.2 Concrete Properties
Two concrete mixes were used to make the six specimens. First three specimens RS-1,
RS-2 and RS-3 are made from 10SF cement and crushed lime stone with a maximum size
of 10 mm with a water cement ratio of 0.22. The target strength for this concrete is 90
MPa. The obtained concrete strength is 90.1 MPa. The second mix used to make the
specimens RS-4, RS-5 and RS-6 is a mixture of 10SF cement and crushed lime stone
with a maximum size of 10 mm. The water cement ratio used is 0.26 and the target
strength for this concrete is 75 MPa. Obtained concrete strength is 75.2 MPa. All
columns were cast vertically and vibrated thoroughly. The strength of the specimens was
monitored timely by testing cylinders. Tests were conducted when the average strength
reached the target strength.
3.2.3.3 Steel Reinforcement
Canadian standard No. 15 and No. 20 deformed bars with a nominal diameter of 16 mm
and 19.5 mm are used as longitudinal reinforcement with yield strength of 500 and 476
41
MPa. Mechanical spices are used to splice longitudinal bars at 500mm and 900mm from
the footing interface.
Table 3.2.1: FRP casing and crosstie details (Ozbakkalogu et al. 2007)
Column Shear Span
(mm)
f’c
(MPa)
Number
of plies R/D
Crosstie area
(mm2)
RS-1 2,000 90.1 5 1/6 0
RS-2 2,000 90.1 5 1/6 6.6
RS-3 2,000 90.1 5 1/6 2 x 6.6
RS-4 2,000 75.2 3 1/6 0
RS-5 2,000 75.2 2 1/6 22.3
RS-6 2,000 75.2 3 1/34 0
Table 3.2.2: Reinforcement details (Ozbakkalogu et al. 2007)
Column
fy
MPa
Reinforcement
arrangement
Longitudinal
reinforcement
ratio
RS-1 476 4 – No. 20 1.68
RS-2 500 8 – No. 15 2.24
RS-3 500 12 – No. 15 3.36
RS-4 500 8 – No. 15 2.24
RS-5 500 8 – No. 15 2.24
RS-6 500 8 – No. 15 2.20
3.2.4 Experimental Test Setup
The columns were fitted with linear variable displacement transducers and strain gauges
to measure the horizontal displacement, anchorage slip, horizontal and transverse strains
and rotation of plastic hinge. All equipment was connected to a microcomputer and data
acquisition system for recording and analyzing data.
42
Each column specimen was tested under incrementally increasing lateral deformation
reversals, simulating seismic load and a constant axial load. Two 1,000 KN capacity
computer servo-controlled MTS hydraulic actuators are placed vertically on two sides of
the column to simulate the axial load applied on the column due the stories above the
column. This column represents the first story column of a multi story building. The
specimens were tested with 30 or 34% of the total concentric capacity, Po, computed
using the following equation.
yssgco fAAAfP +−= )(85.0 '
Where, fc’ = compressive capacity of concrete
Ag = Gross area of the column section
As = Total area of longitudinal steel
The specimens were subjected to incrementally increasing lateral reversal loads. Three
cycles were applied at each of the drift ratio starting at 0.5% and increasing to 1%, 2%,
3%, etc., in the deformation control mode of the horizontal actuator. The lateral load was
applied on the specimen until it looses a large fraction of its maximum lateral load
resisting capacity. The rate of lateral loading was low and the typical duration of the test
is 4-5hrs, depending upon the deformability of the specimen (Ozbakkalogu et al. 2007).
3.2.5 Test Results
Specimens RS-1, RS-2, RS-3, RS-4 and RS-5 behaved almost in the same manner until
2% lateral drift ratio. Specimen RS-6 with small corner radius started demonstrating
signs of distress during the first cycle of 2% lateral drift. All the column specimens with
well rounded corners showed no visual damage until the end of the 2% lateral drift ratio
cycles. At 3% lateral drift ratio localized color change was observed on the FRP on the
column specimens RS-1, RS-4 and RS-5, which have either reduced plies or have no
crossties. This indicated in these columns specimens, there is separation of the FRP
laminate from the concrete due to crushing of concrete. A similar discoloration has been
observed in the column specimens RS-2 and RS-3 which have five plies and also the
crossties at 3% lateral drift ratio. The region discoloration increased as the lateral
43
displacement was increased until it is 540mm from the column-footing interface which is
twice the dimension of the column cross-section.
Specimen RS-6 started to expand into a circular shape beyond 2% lateral drift and at 4%
lateral drift ratio fiber rupture began. These phenomena are not prominent in the columns
with well rounded corners and crossties (Ozbakkalogu et al. 2007).
Specimens RS-1, RS-2 and RS-3 all have the same number of plies in the casing. RS-1
has no crossties, RS-2 has single crossties in each of the cross-sectional directions and
RS-3 has two crossties in each of the cross-sectional directions. Fiber rupture occurred in
RS-1 in the third cycle of 8% lateral drift ratio. Similarly in specimen RS-3 fiber rupture
occurred at 12% lateral drift ratio and in RS-2 before the fiber reached failure the test was
stop due to out of plane deformations after the completion of third cycle of 9% lateral
drift ratio.
Specimens RS-4 and RS-5 have the same amount of fiber per cross-section only
difference being RS-4 has three plies in the casing and RS-5 has two plies in the casing
with the rest of the fiber being used for crossties. Both these columns exhibited similar
behavior, with RS-4 failing at the first cycle of 7% lateral drift ratio and RS-5 failing at
third cycle of 6% lateral drift ratio (Ozbakkalogu et al. 2007).
3.2.6 Deformation of HSC Columns Confined by FRP Casing
The deformation of high strength concrete is a major concern due to the fact that high
strength concrete is brittle in nature, especially in the presence of axial load.
Deformability is a major factor in the seismic design of structure and the major drawback
of high strength concrete over normal concrete in terms of seismic design. The brittle
nature can be improved by the use of FRP casing and crossties.
When column with five plies of FRP and with an R/D ratio of 1/6 tested it developed 8%
lateral drift ratio. When the column with five plies of FRP in the casing, two crossties in
each direction of the cross-section and with R/D ratio of 1/6 it developed 11% lateral drift
44
ratio. When three plies are used instead of five plies for the casing and with the same R/D
ratio of 1/6 the maximum lateral drift ratio has decreased to 6%. However when the ratio
of corner radius to column dimension was minimized to R/D = 1/34 there is a substantial
reduction in the lateral drift capacity of the column and it developed only 2% lateral drift
ratio (Ozbakkalogu et al. 2007).
3.2.7 Summary
Due to the brittle behavior of the high strength concrete, the confinement requirements
are very high to resist earthquake loading and behave in a ductile fashion. FRP stay-in-
place confinement for high strength concrete will give better results compared to the
conventional steel confinement, covering the whole column. The ratio of the corner
radius to the cross-section dimension of the column (R/D) has a major effect on the
effectiveness of the FRP casing. Providing a rounded corner will prevent the premature
failure of the fiber due to high stresses at the corners. The use of FRP crossties will
improve the efficiency of the FRP confinement in the similar way over lapping hoops and
crossties do in the conventional steel confinements. The concept of integrated crossties in
FRP casing has proven to be effective.
3.3 REHABILITATION OF COLUMNS WITH REINFORCED CONCRETE JACKETS
An RC element can be repaired by attempting to restore the original strength and stiffness
of an RC element that is either damaged or deteriorated. There is a distinction between
cosmetic repair and structural repair in his repair of RC columns. If the loss in strength is
lower than 10%, cosmetic repair is considered and if the decrease in strength is above that
value, structural repair is considered. Repairing a damaged RC element just by replacing
some of the original materials does not restore the characteristics of the original element.
Therefore, this method is acceptable only in the case of cosmetic repair (Julio et al.
2003).
3.3.1 Added Longitudinal Reinforcement
One of the advantages of RC jacketing strengthening of columns is that the increase in
stiffness of the structure is distributed uniformly distributed as compared to addition of
45
shear walls or bracing. While jacketing an existing column the added longitudinal
reinforcement bars must be anchored to the foundation. In this method usually it is
necessary to execute a new foundation or at least strengthen the existing one (Julio et al.
2003).
Although several commercial products, effective in bonding the newly added longitudinal
steel to the foundation, are available care must be taken while executing this process.
Details must be considered to ensure proper bonding.
Julio (2001) conducted several test on RC columns strengthened by jacketing. The newly
added reinforcement for the jacketing was anchored to the footing using a commercially
available two component resin. Then the samples were submitted to monotonic tests, with
a constant axial load and increasing shear force and bending moments. The failure of the
longitudinal steel bars of the existing column and slippage of the newly added bars was
observed as shown in the Figure 3.3.1.
Figure 3.3.1: Failure of the steel bars of the column and slippage of the steel bars of the
added jacketing (Julio et al. 2003)
Pull out tests were conducted and it was concluded that slippage of the longitudinal bars
in the jacketing is the main reason of failure. This occurred due to the fact that the holes
46
drilled were not cleaned properly. Cleaning the driller holes with a vacuum cleaner is
enough from changing the failure from a slippage failure to tension rupture.
3.3.2 Slab Crossing
To retain the structural integrity the longitudinal bars added to the structure must go
through the slab and maintain continuity. For the longitudinal bars to pass through holes
must be drilled through the slab. Alcocer et al. (1993) indicates that the use of column
distributed reinforcement is better that column bundles to reduce the possibility of bond
damage. But in the case of a column beam system there is always a possibility of
interrupting the middle bars, so longitudinal reinforcement can be provided in the corners
so as to avoid the interruption.
3.3.3 Interface Surface Preparation
It is important to prepare the interface to achieve good bond between the original column
and the added concrete, so that the whole unit acts monolithically. There are several
methods in use to improve the surface roughness of the original columns. Following are
some of these techniques (Julio et al. 2003).
3.3.3.1 Methods to Increasing Surface Roughness
Several methods are used in increasing the roughness of the original column and thereby
increasing the bond between the original column and jacket. Following are some of the
methods to improve the surface roughness (Julio et al. 2003):
1. Hand Clipping
2. Sand Blasting
3. Jack Hammering
4. Electric hammering
5. Water Demolition
6. Iron Brushing
Roughness of the original column surface is a important factor for the strength of the
column but that has been quantified.
