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TRANSCRIPT
Nwamarah Uche
DEVELOPMENT OF LAYERED ELASTIC ANALYSIS PROCEDURE FOR PREDICTION OF FATIGUE AND RUTTING STRAIN
Digitally Signed by: Content manager’s
DN : CN = Weabmaster’s name
O= University of Nigeria, Nsukka
OU = Innovation Centre
Nwamarah Uche
Faculty of Engineering
Department of Civil Engineering
DEVELOPMENT OF LAYERED ELASTIC ANALYSIS PROCEDURE FOR PREDICTION OF FATIGUE AND RUTTING STRAINS IN
STABILIZED LATERITIC BASE OF LOW VOLUME
EKWULO, EMMANUEL OSILEMMEPG/Ph.D/10/57787
9
: Content manager’s Name
Weabmaster’s name
a, Nsukka
Department of Civil Engineering
DEVELOPMENT OF LAYERED ELASTIC ANALYSIS PROCEDURE FOR IN CEMENT -
LOW VOLUME ROADS
EKWULO, EMMANUEL OSILEMME
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CHAPTER 2
LITERATURE REVIEW
2.1 Pavement Design History
Pavement design is a complex field requiring knowledge of both soil and paving
materials, and especially, their responses under various loadings and environmental
conditions. Pavement design methods can vary, and have evolved over the years in
response to changes in traffic and loading conditions, construction materials and
procedures. Design methods have progressed from rule-of-thumb methods, to
empirical methods and at present, towards a mechanistic approach.
In the United States, the majority of pavement designers use the AASHTO
(American Association of State Highway and Transportation Official ) Guide for
design of Pavement Structures (AASHTO, 1993). The AASHTO Guide was
developed from empirical performance equations based on observations from the
AASHTO Road Test conducted in Illinois from October, 1958 to November, 1960.
Many significant changes in loading conditions, construction materials and methods,
and design needs have occurred since the time of AASHTO Road Test, prompting
development of new mechanistic-empirical design procedures. This procedure
allows the designer to consider current site conditions such as realistic loading,
climatic factors such as temperature and moisture, material properties and existing
pavement condition in the design of a new pavement, rehabilitation of an existing
pavement, or evaluation of an existing pavement. This approach is described in more
details in the Guide for mechanistic-empirical Design of New and Rehabilitated
Pavement Structures (NCHRP, 2004). Additionally, mechanistic-empirical design
procedure was developed such that improvement could be made as technology
advances.
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Empirical methods of analysis are derived from experimental data and practical
experience. The mechanistic-empirical (M-E) design approach considers the three
necessary elements of rational design (Yoder and Witczak, 1975). The element of
rational design include (1) an assumed failure or distress parameter predictive
theory (2) evaluation of material properties in relationship to the theory selected and
(3) relationship determination between the performance level desired and the
appropriate parameter magnitude. The mechanistic-empirical design approach
applies engineering mechanics principles to consider these rational design elements.
The initial phase of the mechanistic design approach consist of proper structural
modeling of pavement structures (NCHRP, 2004). Pavement is modeled as multi-
layered elastic or viscoelastic on elastic or viscoelastic foundation. These models are
used in analysis to predict critical pavement responses (deflections, stresses and
strains) due to traffic loading and environmental conditions for selected trial or
initial design. The accuracy of the chosen model is validated by data from controlled-
vehicle tests or other types of tests where actual loading and environmental
conditions are simulated. Where predicted values agree with measured values, the
level of confidence in the model increases with increase data available for validation.
Once an accurate structural response model is developed, the responses are input
into distress models to determine pavement damage throughout the specific design
period. Failure criteria are then evaluated, and an iterative process continues until a
final design is reached.
2.2 Flexible Highway Pavements
The beginning of flexible pavement construction history to early 1900’s in United
States when experience dominated pavement design and construction. Through the
experience gained over the years, many design methods were developed for
determining critical features like thickness of the asphalt surface. As of 1990, there
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were millions of miles of paved roads in the US, 94% of which are topped by asphalt
(Huang, 1993). A typical flexible pavement cross section consists of an asphalt
concrete surface, base and subbase resting on the natural subgrade.
Since the beginning of road building, three types of flexible pavement construction
have been used: conventional flexible pavement, full-depth asphalt and contained
rock asphalt mat (CRAM). As knowledge increased and other technologies
developed, a composite pavement made up of hot mix asphalt concrete (HMA) and
Portland cement concrete (PCC) beneath the HMA came into being with the most
desirable characteristics. However, the CRAM construction is still relatively rare and
composite pavement is very expensive, and hence seldom used in practice (Huang,
1993).