47
Samples made with different surface roughening methods were studied for the bond
strength of the original concrete and the jacket. One important conclusion is that
pneumatic hammering causes micro cracks in the substrate. This is one of the methods
predominantly used to increase the surface roughness. This method has to be avoided
since it has been proved that the mechanical action of the hammer weakens the joint.
Julio et al. (2003) conducted several experiments to study the influence of the interface
between concretes of different ages on the strength of the joint. The surface prepared by
different techniques on left as cast specimens were tested. Slant shear test and pull-off
test were conducted on specimen interface prepared by sand blasting (Figure 3.3.2),
prepared by electric hammering and treated with iron brushing. It has been observer that
sand blasting is the most effective of the methods considered.
Figure 3.3.2: Specimens prepared by sand-blasting (Julio et al. 2003)
3.3.3.2 Surface Pre-wetting
The question of pre-wetting the surface is inconclusive. The AASHTO-AGB-ARTBA
joint committee recommended that the original surface must be dry before the new layer
of concrete is cast. The Canadian Standards Association standard A23.1 recommends the
original concrete surface be wetted for at least 24 hours before the cast of the new
concrete.
48
A critical amount of moisture must be maintained in the substrate to achieve maximum
strength. An excess amount of moisture in the substrate will close the pores and prevent
the absorption of the repairing material. An excessively dry substrate can absorb too
much water from the repairing material causing excessive shrinkage in the repairing
material. A saturated substrate with a dry surface is considered the best solution (Julio et
al. 2003).
3.3.3.3 Application of Bonding Agents
There are some published works on the effectiveness of the adhesion between repair
materials and concrete substrates with bonding agents. The conclusion reached by
different authors is not always the same. Due to the enormous variety of parameters
influencing the interference strength the results obtained are not comparable.
Julio et al. (2003) conducted slant shear tests and pull-out test on specimens with
different interfaces. Specimens were prepared by different techniques of surface roughing
like sand blasting, electric hammering and iron brushing and two component epoxy resin
was used as a bonding agent as shown in Figure 3.3.3 and the specimens were tested. The
value of the shear and tensile strength of the specimen reduced when epoxy resin was
used with sand blasting, while shear and tensile strength increased when epoxy resin is
used with the other techniques.
Figure 3.3.3: Application of epoxy resin on specimen (Julio et al. 2003)
49
3.3.3.4 Addition of Steel Connectors
Steel connectors (Figure 3.3.4) play an important role in case of precast RC beams with
in situ cast slabs. Julio (2001) conducted push-off on specimens to analyze the effect of
steel connectors on the interface strength. Julio conducted tests on seven different
specimens with seven different surface penetrations were considered. It was observed that
the addition of the steel connectors did not increase the debonding strength but increased
the longitudinal shear strength considering the slippage. Two commercial products were
used to anchor the steel connectors to the concrete. The fact that the steel connectors were
added after the concrete was cast by drilling holes dint reduces the joint strength.
Figure 3.3.4: Steel connectors epoxy bonded on push off specimens (Julio et al. 2003)
3.3.3.5 Testing of Different Methods
Julio (2001) conducted monolithic and cyclic tests on jacketed undamaged RC specimens
prepared by different methods. He considered six different specimens with different
interface treatments: a non strengthened column, a monolithic model, a column without
interface surface preparation, a column strengthened with interface surface prepared by
50
sand blasting, a column with same roughness treatment as the previous specimen with
added steel connectors and a model where non-adhesive between the original column and
the added jacket was artificially induced. Except for the last specimen all other specimens
acted monolithically when subjected to monotonic test and cyclic tests. The major
conclusion of the author was contradictory to the current practice in some countries.
There is no need to improve the interface surface or use any bonding agent to improve the
joint strength for undamaged RC columns.
3.3.4 Spacing of Added Stirrups
The coefficient of monolithic behaviors of the RC columns strengthened by jacketing has
been evaluated and it has been concluded that a higher percentage of transverse
reinforcement gives better confinement to the strengthened column to achieve better
monolithic performance. It has been recommended that half the value of the transverse
reinforcement spacing in the original column be adopted for the transverse reinforcement
spacing on the strengthening jacket.
3.3.5 Temporary Shoring of the Structure
One of the major factors in strengthening of a column is how it has been done.
Strengthening of a loaded column is lot different from strengthening of an unloaded
column. When a loaded column is strengthened the original column is resistant to these
and to the loads already applied. In the second case where an unloaded column has been
strengthened the composite structure of the original column and the RC jacket will act as
a unit and resist the total load. When a combined action of the original column and the
RC jacket is desired, the load on the column must be temporarily transferred to a
temporary shoring so as to strengthen the column as an unloaded column (Julio et al.
2003).
3.3.6 Properties of Added Concrete
Normally the added concrete has aggregate of maximum dimension of 2mm because of
the lack of space in the jacket. For the same reason self compacting concrete (SCC) is
used for jacketing. This is due to the diminished thickness occupied by the concrete due
51
to the volume occupied by the steel. For this reason high strength concrete (HSC) is a
good option while strengthening RC columns with concrete jackets. High strength
concrete is obtained by silica fume addition. Since the substrate of the original concrete is
much older than the new concrete used or the jacketing, it is recommended to use
concrete with less shrinkage.
Julio (2001) conducted test studying the effect of the strength of the joint when different
strength concrete were used in the jacketing procedure. It has been concluded that the
strength of the joint increased as the nominal strength of the concrete used for the
jacketing increased. When high performance concretes (HPC) were used the failure mode
shifted from interface rupture to monolithic failure. Hence HPC is preferred option for
RC column jacketing.
Figure 3.3.5: Concrete casting of the jacket (Julio et al. 2003)
3.3.7 Structural Behavior
A significant increase in the strength and ductility of the columns can be achieved with
this rehabilitation. This method will also alter the overall behavior of the building.
52
Alcocer et al. (1990) conducted several experiments on RC columns strengthened by
jacketing; the specimens were tested by applying bidirectional cyclic loading. The
authors have concluded that jacketing of RC columns can change a system from weak
column strong beam to strong column weak beam scenario.
3.3.7.1 Effect of Damage on Structural Behavior
There is a lot of difference in strengthening a healthy column and heavily damaged
column. Alcocer et al. (1993) conducted experimental test on jacketed RC frames, by
jacketing the most damaged elements, joints and columns, the strength values obtained in
the test at 2% drift was 63% of the undamaged specimen and the stiffness values
obtained at 0.5% drift is 52% of the values obtained for a undamaged specimen.
Rodriguez et al. (1994) performed tests to see the effect of jacketing on damaged and
undamaged specimens to investigate the increase of strength, stiffness and ductility of the
specimens under seismic load conditions. The author built specimens as per the 1950s
New Zealand code and concluded that these specimens have low ductility and were not
suitable for seismic loading. These specimens were jacketed and tested. The author
concluded that the ductility of the jacketed specimens was almost three times the original
as build columns. The author also mentioned that the extent of damage and the
reinforcement details had very little influence on the overall seismic performance.
3.3.8 Summary
RC jacketing technique improves the strength and stiffness of the column. Unlike other
methods this method leads to a uniform increase in the strength and stiffness of the
member. This method does not need any specialized workmanship and this makes RC
jacketing a valuable choice for structural rehabilitation. In this method attention must be
paid to the following aspects.
• The use of hand clipping, jack hammering, electric hammering to remove the
damaged concrete causes micro cracks in the substrate, so sand blasting or water
demolition techniques must be used.
53
• For undamaged columns no additional interface surface preparation is required
except for short columns. Where ever interface surface preparation is necessary
sand blasting or water demolition techniques must be used.
• Use of bonding agent – a two-component epoxy resin is most commonly used.
When trying to improve the roughness of the interface surface an effective
method like sandblast is sufficient. When epoxy resin is used along with sand
blasting technique reduction in the strength is observer, hence this must be
avoided.
• Application of steel connectors – these must be used only in case of short
columns to improve the level of strength and stiffness under cyclic loadings.
• Temporary shoring – care must be takes in such a way that the concrete jackets
resists part of the total load rather than part of the incremental loads on the
column.
• Continuity of the longitudinal bars through the slab is must to retain the integrity
of the structure. So holes must be drilled to allow the longitudinal bars to pass
through the slab.
• The longitudinal reinforcement must be spread uniformly on all sides of the
column. When ever this is not possible care must be taken to avoid excessive
bundling at the corners.
• Added stirrups – stirrups in the jacketing must be placed with a spacing of half the
spacing that is used in the original column’s stirrups.
• Added concrete – self-compacting, high-strength and high-durability concrete,
non shrinkage concrete must be used.
3.4 SEISMIC REHABILITATION BY ADDING SHEAR WALLS
After the 1995 Dinar and 1996 Adana-Ceyhan earthquakes that measured 6.0 and 6.2
magnitude, several buildings are damaged in the towns of Dinar and Ceyhan in Turkey.
Under the guidance of the Earthquake Engineering Research Center of the Middle East
Technical University a total of 130 moderately damaged structures are rehabilitated.
54
The following are the main factors leading to the building damages in Dinar and Ceyhan
(Sucuoglu et al. 2004):
There is no closely spaced confinement reinforcement at beam column joints.
Beams were generally stronger than columns in all stories.
The measured concrete strength is usually less than 15 MPa.
Plain reinforcement with yield strength of 220 MPa bars is used in all buildings.
Sufficient anchorage lengths were not provided for longitudinal reinforcement.
Transverse beam and column are not providing enough confinement.
3.4.1 Rehabilitation Method
Considering the weaknesses of the structure, damaged condition, constrain of completion
of rehabilitation in limited time, a simple technique of rehabilitation has been used for all
the buildings that are damaged. The system used in the rehabilitation of the buildings is to
add concrete shear walls in the existing structure. The newly added shear wall system
will act as the primary system for the seismic loads while the existing system will be the
secondary system. The existing frame work will still be the primary load bearing system
for the gravity loads (Sucuoglu et al. 2004).
3.4.2 Design criteria for seismic design
Since the newly added shear walls must act as the primary system resisting the seismic
loads, the design criteria adopted must ensure that the shear walls added sufficient
stiffness and strength rehabilitated system. Thus, the new walls and the connections were
to take the maximum lateral load and reduce the lateral deformations to acceptable level.
The following are the design criteria adopted (Sucuoglu et al. 2004):
Seismic design was conducted as per the Turkish code.
The material properties that are obtained in the in-situ testing were used in the
design.
The newly added shear walls have to resist at least 70% of the lateral load.
The axial loads in the columns developed both due to the seismic loads and
gravity loads combined must be less than 50% of the axial load capacity of the
column. Otherwise columns are strengthened to increase the axial load capacity.
55
In both the orthogonal directions, the ratio of the cross sectional area of the shear
walls and the total floor area has to be more than 0.002.
Confinement reinforcement was provided at the edges of the shear walls adjacent
to the columns.
The continuity of the vertical bars in the shear walls is maintained by providing
vertical dowelled bars.
To resist the over turning moment, new foundations were provided under the
newly added shear walls.
3.4.3 Four Story Building in Dinar
The four story structure that is shown in the Figure 3.4.1 has been damaged moderately in
the Dinar earthquake. It was rehabilitated by adding shear walls that extend all the way
from the ground floor to the top floor. The layout of the building and the location of the
shear walls have been shown in the Figure 3.4.2.
Figure 3.4.1: A four story building that’s been rehabilitated in Dinar (Sucuoglu et al.
2004)
56
The building was a reinforced concrete frame with concrete slabs and individual footings
connected by foundation tie beams in both directions. The typical floor area is 310 m2
and the floor height is 3.80 m for the ground floor and 3.50 m for all floors above the
ground floor. The most common size of column cross section is 25 cm by 60 cm and all
the beams are 25 cm by 70 cm. There is a 1m cantilever on the front and back of the
building starting from the first floor. There are fewer walls in the ground floor and that
created a weakness.
During the 1 October 1995 Dinar earthquake, all of the 23 columns had been damaged in
the ground floor, two of the columns had been severely damaged with shear failure on
both ends, three were damaged moderately and rest 18 columns were damaged lightly. In
the ground floor all the brick partitions were heavily damaged. In the first floor out of 37
columns two columns were damaged severely and three columns were damaged
moderately and one was damaged lightly. There is visible damage in the brick partitions
even in the upper floors. There was not much damage for the beams, clearly showing that
beams were stronger that the columns. The transverse reinforcement provided in the
columns and beams had a spacing of 20-25cm. The concrete core samples that have been
taken from the building revealed a mean concrete strength of 12 MPa (Sucuoglu et al.
2004).
57
Figure 3.4.2: The Rehabilitated scheme of the four stories structure in Dinar, ground
floor plan (Sucuoglu et al. 2004)
In the rehabilitation process of this building two U-shaped shear walls were added to the
building as shown in the Figure 3.4.2 and the corner columns were strengthened. Column
6C was severely damaged. Since this column was to remain in one of the shear walls,
concrete was completely removed from this column and has been recast along with the
shear wall. Column 6B was also damaged severely. This column was jacketed with a
concrete cover. The shear wall ration in the rehabilitated building in the x and y
directions is 0.0021 and 0.0032 respectively.
3.4.4 Eight Story Building in Ceyhan
This building (Figure 3.4.3) has been damaged moderately in the June 25, 1998 Adana-
Ceyhan earthquake. Damage was mainly observed in beams in the first five levels,
columns and the U shaped shear wall around the elevator in the first floor. As a part of
the rehabilitation process shear walls were added to the structure as shown in the Figure
58
3.4.4. The areas denoted with darker shaded regions are the newly added shear walls
(Sucuoglu et al. 2004).
The structural system of the existing structure was almost symmetrical in the long
direction. This structure had a two way continuous footing at a depth of 1m from the
ground. The beam sizes were 20 mm by 60 mm and the thickness of the concrete slab is
14 cm. The column sizes are 25 mm x 50 mm and 25 mm x 70 mm. The floor area of the
ground floor is 195 m2 and the floor area of the floors above it is 227 m2. The floor height
all through the building is 3 m for all the floors.
Figure 3.4.3: Eight story damaged building in Ceyhan (Sucuoglu et al. 2004) During the Adana-Ceyhan earthquake four of the 24 columns in the first floor in this
building were lightly damaged and the other columns are not damaged. Out of the three
existing concrete wall segments two were lightly damaged and one is moderately
damaged. Most of the 55 beams and 36 infill walls in the ground floor of the structure
were moderately damaged. Similar beam and infill wall damages patters were observed
in the upper floors all the way to the fifth floor.
59
Majority of the connections satisfied a strong column weak beam failure. The
longitudinal reinforcement of the columns was between 1 - 2%. The transverse
reinforcement provided in the column had a spacing of 20mm. All the beams in the
structure were reinforced lightly. A favorable beam mechanism was observed by
considering the beam damage distribution over the five stories, but the infill wall
damages was an indication of the lack of lateral stiffness and strength. The core concrete
samples were collected from walls and beams showed a mean concrete strength of 14
MPa (Sucuoglu et al. 2004).
During the seismic rehabilitation of the structure four infill shear walls were added to the
structure as shown in the Figure 3.4.4. The wall ratio was increased to 0.0020 in the x
direction and 0.0027 in the y direction.
Figure 3.4.4: Rehabilitation scheme of the eight stories building in Ceyhan, ground floor plan (Sucuoglu et al. 2004) 3.4.5 Aftershock Test in Dinar
A magnitude 4.6 after shock occurred on 4 April, 1998 on the Dinar fault. Since all the
rehabilitation work on 35 buildings is completed, this after shock has been considered as
60
a live performance evaluation for the rehabilitated building for seismic forces. The effects
of this after shock is considerably minimal on the 35 rehabilitated buildings. This after
shock caused hairline cracks at the infill walls and existing structure interface. Some of
the buildings also showed hairline cracking of masonry infill wall. The four story
building that has been discussed showed minor shear cracking on the masonry piers
between the windows of the second story which snapped the cantilevering facade. Hair
line cracks at the roots of the first floor beams connecting to the shear walls are observed
(Sucuoglu et al. 2004).
3.5 PASSIVE SEISMIC PROTECTION IN STRUCTURAL REHABILITATION
Passive seismic protection system is commonly referred as a seismic protection system.
A set of devices, through their action increases the seismic capacity of the structure.
These systems will reduce the lateral deformation by modify the dynamic global behavior
of the structure or by increasing the energy dissipations capacity of the assemblies, there
by reducing the forces and deformations (Guerreiro et al. 2006).
There are three types of passive seismic protection systems
1. Passive seismic protection systems
2. Active seismic protections systems
3. Semi-Active seismic protection system
The main difference is that passive seismic protection systems do not need any energy
supply for their normal behavior. Active and Semi-Active seismic protection devices
need energy supply for their normal behavior. Base isolator or the use of energy
dissipation devices are the most important passive seismic protection systems. These
technologies are currently used in seismic rehabilitation of old structures as well as in
new structures (Guerreiro et al. 2006).
Traditional seismic rehabilitation techniques try to improve the capacity of the structure
to resist lateral loads by adding reinforced concrete shear walls or rigid frame structures.
The modification of the global stiffness of the structure, in most cases, increases the
61
natural frequency thereby increasing the seismic demand. In order to avoid this situation
it is important to rehabilitate the structure with out increasing the seismic demand. The
use of base isolator is an effective method of improving the seismic resistance of the
structure without increasing the seismic demand of the structure.
3.5.1 Base Isolation
Base isolator decouples the base horizontal movement from the horizontal movement of
the structure. This is obtained by introducing a horizontal layer with high horizontal
flexibility between the super structure and the foundation. By reducing the horizontal
stiffness of the structure the fundamental frequency of the structure has been reduced to a
lower level compared to a fixed base system. By using a base isolation system we are
reducing the fundamental frequency of the structure there by reducing the seismic force
demand of the super-structure. Since the isolation system has a high horizontal flexibility
the deformations will be large and care should be taken to accommodate high
deformations. Deformations are concentrated at the isolation level, where the base
isolation system is located and is designed to absorb them. The use of base isolators has
two advantages. It reduces the inter story drift and the floor acceleration (Guerreiro et al.
2006).
The base isolation can be achieved by introducing a special device at the isolation level,
creating the flexible layer of decoupling. The isolators must have low horizontal stiffness,
capacity to support vertical forces, horizontal restoring force to re-centre the structure
after the motion, capacity to dissipate energy.
The following are the most common base isolation systems
1) High-damping rubber bearings (HDBR)
2) Lead rubber bearings (LRB)
3) Friction pendulum systems (FPS)
62
Figure 3.5.1: Different types of base-isolation systems (Guerreiro et al. 2006)
Figure 3.5.2: Example of retro-fitting a RC building with base isolation (Guerreiro et al.
2006)
The major advantage of base isolation technique is that the seismic demand of the
structure can be reduced to the same magnitude as the available capacity of the original
structure, even when the available capacity of the structure is rather low. This can be
achieved by lowering the natural frequency and effectively maintaining the energy
dissipation. By implementing this technique the horizontal forces on the structure are
significantly reduced compared to rigid base structure there by reducing the retrofitting
requirement. Base isolation is a modern technique which can be predominantly used in
retrofitting monumental structures because base isolation method does not intervene with
the super structure and has very little effect on the architectural characteristics of the
building. The Oakland City Hall (Figure 3.5.3) and the San Francisco City Hall are some
of the buildings rehabilitated with this method.
63
Figure 3.5.3: Los Angeles City Hall rehabilitated with base isolators (Guerreiro et al.
2006)
3.5.2 Energy Dissipation Devices
The seismic vulnerability of the structure can be effectively reduced by the use of seismic
energy dissipation devices. The use of seismic energy dissipation method increases the
capacity to dissipate energy that has been transmitted to the structure by the ground
moment thereby reducing the seismic effect on the structure. If the system is not
equipped with any energy dissipation devices, energy has to be absorbed by deformation,
elastic or inelastic, of the structural elements. When the structural elements capacity is
not sufficient to accommodate the deformation demand, this can cause fail of the
structural element. By using energy dissipation devices the amount of energy that has to
be absorbed by the structural elements can be reduced by effectively dissipating the
energy. With energy dissipaters, the amount of energy that must be absorbed by the
structure can be controlled and the damage can be limited (Guerreiro et al. 2006).