Various empirical methods have been developed for analyzing flexible pavement
structures. However, due to limitations of the analytical tools developed in the 1960s
and 1970s, the design of flexible pavements is still largely empirically-based. The
empirical method limits itself to a certain set of environmental and material
conditions (Huang, 1993), if the condition changes, the design is no longer valid. The
mechanistic-empirical method relates some inputs such as wheel loads to some
outputs, such as stress or strain. The mechanistic method is more reliable for the
extrapolation from measured data than empirical methods. However, the
effectiveness of any mechanistic design method relies on the accuracy of the
predicted stresses and strains. Due to their flexibility and power, three-dimensional
(3D) finite element methods are increasingly being used to analyze flexible
pavements.
2.3 Pavement Design and Management
Pavement engineering may be defined as the process of designing, construction,
maintenance, rehabilitation and management of pavement, in order to provide a
13
desired level of service for traffic. In the design stage of pavement design, engineers
make a number of assumptions about the construction methods and level of
maintenance for the pavement.
Flexible pavements are classified as a pavement structure having a relatively thin
asphalt wearing course, with layers of granular base and subbase being used to
protect the subgrade from being overstressed. This type of pavement design is based
on empiricism or experience, with theory playing only a subordinate role in the
procedure. However, the recent design and construction changes brought about
primarily by heavier wheel-loads, higher traffic levels, and recognition of various
independent distress modes contributing to pavement failure (such as rutting,
shoving and cracking) have led to the introduction and increased use of stabilized
base and Subbase material. The purpose of stabilizer material is to increase the
structural strength of the pavement by increasing rigidity. Roadway rehabilitation
using asphalt without the need for excavation of old, cracked and oxidized asphalt
pavements with water-weakened, or non-uniform support bases and subbases has
often been attempted, usually with variable success. It was concluded (Johnson and
Roger, 1992) that keeping water out of the road base and sub-base is a major solution
to prevent premature road failures.
The purpose of a pavement is to carry traffic safely, conveniently and economically
over its design life, by protecting the subgrade from the effects of traffic and climate
and ensuring that materials used in the pavement do not suffer from deterioration.
The pavement surface must provide adequate skid resistance. The structural part of
the pavement involves material sections that are suitable for the above purpose. The
design process consists of two parts: the determination of the pavement thickness
layer that have certain mechanical properties, and the determination of the
composition of the material that will provide these properties. The main structural
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layer of the pavement is the road base, whose purpose is to distribute traffic loads so
that stresses and strains developed by them in the subgrade and subbase are within
the capacity of the materials in these layers.
Asphalt pavements are designed and constructed to provide an initial service life of
between 15 to 20 years (Gervais et al, 1992), however, this design life is rarely met,
largely because of more traffic, heavier axle loads, material problems, higher tire
pressure and extreme environmental conditions. These factors usually result in two
major modes of distress: surface cracking and rutting which, if allowed to progress
too far, will require major rehabilitation or complete reconstruction. Research work
over the past several decades had led to many recommended solutions. New asphalt
mixes, use of larger crushes aggregates, textile sheets, thicker asphalt layer, polymer
modification and reinforcement of various types have been tried in the field to
minimize pavement cracking or rutting.
In asphalt pavement, the term “reinforcement” generally means the inclusion of
certain material with some desired properties within other materials which lack
these properties. Within the entire pavement structure, the asphalt concrete layer
receives most of the load and non-load induced tensile stresses. However, it is
known that asphalt concrete lacks the ability to resist such stresses which makes it an
ideal medium for which reinforcement can be considered. If reinforcement is to be
considered, two basic features need to be considered (Haas, 1984):
1. Intended function of the reinforcement
i. reducing rutting
ii. reducing cracking
iii. reducing layer thickness
iv. extending pavement life/reducing maintenance
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2. Reinforcement alternative
i. Types and possible locations in the pavement structure
ii. Major variables (pavement layer and reinforcement properties, traffic
loads and volume etc.
2.4 Flexible Pavement Design Principles
Before the 1920s, pavement design consisted basically of defining the thickness of
layered materials that would provide strength and protection to a soft subgrade.
Pavements were designed against subgrade shear failure. Engineers used their
experience based on successes and failures of previous projects. As experience
evolved, several pavement design methods based on subgrade shear strength were
developed. Ever since, there has been a change in design criteria as a result of
increase in traffic volume. As important as providing subgrade support, it is equally
important to evaluate pavement performance through ride quality and other surface
distress that increase the rate of deterioration of pavement structure. For this reason
performance became the focus of pavement designs. Methods based on serviceability
(an index of the pavement service quality) were developed based on test track
experiments. The AASHTO Road Test in 1960s as a seminal experiment from which
the AASHTO design guide was developed. Methods developed laboratory test data
or test track experiments in which model curves are fitted to data are typical
example of empirical methods. Although they may exhibit good accuracy, empirical
methods are valid for only the materials and climate conditions for which they were
developed.
Meanwhile, new materials started to be used in pavement structures that provide
better subgrade protection, but with their own failure modes. New designs criteria
were required to incorporate such failure mechanisms such as fatigue cracking and
permanent deformation in the case of asphalt concrete. The Asphalt Institute method
16
(Asphalt Institute, 1982, 1991) and the Shell method (Claessen et al, 1977; Shook et al,
1982) are examples of procedures based on asphalts concrete’s fatigue cracking and
permanent deformation failure modes. These methods were the first to use linear
elastic theory of mechanics to compute structural response in combination with
empirical models to predict number of loads to failure for flexible pavements. The
problem in the use of the elastic theory is that pavement material do not exhibit the
simple behaviour assumed in isotropic linear elastic theory. Nonlinearities, time and
temperature dependency, and anisotropy are some of the complicated features often
observed in pavement materials. Therefore to predict pavement performance
mechanistically, advanced modeling is required. The mechanistic design approach is
based on the theories of mechanics and relates pavement structural behaviour and
performance to traffic loading and environmental influences. Progress has been
made on isolated cases of mechanistic performance prediction problem, but the
reality is that fully mechanistic methods are not yet available for practical pavement
design (Schwartz and Carvalho, 2007).
Mechanistic-empirical approach is a hybrid approach. Empirical methods are used to
fill in the gaps that exist between the theory of mechanics and the performance of
pavement structures. Simple mechanistic responses are easy to compute with
assumptions and simplifications (that is homogenous material, small strain analysis,
static loading as typically assumed in linear elastic theory), but they themselves
cannot be used to predict performance directly: some type of empirical model is
required to carryout the appropriate correlation. Mechanistic-empirical methods are
considered an intermediate step between empirical and fully mechanistic methods.
2.5 Pavement Design Procedures
Studies in pavement engineering have shown that the design procedure for highway
pavement is either empirical or mechanistic. An empirical approach is one which is
17
based on the results of experiments or experience or both. This means that the
relationship between design inputs and pavement failure were arrived at through
experience, experimentation or a combination of both. The mechanistic approach
involves selection of proper materials and layer thickness for specific traffic and
environmental conditions such that certain identified pavement failure modes are
minimized. The mechanistic approach involves the determination of material
parameters for the analysis, at conditions as close as possible to what they are in the
road structure. The mechanistic approach is based on the elastic or visco-elastic
representation of the pavement structure. In mechanistic design, adequate control of
pavement layer thickness as well as material quality are ensured based on theoretical
stress, strain or deflection analysis. The analysis also enables the pavement designer
to predict with some amount of certainty the life of the pavement (Schwartz and
Carvalho, 2007).
2.5.1 Empirical Design Approach
An empirical design approach is one that is based solely on the result of experiment
or experience. Observations are used to establish correlations between the inputs and
the outcomes of a process, for example pavement design and performance. These
relationships generally do not have firm scientific basis, although they must meet the
tests of engineering reasonability. Empirical approaches are often used as an
expedient when it is too difficult to define theoretically the precise cause and effect
relationships of a phenomenon.
The principal advantages of empirical design approaches are that they are usually
simple to apply and are based on actual real-world data. Their principal
disadvantage is that the validity of the empirical relationships is limited to the
conditions in the underlying data from which they were inferred. New materials,
construction procedures, and changed traffic characteristics cannot be readily
incorporated into empirical design procedures.
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The first empirical method for flexible pavement design date to the mid 1920s when
the first soil classification were developed. One of the first to be published was the
Public Roads (PR) soil classification system (Huang, 2004). In 1929, the California
Highway Department developed a method using the California Bearing Ratio (CBR)
strength test (Porter, 1950; Huang, 2004). The CBR method relates the material’s CBR
value to the required thickness to provide protection against subgrade shear failure.
The thickness computed was defined for the standard crushed stone used in the
definition of the CBR test. The CBR test was improved by the US Corps of Engineers
(USCE) during the World War II and later became the most popular design method.
In 1945 the Highway Research Board(HRB) modified the PR classification. Soils were
grouped in seven categories (A-1 to A-7) with indexes to differentiate soils within
each group. The classification was applied to estimate subbase quality and total
pavement thickness (Huang, 2004).
Several methods based on subgrade shear failure developed after CBR method.