64
The energy dissipation devices are devices precisely designed to dissipate large amount
of energy without deterioration, and can be distributed in three major classes: viscous
dampers, hysteretic dampers and viscoelastic devices. The hysteretic devices behavior is
based on the plastic deformation capacity of metallic elements, usually steel elements. In
these systems the force depends on the deformation and the control parameters are the
initial stiffness, the yield level and the stiffness after yielding (Guerreiro et al. 2006).
Even if the structure is fitted with energy dissipation devices, these dampers do not
provide any resisting force and the structure has to resist all the lateral loads. A typical
fluid viscous damper has a central piston that strokes though a viscous fluid filled
chamber. The fluid moves through the orifices in the piston head and dissipates energy
and also creates a force that resists the motion of the damper. To ensure proper fluid
performance and stability, silicon-based fluids are used.
A typical arrangement of a viscoelastic damper consists of viscoelastic layers bonded
with steel plates as shown in Figure 3.5.3. A frame structure is needed to install a energy
dissipation device on a structure. So this method is applicable to steel frame structures
and reinforcement concrete moment resisting frames (Guerreiro et al. 2006).
Figure 3.5.4: Arrangement of a viscoelastic damper (Guerreiro et al. 2006)
65
Chapter 4
REHABILITAION FOR BLAST
Most of the buildings are designed without considering blast loading, in wake of the
unexpected events, like recent terrorist attacks, design for blast loading is gaining gradual
attention in the structural community. This chapter summarizes some of the methods that
are currently in use in blast resistant design.
4.1 POLYMER RETROFIT OF UNREINFORCED MASONRY WALLS
Strengthening the unreinforced, non-load bearing concrete partition walls is one of the
primary focuses in the recent years due to the following reasons
1) the frequent use of unreinforced concrete masonry partition walls in building that
generally have high occupancy
2) The susceptibility of these components to fragmentation even in case of a low
blast pressure.
There are several methods to strengthen the unreinforced concrete masonry walls. Some
of the retrofit material includes carbon fiber laminates, aramid composite fibers, etc.
These methods have demonstrated the ability to increase the strength and ductility of
unreinforced concrete masonry to a large extent, but feasibility of wide spread application
of these products is challenged by the development cost, methods of applying these to the
structure. Connell (2000) conducted three full scale tests to determine the effectiveness of
polymers for retrofitting structures for blast loading.
To over come constrains of the above materials experiments were conducted using spray
on polymers. Three full scale experiments were conducted to determine the potential of
these materials in improving the blast resistance of the unreinforced concrete masonry
walls. These tests were conducted to determine the electrometric polymer application
process, measure the deflections at critical wall locations, measure the internal and
66
external pressure created by the blast, failure modes and determine the effectiveness and
the level of protection by the electrometric polymer retrofit (Davidson et al. 2004).
In each of these tests several wall panels were tested for blast loading. Some of these
were coated with polymer and while others were not, to evaluate the effectiveness of the
polymers. The wall samples were tested in reusable reaction structures designed to
withstand blast loads. Blast loads were then applied to the panels by detonating explosive
charges from a stand off distance. Instruments were fitted in the structure to measure the
displacements, acceleration and pressure.
4.1.1 Selection of Retrofit Material
In the initial stages, 21 prospective retrofit materials were considered. Seven of the
materials were extruded thermoplastic sheet materials, 13 were spray on polymers and
one was a brush on material. All of the prospective polymers possessed temperature and
ultraviolet stability, flame resistant and were cost effective. To determine the structural
properties of all the polymers MTS load frame tests were conducted at a loading rate of
8.38 mm/s. 4.1. 1 shows the average of the results obtained in the tests for all the groups
(Knox et al. 2000).
Table 4.1.1: Average tensile strength properties obtained from the tests (Davidson et al.
2004)
Application (number of polymers tested)
Secant modulus of elasticity
Elongation at rupture (%)
Maximum tensile strength
Extrusion (7) 113,000 kPa (164,000 psi)
52 55,800 kPa (8,100 psi)
Spray-on (13) 78,500 kPa (11,400 psi)
109 9,650 kPa (1,400 psi)
Brush-on (1) 6,890 kPa (1,000 psi)
25 5,510 kPa (800 psi)
The extrusion polymers were stiffer and stronger than the other groups, but envision
retrofit approach of creating protective shells with in the occupied space made extrusion a
difficult choice to implement. Hence the extrusion thermoplastic polymers are eliminated.
67
The brush on polymers were observed to be very weak, brittle and had very long cure
times, hence these are eliminated (Knox et al. 2000).
Spray-on Polyurea was select for the retrofit due to its strength, flammability and cost.
These polymers have many applications ranging from marine application to forming the
lining of food and storage tanks. Material test were conducted on the selected polymer
and the results from the tests are shown in Tables 4.1.2 and 4.1.3.
Table 4.1.2: Properties of Polyurea (Davidson et al. 2004)
Property Measured Value Modulus of Elasticity 234,000 kPa (initial); 165,000 kPa (secant)
[ 34,000 psi (initial); 24,000 psi (secant)] Elongation at rupture 89% Stress at rupture 13,900 kPa( 2,011 psi) Maximum Tensile Strength 14,000 kPa ( 2,039 psi) Toxicity (according to the manufacturer) Non toxic after curing Flame Test (ASTM D635) ATB=infinite, AEB= 19 mm
Table 4.1.3: Material properties obtained for the tests (Davidson et al. 2004)
Sample Maximum Tensile Strength
Elongation at maximum tensile strength
Maximum Elongation (%)
Secant Modulus
Toughness
Polyurea-A 12,700 kPa ( 1,840 psi)
46.4 53.6 180,000 kPa ( 26,100 psi)
5,830 (kPa.X mm/mm) 846 (psi x in. /in.)
Polyurea-B 14,100 kPa ( 2,040 psi)
73.7 83.5 167,000 kPa ( 24,200 psi)
10,100 (kPa x mm/mm) 1,159 (psi x in. /in.)
Polyurea-C 13,200 kPa ( 1,920 psi)
88.6 94.4 152,000 kPa ( 22,000 psi)
10,500 (kPa x mm/mm) 1,522 (psi x in. /in.)
MEAN 13,300 kPa ( 1,930 psi)
69.6 77.2 166,000 kPa ( 24,126 psi)
8,790 ( kPa x mm/mm) 1,276 (psi x in. /in.)
68
Figure 4.1.1: Test setup for testing the effectiveness of the spray-on polymer retrofitting
method (Davidson et al. 2004)
4.1.2 Test Procedures
Three tests were conducted to evaluate the effectiveness of the spray on polymer retrofit
technique. In each of the test there was an explosive charge positioned away from a
masonry wall that was built in a highly reinforced concrete structure. Figure 4.1.1
illustrates the test setup. Two masonry walls were constructed inside the reaction
structure. Each of the two walls was 2.24 m x 3.66 m and they are separate by a W12X35
section and 19.1mm foaming on both sides of the wall. These conditions were used to
enforce one way bending. The interior and exterior bottom of each section had been
secured using a 76.2 mm x 102 mm x 6.3 mm (3 in. x 4 in. x ¼ in.) angle and the interior
top had been secured using the same angle and the exterior top had been secured using a
4.88 m x 0.305m x 6.4 m (16 ft x 12 in. x ¼ in.) steel plate.
69
One layer of the spray on polymer had been used on most of the walls on the interior and
on the interior and exterior on one wall in test three. The polymer was overlapped in to
the surrounding reaction structure. “Control walls” without the polymer application have
been provided to act as a measuring gauge for the retrofitted walls (Davidson et al. 2004).
4.1.3 Instrumentation
Pressure, acceleration and deflection experienced by the wall were measured by pressure
gauges, single axis accelerometers and laser deflection gauges. The setup of all the
instruments mounted on the walls is shown in Figure 4.1.2.
Figure 4.1.2: Instrumentation plan (Davidson et al. 2004)
All reflection pressure gauges were mounted in a pipe and were suspended from the top
supported from the reaction structure in front of the wall panels. Accelerometers were
attached to the interior side of the polymer retrofitted walls. Laser deflection meters were
placed at the center of both the walls.
70
4.1.4 Test Results
Test 1 Results
The typical illustration of the reflected pressure obtained from the test 1 is shown in the
Figure 4.1.3. The maximum values of pressure, deflection and acceleration are listed in
the Table 4.1.4. The peak pressure observed in the experiment is 393 kPa. The laser
deflection gauge indicated that both the walls moved inward by 184mm. the control wall
completely collapsed while the wall with the retrofit remained intact (Figure 4.1.4).
Figure 4.1.3: Test 1 reflected pressure: gauge R1 and R2 (Davidson et al. 2004)
Table 4.1.4: Gauge measurements obtained from Test 1 (Davidson et al. 2004)
Gauge ID Type Measured R1 Reflected Pressure/impulse 393 kPa/1,460 kPa ms
(57 psi/212 psi ms) R2 Reflected Pressure/impulse 362 kPa/1,380 kPa ms
(52.5 psi/200 psi ms) R3 Reflected Pressure/impulse 303 kPa/1,120 kPa ms
(44 psi/163 psi ms) F1 Reflected Pressure/impulse 186 kPa/551 kPa ms
(27 psi/80 psi ms) L1 Laser Deflection 184 mm (7.25 in.) L2 Laser Deflection 184 mm (7.25 in.) A1 Accelerometer 379g A2 Accelerometer 379g A3 Accelerometer 444g
71
Figure 4.1.4: View of the damaged walls after test 1 (Davidson et al. 2004)
Test 2 Results
Since the retrofitted wall didn’t collapse in test one. The charge of the explosion was
doubled and the stand off distance was reduced by 14 percent. The instrumental set up is
typically the same as the test1. Due to the increase in the charge and the reduction in the
stand off distance the impact on the wall panel in the test 2 was tripled compared to test1.