Huang (2004) used Terzaghi’s bearing capacity formula to compute pavement
thickness, while Huang (2004) applied logarithmic spirals to determine bearing
capacity of pavements. However, with increasing traffic volume and vehicle speed,
new materials were introduced in the pavement structure to improve performance
and smoothness and shear failure was no longer the governing design criterion.
The first attempt to consider a structural response as a qualitative measure of the
pavement structural capacity was measuring surface vertical deflection. A few
methods were developed based on the theory of elasticity for soil mass. This method
estimated layer thickness based on a limit for surface deflection. The first published
work on this method was the one developed by the Kansa State Highway
Commission, in 1947 (NCHRP, 2007), in which Boussinesg’s equation was used and
the deflection of subgrade was limited to 2.54mm. Later in 1953, the U.S. Navy
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applied Burmister’s two-layer elastic theory and limited the surface deflection to
6.35mm. Other methods were developed over the years, incorporating strength tests.
More recently, resilient modulus has been used (Huang, 2004) to establish
relationships between the strength and deflection limits for determining thickness of
new pavement structures and overlays. The deflection methods were most appealing
to practitioners because deflection is easy to measure in the field. However, failures
in pavements are caused by excessive stress and strain rather than deflection
(NCHRP, 2007). In the early 1950s, experimental tracks started to be used for
gathering pavement performance data. Regression models were developed linking
the performance data to design inputs. The biggest disadvantage of regression
methods is the limitation on their application. As is the case for any empirical
method, regression methods can be applied only to the conditions similar to those
for which they were developed. The empirical AASHTO method (AASHTO, 1993),
based on the AASHTO Road Test from the late 1950s, is the most widely used
pavement design method today. The AASHTO design equation is a regression
relationship between the number of load cycles, pavement structural capacity, and
performance measured in terms of serviceability. The concept of serviceability was
introduced in the AASHTO method as an indirect measure of the pavement’s ride
quality. The serviceability index is based on surface distress commonly found in
pavements.
The AASHTO (1993) method has been adjusted several times over the years to
incorporate extensive modifications based on theory and experience that allowed the
design equations to be used under conditions other than those of the AASHTO Road
Test.
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2.5.2 CBR Design Methods
The almost universal parameter used to characterize soils for pavement design
purpose is the California Bearing Ratio (CBR). This empirical index test was
abandoned in California over 50 years ago but, following its adoption by the US.
Corps of Engineers in World War II, it was gradually accepted World-wide as the
appropriate test (Brown, 1997). Given that the test is at best, an indirect measurement
of undrained shear strength and the pavement design requires knowledge of soil
resilience and its tendency to develop plastic strains under repeated loading, the
tenacity exhibited by generation of highway engineers in regard to the CBR is
somewhat surprising. Jim Porter, a Soil Engineer for the State of California,
introduced the “Soil Bearing Test” in 1929 commented nine years later, that the
bearing values are not direct measure of the supporting value of materials (Porter,
1938). In recognition that the CBR design curves give a total thickness of pavement to
prevent shear deformation in the soil, Turnbull (1950) noted that the CBR is an index
of shearing strength. The shear strength of soil is not of direct interest to the road
engineer, the soil should operate at stress levels within the elastic range (Brown,
1997). The pavement engineer is therefore more concerned with the elastic modulus
of soil and the behaviour under repeated loading.
The CBR method of pavement design is an empirical design method and was first
used by the California Division of Highways as a result of extensive investigations
made on pavement failures during the years 1928 and 1929 (Corps of Engineers,
1958). To predict the behaviour of pavement materials, the CBR was developed in
1929. Tests were performed on typical crushed stone representative of base course
materials and the average of these tests designated as a CBR of 100 percent. Samples
of soil from different road conditions were tested and two design curves were
produced corresponding to average and light traffic conditions. From these curves
the required thickness of Subbase, base and surfacing were determined. The
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investigation showed that soils or pavement material having the same CBR required
the same thickness of overlying materials in order to prevent traffic deformation. So,
once the CBR for the subgrade and those of other layers are known, the thickness of
overlying materials to provide a satisfactory pavement can be determined. The US
corps of Engineers adopted the CBR method for airfield at the beginning of the
Second World War, since then, several modifications of the original design curves
have been made (Oguara, 2005). Some of the common CBR design methods include
the Asphalt Institute (Asphalt Institute, 1981) method, the National Crushed Stone
Association (NCSA) design method (NCSA, 1972), the Nigerian (CBR) design
procedure (Highway Manuel, 1973) etc.