The reflection pressures obtained from the test 2 are listed in Table 4.1.5. The values
obtained from laser deflection gauge and the accelerometers were not usable.
Both the control wall and the retrofitted wall panel were destroyed. The control wall
completely disintegrated. The retrofitting polymer held much of the wall together, but the
wall sheared from its supports due to the extreme energy imparted by the blast. As the
wall flexed during the blast the polymer ripped at the height wise center of the wall. The
wall then fell on top of itself in two pieces (Davidson et al. 2004).
72
Table 4.1.5: Gauge measurements obtained from Test 2 (Davidson et al. 2004)
Gauge ID Type Measured
R1 Reflected Pressure/impulse 1,100 kPa / 289 kPa ms
( 159 psi / 419 psi ms)
R2 Reflected Pressure/impulse 1,320 kPa / 1,440 kPa ms
( 192 psi / 209 psi ms)
R3 Reflected Pressure/impulse 1,640 kPa / 2,740 kPa ms
( 238 psi / 398 psi ms)
R4 Reflected Pressure/impulse 1,200 kPa / 2,210 kPa ms
( 174 psi / 321 psi ms)
F1 Free Field Pressure/impulse 455 kPa / 937 kPa ms
( 66 psi / 136 psi ms)
F2 Free Field Pressure/impulse 27.6 kPa / 207 kPa ms
( 4 psi / 30 psi ms)
Test 3 Results
Two additional 3.05 m x 3.05 m (10ft x 10ft) wall panels in cubicles were used in this test
as shown in the Figure 4.1.1. A total of 4 wall panels retrofitted with different schemes
are tested. Four unreinforced concrete masonry walls are housed in the reaction structure
(two wall panels) and cubicles (one wall panel each). The left wall panel of the reaction
structure was retrofitted with 9.5 mm (3/8 in.) layer of polymer and the polymer
overlapped the roof and floor slabs by 0.305 m (12 in.). The right panel in the reaction
structure was retrofitted with 3.2 mm (1/8 in.) polymer layer on both the interior and
exterior faces of the wall with a overlap pf 0.305 m (12 in.). Both the walls in the cubical
were retrofitted with 3.2 mm (1/8 in.) polymer layer on the interior with different
overlaps. One of the cubical was provided with an overlap of 0.152 m (6 in.) and the
other was provided with 0.305 m (12 in.). Each panel is allowed to move freely on the
sides to simulate a one-way flexural response. The explosive charge used was the same as
that used in the test 2. The stand of distance was increase by 30% compared to test 1
(Davidson et al. 2004).
73
The instruments used in this test were five reflected pressure gauges (R1, R2, R3, R4,
R5), one filed pressure gauge (F1) and four laser deflection meters (L1, L2, L3, L4). All
the laser deflection gauges were mounted as described earlier and as shown in Figure
4.1.2. A free-Field pressure gauge (F1) was located at the stand off distance from the
charge as shown in the Figure 4.1.5. Three of the reflected pressure gauges are mounted
on the reaction structure. R2 was fitted in front of the steel section dividing the wall panel
1.83 m (6 ft) off the ground. R1 was fitted at the center of the left panel 1.83 m (6 ft) off
the ground. R3 was fitted at the center of the right wall 1.83 m (6 ft) off the ground. Two
reflected pressure gauges were mounted on the cubicles: on at the center of the left
cubical 1.52 m (5 ft) off the ground and other center of the right cubical 1.52 m (5 ft) off
the ground.
All the wall panels in test 3 sustained severe damage. The polymer retrofit helped to hold
the walls intact and prevented the debris from fragmenting. Figure 4.1.5 show the damage
to the wall panels in the reaction structure. Figure 4.1.6 show the damage sustained by the
wall panels on the cubicles (Davidson et al. 2004).
Figure 4.1.5: Test 3 Result: Wall panels on reaction structure (Davidson et al. 2004)
74
Figure 4.1.6: Test 3 Result: Wall panels on test cubicles (Davidson et al. 2004)
Although the polymer coating was provided on the inside and the outside on one of the
walls in the reaction structure, not sufficient enhancement in protection is provided for
the additional cost. The initiation of tearing on the interior of the wall was shown in
Figure 4.1.8. The reflection pressures obtained from the test 3 are listed in Table 4.1.6.
Table 4.1.6: Gauge measurements obtained from Test 3 (Davidson et al. 2004)
Gauge ID Type Measured R1 Reflected Pressure/impulse 409 kPa / 1,560 kPa ms
( 59.4 psi / 227 psi ms) R2 Reflected Pressure/impulse 479 kPa / 1,830 kPa ms
( 69.5 psi / 266 psi ms) R3 Reflected Pressure/impulse 446 kPa / 1,650 kPa ms
( 64.8 psi / 239 psi ms) R4 Reflected Pressure/impulse 442 kPa / 1,490 kPa ms
( 64.2 psi / 217 psi ms) R5 Reflected Pressure/impulse 476 kPa / 1,500 kPa ms
( 69.1 psi / 218 psi ms) F1 Free Field Pressure/impulse 87.5 kPa / 655 kPa ms
( 12.7 psi / 95 psi ms) L1 Laser Deflection 239 mm (scratch gauge) (9.4 in.) L2 Laser Deflection 198 mm (scratch gauge) (7.8 in.) L3 Laser Deflection 125 mm (scratch gauge) (4.9 in.) L4 Laser Deflection 140 mm (scratch gauge) (5.9 in.)
75
Figure 4.1.7: Tearing of the polymer on the inside from Test 3 (Davidson et al. 2004)
4.1.5 Summary
These tests indicate that spray on polymer technique evaluated here is an effective
method to improve the response of unreinforced concrete masonry walls to blast loading.
Although these tests have shown results that indicate the effectiveness of the tests, the
failure mechanism depends on the peak pressure and duration of the pressure and is not
thoroughly understood. The failure mechanism is also dependent on the support
conditions.
4.2 REHABILITATION OF STRUCTURE AFTER A GAS EXPLOSION
An explosion detonated in a gaseous medium will give rise to a sudden increase in the
pressure in that medium from the ambient pressure to the peak incident pressure of the
explosion. After the explosion a shock wave travels from the blast location at speeds
exceeding the speed of sound. The gas molecules travel at a speed less than the pressure
wave. The pressure and the temperature decreases as the distance is increased. When a
blast occurs inside a building, in a confined space, the hot gases cannot freely mix with
enough cool air. When the pressure wave impacts on a rigid surface, it instantaneously
develops a reflected pressure on the surface which in value is more than the incident
pressure.
76
When the peak incident pressure is between 8.3-6.2 kN/m2, the damage to the building is
minimum up to about 5% of replacement cost and the personnel in the building may be
injured by broken glass and building debris. When the peak incident pressure is
15.8kN/m2, the damage to the building is expected to be about 20% of replacement cost
and the personnel in the building may suffer temporary hearing loss and injury from
secondary blast effect. When the peak incident pressure is 24kN/m2, severe damage to the
building can be expected and the injury to the personnel in the building will be of a
serious nature (1% eardrum rupture). When the peak incident pressure is 55.3 kN/m2, the
building damage approaches total destruction, and the personnel in the building will
sustain serious injury. When the peak incident pressure is 82.7kN/m2, building will
sustain severe structural damage approaching total destruction and personnel in the
building can sustain severe injury or death from direct blast. When the peak incident
pressure is 186kN/m2, the building will be completely destroyed and there will be death
of the personal in the building due to the direct action of the blast (Bob 2004).
4.2.1 Rehabilitation Method
Most buildings are not designed to withstand blast loadings. The rehabilitations scheme
for the deterioration structural member depends on the material.
For RC structures, rehabilitation work is carried when the damage is considerably low
and demolished when the rehabilitation costs are high. Repair is done for surface
deteriorations, cracks, damage resulting from improper casting and reinforcement
corrosion. In RC structures increase in stiffness and ductility is achieved by coating the
beams, columns and joints. These coating agents can be RC jacketing, Steel jacketing,
carbon fibers, etc. In some case it is necessary to transform the existing structure
completely. Some of these techniques are:
1) Adding steel bracing to RC structure
2) Infilling of frame holes with reinforced masonry and reinforced concrete.
In steel structures repair involves working on a damaged structure and restoring its
formal structural efficiency. On the other hand, strengthening involves modifications to
77
the structural elements or the structure as a whole to improve the structural performance
(Bob 2004).
Rehabilitation of structural elements consists of the following:
1) Adding cover plate connection modifications to the lower and/or the upper sides
and adding bolted brackets to the existing welding connections.
2) Gutting, involves removal of internal elements of the structure and adding new
ones with different properties.
3) Adding new structural elements within the original building.
Masonry structures without reinforcements can be rehabilitated by:
1) Erection of RC cores at appropriate distance.
2) Masonry lining with reinforced concrete
3) Interlocking of masonry walls at corners and crossings.
Conventional methods of rehabilitation may lead to inconvenience and the methods prove
to be costly and the improvements achieved after the retrofit is some times are not as
expected. A typical approach to improve the response of an element to blast loading is by
increasing the structural mass, this leads to seismic problems. Carbon fiber reinforcement
plastics (CFRP) provide a solution to this problem. Structural elements designed only for
gravity load and then retrofitted with CFRP, demonstrated ability to withstand negative
loads and also displayed high ductility. This solves the problem by improving the
structural elements resistance and effectively the mass remains unchanged. Crowford (et
al. 2001) demonstrated a full scale testing of CFRP vertical strips and CFRP horizontal
wraps. CFRP vertical strips and CFRP horizontal wraps were designed, applied and
tested with a blast load full scale field test (Bob 2004).
4.2.2 Case Study of a Structure Damaged by Gas Explosion
In early December 2002 an explosion occurred in a flat in the town of Timisoara,
Romania. The building is a 5 story with 100 flats, and the explosion happened in the
second flat on the fourth floor. The explosion occurred due to a leak in a propane gas
78
bottle, the gas accumulated and when the inmates switched on a light in the middle of the
night the gas ignited and caused an explosion. The explosion completely damaged the
concrete walls, concrete floor, windows and doors of the flat. It also caused severe
damage to the other structural members (Bob et al. 2003).