2.5.2.1 The Asphalt Institute CBR Method
Although the Asphalt institute has developed a new thickness design procedure
based on the mechanistic approach (Asphalt Institute, 1981), the original asphalt
institute thickness design procedure is based on the concept of full depth asphalt,
that is using asphalt mixtures for all courses above the subgrade or improved
subgrade. Traffic analysis is in terms of 80kN equivalent single axle load in the form
of a Design Traffic Number, DTN. The DTN is the average daily number of
equivalent 80kN single-axle estimated for the design period. The CBR, Resistance
value or Bearing value from plate loading test is used in subgrade strength
evaluation. Figure 2.1 shows the Thickness chart for Asphalt pavement structure.
The recommended minimum total asphalt pavement thickness (TA) is presented in
Table 2.1
2.5.2.2 The National Crushed Stone Association CBR Method
The National Crushed Stone Association (NCSA) empirical design method (NCSA,
1972) is based on the US Corps of Engineers pavement design. Traffic analysis is
based on the average number of 80kN single-axle loads per lane per day over a
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pavement life expectancy of 20 years. The method incorporates a factor of traffic in
the design called Design Index (DI). Six design index categories are defined as
presented in Table 2.2. In the absence of traffic survey data, general grouping of
vehicles can be obtained from spot checks of traffic and placed in one of the three
groups as follows:
Group 1: Passenger cars, panel and pickup trucks
Group 2: Two-axle trucks loaded or larger vehicles empty or carrying light
Loads.
Group 3: All vehicles with more than three loaded axles
Subgrade strength evaluation is made in terms of CBR and compaction requirement
is provided to minimize permanent deformation due to densification under traffic.
Presented in Figure 2.2 is the NCSA design chart.
Figure 2.1: Thickness Requirement for Asphalt Pavement Structure (Source: Oguara, 2005)
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Table 2.1.: Minimum Asphalt Pavement Thickness(TA) (Source: Oguara, 2005)
Traffic DTN Minimum TA(mm)
Light Less than10 100
Medium 10 - 100 125
Heavy 100 – 1000 More than
1000
150 175
Table 2.2: NCSA Design Index categories (Source: Oguara, 2005)
Design Index
General Character Daily ESAL
DI-1 Light traffic (few vehicles heavier than passenger cars, no regular use by Group 2 or 3 vehicles)
5 or less
DI-2 Medium-light traffic (similar to DI-1, maximum 1000 VPD including not over 5% Group 2, no regular use by Group 3 vehicles
6-20
DI-3 Medium traffic (maximum 3000VPD, including not over 10% Group 2 and 3, 1% Group 3 vehicles)
21-75
DI-4 Medium – heavy traffic (maximum 6000VPD, including not over 15% Group 2 and 3, 1% Group 3 vehicles)
76-250
DI-5 Heavy traffic (maximum 6000VPD, may include 25% Group 2 and 3, 10% Group 3 vehicles)
251-900
DI-6 Very heavy traffic (over 6000VPD, may include over 25% Group 2 or 3 vehicles)
901-3000
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2.5.2.3 The Nigerian CBR Method
The Nigerian (CBR) design procedure is an empirical procedure which uses the
California Bearing Ratio and traffic volume as the sole design inputs. The method
uses a set of design curves for determining structural thickness requirement. The
curves were first developed by the US Corps of Engineers and modified by the
British Transportation and Road Research Laboratory (TRRL, 1970), it was adopted
by Nigeria as contained in the Federal Highway Manual (Highway Manuel, 1973).
The Nigerian (CBR) design method is a CBR-Traffic volume method, the thickness of
the pavement structure is dependent on the anticipated traffic, the strength of the
foundation material, the quality of pavement material used and the construction
procedure. This method considers traffic in the form of number of commercial
vehicles/day exceeding 29.89kN (3 tons). Subgrade strength evaluation is made in
terms of CBR. The selection of pavement structure is made from design curves
shown in Figure 2.3.
Figure 2.2: NCSA Design Chart (Source: Oguara, 2005)
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The thickness of the pavement layers is dependent on the expected traffic loading.
Recommended minimum asphalt pavement surface thickness is considered in terms
of light, medium and heavy traffic as follows:
Light traffic - 50mm
Medium - 75mm
Heavy - 100mm
Figure 2.3: The Nigerian CBR Design chart (Source: Oguara, 2005)
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2.5.2.4 The AASHTO Pavement Design Guides
The AASHTO Guide for Design of Pavement Structures is the primary document
used to design new and rehabilitated highway pavements. The Federal Highway
Administration's 1995-1997 National Pavement Design Review found that some 80
percent of states use the 1972, 1986, or 1993 AASHTO Guides (AASHTO, 1972;
1986; 1993), of the 35 states that responded to a 1999 survey by Newcomb and
Birgisson (1999), 65% reported using the 1993 AASHTO Guide for both flexible and
rigid pavement designs.
All versions of the AASHTO Design Guide are empirical methods based on field
performance data measured at the AASHO Road Test in 1958-60, with some
theoretical support for layer coefficients and drainage factors. The overall
serviceability of a pavement during the original AASHO Road Test was quantified
by the Present Serviceability Rating (PSR; range = 0 to 5), as determined by a panel
of highway raters. This qualitative PSR was subsequently correlated with more
objective measures of pavement condition (e.g., cracking, patching, and rut depth
statistics for flexible pavements) and called the Pavement Serviceability Index (PSI).
Pavement performance was represented by the serviceability history of a given
pavement - i.e., by the deterioration of PSI over the life of the pavement. Roughness
is the dominant factor in PSI and is, therefore, the principal component of
performance under this measure.
2.5.3 Mechanistic Design Approach
The mechanistic design approach represents the other end of the spectrum from the
empirical methods. The mechanistic design approach is based on the theories of
mechanics to relate pavement structural behavior and performance to traffic
loading and environmental influences. The mechanistic approach for rigid
pavements has its origins in Westergaard's (Westergaard, 1926) development
27
during the 1920s of the slab on subgrade and thermal curling theories to compute
critical stresses and deflections in a PCC slab. The mechanistic approach for flexible
pavements has its roots in Burmister's (Burmister, 1945) development during the
1940s of multilayer elastic theory to compute stresses, strains, and deflections in
pavement structures.
A key element of the mechanistic design approach is the accurate prediction of the
response of the pavement materials - and, thus, of the pavement itself. The
elasticity-based solutions by Boussinesq, Burmister, and Westergaard were an
important first step toward a theoretical description of the pavement response
under load. However, the linearly elastic material behavior assumption underlying
these solutions means that they will be unable to predict the nonlinear and inelastic
cracking, permanent deformation, and other distresses of interest in pavement
systems. This requires far more sophisticated material models and analytical tools.
Much progress has been made in recent years on isolated pieces of the mechanistic
performance prediction problem. The Strategic Highway Research Program during
the early 1990s made an ambitious but, ultimately, unsuccessful attempt at a fully
mechanistic performance system for flexible pavements. To be fair, the problem is
extremely complex; nonetheless, the reality is that a fully mechanistic design
approach for pavement design does not yet exist. Some empirical information and
relationships are still required to relate theory to the real world of pavement
performance.
2.5.4. Mechanistic –Empirical Design Approach
The development of mechanistic-empirical design approaches dates back at least
four decades. As its name suggests, a mechanistic-empirical approach to pavement
design combines features from both the mechanistic and empirical approaches. The
induced state of stress and strain in a pavement structure due to traffic loading and
environmental conditions is predicted using theory of mechanics. Empirical models
28
link these structural responses to distress predictions. Huang (1993) notes that
Kerkhoven and Dormon (1953) were the first to use the vertical compressive strain
on top of the subgrade as a failure criterion to reduce permanent deformation. Saal
and Pell (1960) published the use of horizontal tensile strain at the bottom of the
asphalt bound layer to minimize fatigue cracking. The concept of horizontal tensile
strain at the bottom of the asphalt bound layer was first used by Dormon and
Metcaff 1965) for pavement design. The Shell method (Claussen et al, 1977) and the
Asphalt Institute method (Shook et al, 1982; Asphalt Institute, 1992) incorporated
strain-based criteria in their mechanistic-empirical procedures. Several studies over
the past fifteen years have advanced mechanistic-empirical techniques. Most of the
works, however, were based on variants of the same two strain-based criteria
developed by Shell and the Asphalt Institute. The Washington State Department of
Transportation (WSDOT), North Carolina Department of Transportation(NCDOT)
and Minnesota Department of Transportation(MNDOT), to name but a few,
developed their own Mechanistic-Empirical procedures (Schwartz and Carvalho,
2007). The National Cooperative Highway Research Program (NCHRP) 1-26 project
report, Calibrated Mechanistic Structural Analysis Procedures for Pavements (1990),
provided the basic framework for most of the efforts made by state DOTs. WSDOT
(Pierce et al., 1993; WSDOT, 1995).
2.5.5 Layered Elastic System
The analysis of stresses, strains and deflections in pavement systems have been
largely derived from the Boussinesq equation originally developed for a
homogeneous, isotropic and elastic media due to a point load at the surface.