The plan of the building is shown in the Figure 4.2.1. This building is built in 1976 and
the plan dimensions are 43.55 x 14.75 m with a sub-basement and a story height of
2.72m. the building consists of vertical structural member built with longitudinal
reinforcement and transverse reinforcement concrete walls of width 30 cm for concrete
facing the slabs and 15 cm for interior panels. Prefabricated slabs are used in this
structure. The reinforcement of the prefab slabs is 6mm bars at 15 cm c/c over the shorter
span and 6mm bars at 20 cm c/c over the long spam.
Figure 4.2.1: Typical floor plan of the structure (Bob 2004)
4.2.3 Building Damage Assessment
1) The flat directly affected by the blast.
All transverse walls were completely destroyed (Figure 4.2.2)
The concrete facing the slab was moved 55mm from its original position by the
force of the blast (Figure 4.2.3)
Both the bottom and the top slabs showed a maximum deformation of 280-300
mm (Figure 4.2.4).
All the doors and windows were damaged.
79
Figure 4.2.2: View of the damaged transverse walls (Bob 2004)
Figure 4.2.3: View of the damaged floor-wall connection (Bob 2004)
80
Figure 4.2.4: View of the damaged RC floor (Bob 2004)
2) The surrounding structural members affected by the blast
The concrete facing slabs directly above and below the affected flat were moved
from the original position by approximately 10mm.
The Reinforce concrete floor of the neighboring flat had a maximum deflection of
50mm.
The floors and the transverse walls from1st to 5th floors on one side of the
corridor surrounding the site of explosion were damaged by the shock wave (Bob
2004).
4.2.4 Rehabilitation Scheme
The rehabilitation scheme was selected on bases of technical and economical advantages:
Safe behavior under seismic action.
Slight change of general stiffness of the structure.
Short period of rehabilitation.
Low cost of rehabilitation.
81
Figure 4.2.5: strengthening with RC Coating (Bob 2004)
The rehabilitation for this damages structure has been done for the following structural
elements.
1) New concrete floors were added in the levels 3, 4 and 5 with the same geometric
and reinforcement characteristics as of the original members.
2) New reinforced concrete walls at levels 4 and 5 were added with the same width
as of the original members.
3) Local strengthening was carried out by adding a 5cm RC coating on all sides of
columns ( 20x60 cm columns in the corridor and 20x30cm columns in the
facade), longitudinal beams at all levels and vertical elements from ground to the
roof on each side of the corridor (Figure 4.2.5).
4) CFRP (sika wrap) was used to rehabilitate 10 damage transverse walls and 12
damaged floors (Figures 4.2.6, 4.2.7, and 4.2.8) (Bob 2004).
82
Figure 4.2.6: strengthening of walls with CFRP (Bob 2004)
Figure 4.2.7: Installation of CFRP to strengthen floors (Bob 2004)
83
Figure 4.2.8: Strengthening of floors with CFRP (Bob 2004)
These modifications were chosen in accordance with the condition of the building.
Instead of removing the severely damaged structural member new members were added
to the structure. The coating on the columns was necessary since the columns were
severely damage and this ensures connectivity and stability of the vertical members. The
use of CFRP to strengthen the slightly damages members of the structure made it easy to
install and a short time of erection. The rehabilitation scheme followed is shown in the
plan view in Figure 4.2.9 and 4.2.10. The strengthening of the floor by CFRP was shown
in the Figure 4.2.11 (Bob 2004).
84
Figure 4.2.9: Strengthening with RC sheets, columns and longitudinal beams (Bob 2004)
Figure 4.2.10: Local strengthening of columns and beams with RC jacketing (Bob 2004)
85
Figure 4.2.11: Strengthening of floors with CFRP (sika wrap) (Bob 2004)
4.2.5 Summary
The Damage to the structural members in the building is dependant on the position, the
members that are in direct contact with blast were completely damaged and the ones near
by are slightly damaged. This strengthening solution has been considered to obtain
technical and economical advantages.
4.3 BLAST RESISTANT DESIGN OF COMMERCIAL BUILDINGS
There are numerous commercial office and retail buildings throughout the United States
that are vulnerable to terrorist attack. Here we are examining a prototypical commercial
office building and examining the deficiencies and vulnerabilities of the system for blast
loading and recommending modifications that improve the performance of the building
against blast loading.
86
The building chosen for this study is a cast-in-place reinforced concrete eight story
structure. Though this is a very commonly found structure, it has very high vulnerability
for blast loadings. Therefore, this structure was chosen to identify the vulnerabilities and
improve it for blast loads (Ettouney et al. 1996).
The eight story structure considered in this study is show in the Figure 4.1.1. The
structural system of all the eight stories and the slab is typical of reinforced concrete flat-
slab construction. The columns, slabs and beams all are cast-in-place concrete. In this
structure columns are spaced 9 m center to center and the typical floor height is 3.9 m and
the first floor height is 6 m. Spandrel beams are provide on the out side edge of the
building to support the facade. The lateral loads are resisted by the shear wall around the
elevator chambers. This building has been designed to resist wind loads and seismic loads
(Ettouney et al. 1996). The seismic load specification confirm to the uniform building
code (UBC 1991). This building occupies a complete city block and has public access on
all four sides with a surface parking lot at the rear of the building. There is also a loading
dock at the rear of the building. One of the distinctive features of this office building is a
two story atrium in the front of the building, faced with exterior glass on the perimeter
and with open in the interior. The perimeter of the atrium is ringed by a spandrel beam
that supports the outer edge of the slab. Above the atrium, the column spacing of 9m
center to center is restored by the transfer girder (Ettouney et al. 1996).
Figure 4.3.1: Elevation view of the building (Ettouney et al. 1996)
87
Figure 4.3.2: Plan view of the building (Ettouney et al. 1996)
Figure 4.3.3: Isometric view of the building (Ettouney et al. 1996)
88
4.3.1 External Treatment
The most important factors that influence the blast environment are
1) Stand off distance (The distance of the charge from the object).
2) Bomb’s charge weight
Since the charge of the bomb can not be controlled, the only factor anyone can control is
the standoff distance. Irrespective of the charge of the bomb maximum possible stand off
distance must be provided around the entire perimeter of the building in every case so as
to reduce the effect of the explosion. The main factor stand off distance depends is the
site selection.
For the building under consideration the only area that can be controlled is the side walk
around the building to limit the stand off distance. Since there is not much stand off
distance this building is highly vulnerable to hand thrown bombs and car bombs. The
most directly effected structural members are the columns beams and the atrium in the
first floor and the facade. Since these members are highly vulnerable special attention is
required (Ettouney et al. 1996).
4.3.1.1 Stand off Distance
Maximum stand off distance, within which explosive laden vehicles may not penetrate,
must be provided and guaranteed. As we all know greater the stand off distance greater is
the dissipation and the building experiences lower pressure and impulse. Following are
the recommendations that can increase and improve the effectiveness of the stand off:
1) Use anti-ram bollards or large planters, placed all around the building. The
bollards must be design to resist very impact loads. While designing the bollards
care must be taken on the maximum speed that a vehicle can attain, site
conditions govern the maximum speed that can be attained by a vehicle. And
while designing the connections for the bollards, these must be designed for the
maximum impact load that can be applied on the bollards. When there are design
restrictions on the bollard connection design care must be taken to reduce the
maximum speed attained by applying field modification.
89
2) The public parking lot at the back of the building is a vulnerable point to plant a
car bomb. So, this parking lot must be secured and all the vehicles that enter the
parking lot must be cleared, i.e. employee vehicles or vehicles visually examined.
If possible parking must be eliminated on the near side of the parking lot.
3) Street parking typically on the near side of the building has to be eliminated. This
reduces the chances of parked car bomb. Normally, the city gets high revenue
from street parking, so the owner of the building has to pay for the loss of
revenue.
4) Additional stand off distance can be attained by removing one lane of traffic
around the building and using this space as a walkway. This has to be approved
by the city officials and could also cause traffic problems.
5) An additional measure to improve the effectiveness of the stand off distance is to
remove the street parking on the other side of the road. Even though this will not
improve the stand off distance, this will decrease the chances of parked car
bombs. This will not reduce the chances of “park and run”, drive-by and suicide
bombs. Unfortunately, in the case of the Oklahoma City bombing, a truck laden
with explosives is parked for approximately for 2 minutes and still it dint grab the
security officer’s attention.
It must be understood that increasing the stand off distance is very effective in case of a
small charge. When the bomb has a very high charge, an increase in stand off by 9 or feet
will not be enough, the blast forces may overwhelm the structure even after the increase
(Ettouney et al. 1996).
4.3.1.2 Lower Floor Exterior
The architectural design of the building used glass facade on all sides of the building.
Unless this has been replaced with reinforced concrete walls, the lower level structural
member and their connections will suffer heavy damage. This will also cause severe
damage to inhabitants of lower floors. In general three cases of charges and the corrective
action are discussed below:
90
1) To protect against a small charge, a 300mm thick wall with 0.3% steel double
reinforcement in both direction is required.
2) To protect against a intermediate size charge, a 500mm thick wall with 0.5%
reinforcement in both direction is required.
3) In case a large charge, the blast will breach any reasonable sized wall and damage
the lower floor structural members. So protect against a large charge, precautions
must be taken and adjustments must be made for the whole structure (Ettouney et
al. 1996).
4.3.2 Glazing
Glazing is the first weak link when blast loading is considered. For any reasonably sized
bomb, all the glazing will shatter especially on the side facing the bomb. Commonly used
annealed glass behaves very poorly when loaded drastically. The failure mode for the
annealed glass will create large sharp objects resembling knifes and shatter them all
around inside the structure and cause heavy injuries and causalities. It has been observed
in the previous blasts that glass shattered will cause heavy damage and that is one of the
important factors.