According to Boussinesq, the vertical stress σZ at any depth z below the earth’s
surface due to a point load P at the surface is given by (Oguara, 2005):
29
σZ = 2
.Z
Pk (2.0)
Where,
k = ( )[ ] 2
52
1
1
2
3
z
r+π (2.1)
and
r is the radial distance from the point of load application.
For stress on a vertical plate passing through the centre of a loaded plate:
σZ = ( )
+−
23
22
3
1zr
zP (2.2)
Where,
P is the unit load on a circular plate of radius r ( or of a tyre of known contact area
and pressure). Here the vertical stress is dependent on the depth z and radial
distance r and is independent of the properties of the transmitting medium.
Considering radial strains which is dependent on Poisson’s ratio µ, from equation
(2.2) and µ = 0.5, the Boussinesq equation for deflection, ∆ at the centre of a circular
plate is given as:
∆ = ( )
( ) 21
22
2
2
3
zrE
rP
+ (2.3)
This may be written as
∆ = FE
aP )( (2.4)
Where, F = ( )[ ] 2
12
1
1.
2
3
zr+
(2.5)
30
The term F reflects the depth-radius ratio. The value of F when taken at the contact
surface equals 1.5 and 1.18 for flexible and rigid plate respectively.
For flexible plate, the deflection at the centre of the loaded circular plate of radius
“a” is therefore given as:
∆ = E
Pa5.1 (2.6)
and for a rigid plate, the deflection is given as:
∆ = E
Pa18.1 (2.7)
From equations (2.6) and (2.7), the modulus of elasticity E of a soil or pavement can
be computed by measuring the deflection under a known load and contact area
(Oguara, 2005). The fact that pavement deflection can be directly related to Hook’s
law that says stress σ is proportional to strain Є, or to the modulus of elasticity of the
material, has brought forth the use of elastic layered systems – a mechanistic
approach in design of pavements (Oguara, 1985)
The response of pavement systems to wheel loading has been of interest since 1926
when Wetergaard used elastic layered theory to predict the response of rigid
pavements (Westergaard, 1926). It is generally accepted that pavements are best
modeled as a layered system, consisting of layers of various materials (concrete,
asphalt, granular base, subbase etc.) resting on the natural subgrade. The behaviour
of such a system can be analyzed using the classical theory of elasticity (Burmister,
1945). The Layered Elastic Analysis (LEA) is a mechanistic-empirical procedure
capable of determining pavement responses (stress and strain) in asphalt pavement.
The major assumptions in the use of layered elastic analysis are that;
31
i. the pavement structure be regarded as a linear elastic multilayered system
in which the stress-strain solution of the material are characterized by the
Young’s modulus of Elasticity E and poison’s ratio µ.
ii. Each layer has a finite thickness h except the lower layer, and all are infinite
in the horizontal direction.
iii. The surface loading P can be represented vertically by a uniformly
distributed vertical stress over a circular area.
In three-layered pavement system, the locations of the various stresses are as shown
in Figure 2.4 (Yoder and Witczak, 1975). The horizontal tensile strain at the bottom of
the asphalt concrete layer and vertical compressive strain at the top of the subgrade
are given by equations 2.8 and 2.9 respectively;
Єr1 = 1
11
1
11
1
1
EEE
zrr σµ
σµ
σ−− (2.8)
Єz1 = ( )32
3
1rz
Eσσ − (2.9)
Where,
1zσ = vertical stress at interface 1 (bottom of asphalt concrete layer)
2zσ = vertical stress at interface 2
1rσ = horizontal stress at the bottom of layer 1
2rσ = horizontal stress at the bottom of layer 2
3rσ = horizontal stress at the top of layer 3
31 EandE are Modulus of elasticity of layer 1 and 3 receptively.
µ = Poisson’s ratio of the layer
32
2.5.6 Finite Element Model
The Finite Element Method (FEM) is a numerical analysis technique for obtaining
approximate solutions to engineering problems. In the finite element analysis of
asphalt pavements, the pavement and subgrade is descritized into a number of
elements with the wheel load at the top of the pavement. The FEM assumes some
constraining values at the boundaries of the region of interest (pavement and
subgrade) and is used to model the nonlinear response characteristic of pavement
materials.