While typically annealed glass can only withstand 14KPa (9psi) of blast load there are
other alternative glazing materials which can resist a greater amount of blast load and can
perform better in some case of the blast loadings. Thermally Tampered Glass (TTS) and
Polycarbonate lay-ups can be made in to sheets of one inch thick and can withstand
higher blast loads than the annealed glass. Unlike annealed glass, TTS normally breaks in
to rock-slat sized pieces and infringe less injury to the inmates. TTS can normally
withstand 200 – 275 KPa (30 – 40psi). TTS is used in the side and rear windows of the
automotives. Failed Polycarbonate lay-ups remains in one large piece and will also cause
heavy damage to the inmates same like annealed glass. Polycarbonate lay-ups is normally
used in the windshields of cars. Care must be taken when design of the glass is carried.
While designing the connectors for the design of glass, the connectors must be designed
in such fashion that full strength of the glass has been achieved before any failure of the
91
connectors. If the connectors fail before the glass, the glass as a whole will fly and
infringe heavy damage (Ettouney et al. 1996).
4.3.3 Facade and Atrium
As the exterior of the building is the first defense against blast loading, how the facade
responds to blast loading is an important factor. The facade consists of the glazing and
the exterior walls. Realistically glazing is pressure sensitive and is the first building
component that will fail in presence of blast loading. Although there are methods to
strengthen the exterior walls, the number of methods available to strengthen glass and
windows are limited. Windows will break during the blast and the pressure wave will
enter the building. There is direct correlation between the degree of fenestration and the
amount of blast that is allowed to enter the occupied space. Limiting the amount of
fenestration will also limit the blast effects. Atriums are common on prestigious office
buildings. These atriums will provide the buildings with a grand look and also allow the
natural light to enter the lobby area. And also provide excellent functioning spaces and
balcony elevator lobby. Atriums are inviting target for the reason that, the damaged glaze
will expose all the structural elements and this may cause a lot of damage to the structural
system. The building under consideration has a big window at the entrance, this window
cannot be strengthened to withstand the blast loadings, so the shattered fragments from
this window and the glaze will cause a potential hazard to the inmates and this will also
allow the pressure wave to enter the structure (Ettouney et al. 1996).
4.3.3.1 Exterior of the Atrium
The exterior of the atrium is very important. The window provided at the entrance and the
glazing must be strengthened to resist small charges so as to protect inmates or the
exterior glazing can be replaced with reinforced concrete walls and protect the structural
system from moderate-sized charge (Ettouney et al. 1996).
4.3.3.2 Interior of Atrium
Almost all blast will generate a pressure greater that 14 KPa (2psi) on the external facade
of the structure destroying the glazing and letting the blast wave enter the building. The
92
blast wave will dissipate energy both with distance and reflection off of the internal
surfaces. Depending on the charge there will be a height where the blast wave intensity
has been reduced to 70 – 100 KPa (10-15psi), a magnitude where human fatality is not
likely. At this elevation the blast wave that enters the structure thought the shattered glass
will reduce sufficiently to pose a reduced threat to the occupants. In case of a moderate
sized charge explosion outside the glass facade will cause a extensively high blast wave
intensity of 200 KPa (30psi) over the entire height of the building. The shock wave
entering the structure will damage the partition walls and pose danger to the occupants.
The only way to protect the structural elements is by strengthening the balcony parapet,
spandrel beams and exposed slabs to resist blast loads.
4.3.4 Floor Slabs
When the structure is subjected to blast loads, the flat slab construction is subjected to
large dynamic pressure load. The softening of the moment resisting capacity of the slabs
will reduce the lateral-load-resisting capacity of the system. When the moment carrying
capacity of the slabs at the columns is lost the ability to transfer the loads to the shear
walls is also reduced and this will weaken the structure severely (Ettouney et al. 1996).
These are some of the possible modes of failure:
Figure 4.3.4: Failure mechanism of the flat slab (Ettouney et al. 1996)
93
Figure 4.3.5: Effects of blast loading on columns (Ettouney et al. 1996)
Figure 4.3.6: Lateral load carrying mechanism and effects after the blast (Ettouney et al.
1996)
1) The slab by itself can undergo localized failure as shown in Figure 4.3.4.
2) The loss of the connection between the columns and the slabs will increase the
unsupported length of the column and may lead to the buckling of the column.
This has been depicted in the Figure 4.3.5.
3) The lateral load carrying system consists of the columns, shear walls and the slab
that transfers the lateral loads. This system can be damaged to such an extent that
the structure as a whole is unstable for lateral loads. This has been depicted in the
Figure 4.3.6.
94
Figure 4.3.7: High and Low vulnerability locations (Ettouney et al. 1996)
Figure 4.3.8: Flat slab improvements (Ettouney et al. 1996)
To avoid such calamities, following improvements must be considered.
1) More attention must be taken while designing the exterior bays and lower floors
which are very vulnerable to blast loads. The graphical representation of this is
shown in the Figure 4.3.7.
2) Spandrel beam which are not mandatory in the structure must be provided and
tied together to improve the response of he slab edges.
3) In exterior bay and lower floors, column heads and drop panels must be used to
enhance the punching shear resistance as shown in the Figure 4.3.8.
95
4) If vertical clearance is a problem, shear heads embedded in the slab will improve
the shear capacity and also improve the transfer of the moments from the slab to
the column.
5) The ductility demands and the shear capacity to resist multiple load reversals
make it a ideal place to provide a beam to span over the critical sections of the
slab.
6) Bottom reinforcement must be provided continuously through the column, this
prevents brittle failure (Ettouney et al. 1996).
The slab must be designed for punching shear as a collapse of the slab may cause a
progressive collapse. Hawkins and Mitchell (1979) showed that a punching shear failure
in an internal column is more likely to cause a progressive collapse than a damaged
external column due to a car bomb.
4.3.5 Columns
For typical building columns are designed for gravity loads and no special consideration
is taken to design for blast loading. In case of blast loading the column has to be design to
withstand large lateral deformations and have high ductility. Incase of blast loading
depending upon the distance of the charge, the characteristics of the loading of the
column can be summarized in to two different scenarios:
1) A building located at a distance more than the perimeter proximity of 30m from
the charge will experience a low pressure uniform distributed all over the facade.
2) Building that are situated less than 30m from the curb are more prone to be be
exposed to more localized, high intensity blast loads.
Most of the columns that are designed for gravity loads must be taken in to consideration
for improvements to resist blast loads. As shown in the Figure 4.3.9, when an external
column is subjected to blast loading, it experiences high blast pressure. This blast
pressure will result in heavy bending of the column in addition to the axial load of the
column. To withstand the axial load and the lateral deformation due to the blast load, the
column has to be designed with sufficient ductility (Ettouney et al. 1996).
96
Figure 4.3.9: Direct Lateral loading of column (Ettouney et al. 1996)
Figure 4.3.10: Uplifting on the columns (Ettouney et al. 1996)
97
The blast pressure that enters the building through the shattered windows and openings,
will load the underside of the slab and then the upper side, with some time delay. This
time delay in loading the slab may some times cause a net upward force on the slab and
the difference in the pressure on both sides of the slab, May also creates an upward force.
So the slabs must be designed to resist loads opposing gravity. When there is an upward
force on the slabs, even the column may sometimes experience a net tensile force (fig10).
The conventional columns on the building under consideration are not designed for
combined effect of bending and tension and therefore may be prone to damage (Ettouney
et al. 1996).
These are some of the recommendations that improve response of the columns for blast
loading.
1) The potential direct lateral load and the impact from the blast debris on the lower
level column make it important for these columns to have high ductility and
strength.
2) The lower level perimeter columns must be designed to resist high lateral loading
that can be caused due to a blast, as show in the Figure 4.3.9.
3) The column ductility and the strength can be improved by encasing the column in
a steel jacket. This also improves the concrete confinement.
4) The possibility of uplift in the columns has to be considered and if deemed likely,
measures must be taken to design the column for a transient tensile force.
5) For smaller charges, spiral reinforcement in the columns will improve the
confinement of the columns and improve the ductility and strength of the column
to resist the blast.
98
Figure 4.3.11: Progressive collapse mechanism (Ettouney et al. 1996)
4.3.6 Transfer Girders
Transfer girder transfers the load for the columns above the atrium to the adjacent
columns out side the atrium. Transfer girder spans the width of the atrium; this allows a
column free architecture for the atrium. All building with transfer girder must be treated
with care when blast loading is considered. A blast load that adversely affects the transfer
girder may trigger a progressive collapse and destroy the whole structure (Figure 4.3.11).
The column connections must support the transfer girder even after in elastic deformation
(Ettouney et al. 1996).
The following recommendation will improve the blast resistance of the transfer girder.
1) Adequate detailing must be used while designing the column connections for blast
loading.
2) If the blast loading exceeds the girder capacity, a progressive collapse analysis
must be preformed.
99
Chapter 5
CONCLUSIONS AND RECOMMENDATIONS
5.1 CONCLUSIONS
In summary the following conclusions are drawn from the study.
Wrapping a Beam-Column joint with GFRP will enhance the response of the joint
to seismic loading and transform the brittle behavior to a more ductile behavior.
High strength concrete columns when confined by a stay-in-place FRP
confinement can develop ductile behavior under simulated seismic loads.
The increased confinement requirement of the high strength concrete columns can
be met with the use of FRP stay-in-place confinement. Unlike the discrete nature
of the conventional reinforcement, FRP confinement provides continuous
confinement, covering the whole column face, thus providing better confinement
efficiency.
RC jacketing of columns has many advantages. This method improves the
stiffness of the column uniformly all through the column length. Sand blasting is
an effective technique for interface surface preparation.
Adding shear walls to a structure will effectively increase the lateral stiffness of
the structure and act as the primary lateral load carrying system thereby protecting
the old structural frame from seismic loading. Adding shear walls to a structure
will reduce the undesirably large lateral deflections.
The use of base isolation system will effectively retain the architectural beauty of
old buildings and enhance the response of these building to earthquake loadings.
This is the most suitable method for historical buildings were the architectural
aspects of the building can not be modified.
Providing maximum stand off distance is the best possible solution for protecting
a structure from the effect of blast.
The spray-on polymer approach to strengthen unreinforced masonry wall for blast
loading is quite effective. The peak pressure that the wall can withstand increases
100
many times after the application of the polymer. The polymer layer also helps in
preventing fragmentation of the wall.
The use of Thermally Tempered Glass (TTS) and Polycarbonate lay-ups in place
of annealed glass is a preferred option to prevent shattering of glass after blast and
thus protect the occupants from serious injuries. A summary of various rehabilitation techniques for resisting earthquake and blast loading
are provided in Tables 5.1.1 and 5.1.2. Table 5.1.1: Rehabilitation Techniques for Resisting Earthquake Loading
Technique Comment
FRP wrapping of beam-
column joints
Wrapping beam column joints with FRP laminates
increases the ductile behavior of the joint and the
resistance to earthquake loading.
FRP stay-in-place
confinement for HSC columns
High strength concrete is generally brittle. So the
confinement requirements are very high. Using
conventional confinements with high strength concrete
will create cage congestion. This can be avoided by
providing FRP stay-in-place confinement.
RC-jacketing of concrete
columns
By RC jacketing of concrete columns, significant
increase in strength and ductility of the column can be
achieved. This method improves the stiffness of the
column uniformly all through the length of the column.
Shear walls Shear walls are added to the structure in order to
increase the lateral stiffness of the structure. Soft story
failure is observed in structures with low lateral stiffness
in the lower floors. This can be avoided by adding shear
walls in the lower floors.
Bracing Similar to shear walls bracings also increase the lateral
stiffness of the structure. By adding bracings the lateral
deformation in the event of an earthquake can be
reduced effectively.
101
FRP laminates for walls Ductility of the wall panels can be improved by adding
FRP laminates. This will increase the lateral stiffness
and minimize the deformations.
Base isolators
Base isolators decouple the horizontal movement of the
base from the horizontal movement of the
superstructure. This is an expensive method, but is
useful to maintain the architectural integrity of historical
structures.
Energy dissipation devices Energy dissipation devices are installed in the structure
to effectively dissipate the energy transmitted to the
structure and reduce its deformation.
Table 5.1.2: Rehabilitation Techniques for Resisting Blast Loading
Technique Comment
Increasing stand-off distance Most effective technique but large stand-off distance
may not always be possible for effective functioning of
the building (e.g., building in downtown of a crowded
city, hospitals, etc.)
Spray-on polymer This technique is useful in improving the ductility of the
structural elements. This method is suitable for
unreinforced masonry walls. This helps in preventing
complete shattering of the wall. The peak incident
pressure that the wall can resist can be improved by this
method.
Use of Thermally Tampered
Glass (TTS) or Polycarbonate
lay-ups for glazing
Annealed glass that is typically used for glazing has
brittle nature and can not withstand blasting loading.
Thermally Tampered Glass (TTS) or Polycarbonate lay-
ups can be made into sheets of one inch thick and can
withstand higher blast loads.
Steel jacketing of columns Lower floor columns experience heavy lateral forces
during a blast. So the ductility of the columns has to be
102
increased to improve the column resistance to blast
loading. Jacketing of columns increases the ductility and
strength of the columns.
FRP laminates for walls In this method FRP laminates are attached to the walls,
which increase their ductility. The walls can then
withstand higher peak pressures without fragmentation.
5.2 RECOMMENDATIONS
All the methods discussed in this report have advantages and disadvantages, and some
have applicability limitations. The adaptation of a particular method is also dependent on
economic consideration. Hence a detailed economic comparison between applicable
methods is necessary before rehabilitating a given structure.
The feasibility of using nondestructive evaluation methods to monitor and asses the
condition of the FRP composite bonded to the structure should be considered.
Finite element models should be used to simulate the blast conditions and asses the
structural behavior, thereby facilitating the understating of the fracture mechanism.
A combination of two or more of the aforementioned rehabilitation techniques can be
implemented for more effective energy dissipation and hence obtaining a more ductile
behavior.
103
REFERENCES Abramovitz, J. N. (2001). Unnatural Disasters, World Watch Paper, USA.
Alcocer, SM. (1993). “RC frame connections rehabilitated by jacketing,” Journal of Structural Engineering, ASCE, 119(5), 1413–1431. Alcocer, S. & Jirsa, J. (1990). “Assessment of the response of reinforced concrete frame connections redesigned by Jacketing,” Proceedings of the 4th US National Conference on Earthquake Engineering, 3, 295–304. ASCE (1997). Design of Blast Resistant Buildings in Petrolium Facilities, American Society of Civil Engineers, USA. Beres, A., El-Borgi, S., White, R. N. and Gergely, P. (1992). “Experimental results of repaired and retrofitted beam-column joint tests in lightly RC frame building," Technical Report NCEER-92-0025, National Center for Earthquake Engineering Research, State University of New York at Buffalo, NY. Bob, C. (2004). “Evolution and rehabilitation of a building affected by a gas explosion.” Progress in Structural Engineering and Material, 6, 137-146. Bob, C., Jurca, A., Florea, V., Palade, C., and Murarasu, O. (2003). “Effective solution for rehabilitaion of building affected by explosion.” Romania Academy, Timisoara, Romania, 32-41. Booth, E. and Key, D. (2006). Earthquake Design Practice for Buildings, Second Edition, Thomas Telford, USA. Chile earthquake web site (2007). Great Chilian Earthquake, http://en.wikipedia.org/wiki/Great_Chilean_Earthquake (Last accessed 2007) Chopra, A. K. (2005). Dynamics of Structures, Third Edition, Prentice-Hall International, USA. Connell, J. D. (2002). “Evaluation of electrometric polymers for retrofit of unreinforced masonry walls subjected to blast.” Masters thesis, The University of Alabama at Birmingham, Birmingham, Alabama. Crowford, J. E., Malvar, L. J., Morril, B. K., and Ferrito, J. M. (2001). “Composite retrofits to increase the blast resistance of reinforced concrete building,” Proceedings of the 10th International Symposium on Interaction of the Effects of Munitions with Structures, California, USA, 1-24.
104
Davidson, S. J., Porter, R. J., Dinan, J. R., Hammons, I. M., and Connell, D. J. (2004). “Explosive testing of polymer retrofit masonry walls.” Journal of Performance of Constructed Facilities, ASCE, 18(2), 100-106. Ettouney, M., Smilowitz, R., and Rittenhouse, T. (1996). “Blast resistant design of commercial buildings.” Practice Periodical on Structural Design and Construction, 1(1), 31-39. Explosions web site (2007). Types of Explosions. http://www.fireandsafety.eku.edu/VFRE-99/Theory/Explosions/Explosions.htm (Last access 2007) Ghobarah, A. and Said, A (2001). “Seismic rehabilitation of beam-column joints using FRP laminates,” Journal of Earthquake Engineering, 5(1), 113-129. Guerreiro, L., Craveiro, A. and Branco, M. (2006). “The use of passive protection in structural rehabilitation,” Progress in Structural Engineering and Material, 8, 121-132. Julio, E. S. (2001). “A influencia da interface no comportamento de pilares reforc¸ados por encamisamento de beta˜o armado,” PhD Thesis, Universidade de Coimbra. Julio, E. S., Branco, F. and Silva, V. D. (2003). “Structural rehabilitation of columns with reinforced concrete jacketing,” Progress in Structural Engineering and Material, 5, 29-37. Kashmir earthquake web site (2007). 2005 Kashmir Earthquake, http://en.wikipedia.org/wiki/2005_Kashmir_earthquake (Last accessed 2007) Knox, K. J., Hammons, M. I., T. T., and Porter, J. R. (2000). Polymer Materials for Structural Retrofit, Force Protection Branch, Air Expeditionary Forces Technology Division, Air Force Research Laboratory, Tyndall AFB, Florida. Kuan, S. Y. W. (1991). “Response of epoxy-repaired R/C Exterior beam-column joints," Proceedings of the 1991 Annual Conference of the Canadian Society for Civil Engineers, Vancouver, British Columbia, Canada, 335-344. Mirmiran, A., Shahawy, M., Samaan, M., El Echary, H., Mastrapa, J. C., and Pico, O. (1998). “Effect of column parameters on FRP-confined concrete.” Journal of Composites for Construction, 2(4), 175–185. Mitchell, D., Devall, R. H., Kobayashi, K., Tinawi, R. and Tso, W. K. (1996). “Damage to concrete structures due to the January 17, 1995, Hyogo-ken Nanbu (Kobe) earthquake," Canadian Journal of Civil Engineering, 23, 757-770. Mugurama, H., Nishyiyama, M. and Watanabe, F. (1995). ”Lessons learned from the Kobe earthquake - A Japanese perspective," PCI Journal, a Special Report, 28-42.
105
Northridge earthquake web site (2007). North Ridge Earthquake, http://en.wikipedia.org/wiki/1994_Northridge_Earthquake (Last access 2007) Oklahoma web site (2007). Oklahoma City Bombing, http://en.wikipedia.org/wiki/Oklahoma_City_bombing (Last accessed 2007)
Oklahoma City web site (2007). The Bombing of the Federal Building in Oklahoma City, http://911research.wtc7.net/non911/oklahoma/index.html (Last accessed 2007) Ozbakkalogu, T., and Saatcioglu, M. (2007). "Seismic performance of square high-strength concrete columns in FRP stay-in-place formwork," Journal of Structural Engineering, ASCE, 133(1), 44-56. Pakistan earthquake web site (2007). Disaster pages of Dr. George P. C, http://www.drgeorgepc.com/Earthquake2005Pakistan.html (Last accessed 2007) Pessiki, S., Harries, K. A., Kestner, J. T., Sause, R., and Ricles, J.M. (2001). “Axial behavior of reinforced concrete columns confined with FRP jackets.” Journal of Composites for Construction, 5(4), 237–245. Rodriguez, M. and Park, R. (1994). “Seismic load tests on reinforced concrete columns strengthened by jacketing,” ACI Structural Journal, 91(2), 150–159. Sucuoglu, H., Gur, T. and Gunay, M. S. (2004). “Performance-Based Seismic Rehabilitation of Damaged Reinforced Concrete Buildings,” Journal of Structural Engineering, ASCE, 130(10), 1475-1486. UBC (1991). Uniform Building Code, International Conference of Building Officials, Pasadena, California. WTC web site (2007). World Trade Center 1993 Bombing, http://en.wikipedia.org/wiki/World_Trade_Center_bombing (Last accessed 2007)
106