2.5.7 Mechanistic-Empirical Design Inputs
Inputs for M-E pavement design include traffic, material and subgrade
characterization, climate factors and performance criteria. Layered elastic models
require a minimum number of inputs to adequately characterize a pavement
structure and its response to loading. Some of the inputs include modulus of
elasticity (E) and Poisson’s ratio (µ) of material, pavement thickness(h) and the
P
µ1 = 0.5, h1, E1
µ2 = 0.5, h2, E2
µ1 = 0.5, h3, E2
a
σz1
σr1
σz2
σr2
σr3
Interface 1
Interface 2
Figure 2.4: Three-Layer Pavement System Showing Location of Stresses
33
loading (P). In the Mechanistic-Empirical(M-E) pavement design guide (AASHTO,
1993), three levels of material inputs are adopted as shown in Table 2.3. Level 1
material input is obtained through direct laboratory testing and measurements. This
level of input uses the state of the art technique in characterization of materials as
well as characterization of traffic through collection of data from weigh-in-motion
(WIM) stations; Level 2 uses correlations to determine the required material inputs,
while Level 3 uses material inputs selected from typical defaults values. Tables 2.4
and 2.5 shows typical input values for some pavement materials. The outputs
expected in layered elastic analysis are the pavement responses; stresses, strains and
deflections.
Table 2.3: Inputs levels in layered elastic Design
Material Input
Level 1
Input
Level 2
Input
Level 3
Asphalt Concrete Measured
Diametric Modulus
Estimated
Diametric Modulus
Default
Diametric Modulus
Portland Cement
Concrete
Measured
Elastic Modulus
Estimated
Elastic Modulus
Default
Elastic Modulus
Stabilized Materials Measured
Resilient Modulus
Estimated
Resilient Modulus
Default
Resilient Modulus
Granular Materials Measured
Resilient Modulus
Estimated
Resilient Modulus
Default
Resilient Modulus
Subgrades Measured
Resilient Modulus
Estimated
Resilient Modulus
Default
Resilient Modulus
34
Table 2.4: Default Resilient Modulus (Mr) Values for Pavement Materials
General Level of Subgrade Support
AASHTO Soil Classification Broad Mr range and Mean Mr at Optimum Moisture
Content
Very Good Coarse grained: Gravel and gravely soils; A-1-a, A-1-b
172 to 310MPa Mean = 269MPa
Good Coarse grained: Sand and Sandy soils A-2-4, A-3
138 to 275MPa Mean = 207MPa
Fair Fined grained: Mixed silt and clay A-2-7, A-4, A-2-5, A-2-6
103 to 207MPa Mean = 179MPa
Poor Fine grained: Low compressibility A-5, A-6
69 to 172MPa Mean = 124MPa
Very Poor Fine grained: High compressibility A-7-5, A-7-6
34 to 103MPa Mean = 69MPa
Crushed Stone 138 to 241MPa Mean = 172MPa
NOTE: Subgrade properties for the above soil classes are as follows Very Poor: (PI = 30, No. 200 = 85%, No. 4 = 95%, D60 = 0.02mm) Poor: (PI = 15, No. 200 = 75%, No. 4 = 95%, D60 = 0.04mm) Fair: (PI = 7, No. 200 = 30%, No. 4 = 70%, D60 = 1.0mm) Good: (PI = 5, No. 200 = 20%, No. 4 = 61%, D60 = 3.0mm) – Meets most agencies spec for subbase materials. Very Good: (PI = 1, No. 200 = 5%, No. 4 = 47%, D60 = 8.0mm) Meets most agencies spec for base material.
Table 2.5: Typical Poison’s Ratio Values for Pavement Materials (NCHRP, 2004; WSDOT, 2005)
Material µ Range Typicalµ
Clay (saturated) 0.4 - 0.5 0.45
Clay (unsaturated) 0.1 - 0.3 0.2
Sandy clay 0.2 - 0.3 0.25
Silt 0.3 - 0.35 0.325
Dense sand 0.2 - 0.4 0.30
Coarse-grained sand 0.15 0.15
Fine-grained sand 0.25 0.25
Bedrock 0.1 - 0.4 0.25
Crushed Stone 0.1 – 0.45 0.30
Cement Treated Fine-grain
Materials
0.15 – 0.45 0.40
35
2.5.8 Traffic Loading
An important factor affecting pavement performance is the number of load
repetitions and the total weight a pavement experiences during its lifetime.
Although it is not too difficult to determine a wheel or an axle load for an individual
vehicle, it becomes quite complicated to determine the number and types of wheel/
axle loads that a particular pavement will be subjected to over its design life.
Furthermore, it is not the wheel load but rather the damage to the pavement caused
by the load that is of primary concern. The most common approach is to convert
damage from wheel loads of various magnitude and repetitions (“mixed traffic”) to
damage from an equivalent number of “standard” or “equivalent” loads. The most
commonly used equivalent load is the 18,000lb (80kN) Equivalent single axle Load
ESAL. As a result of variation in traffic loading, many pavement design agencies
have developed multiplying factors called “load equivalency factors” as a means of
reducing the variation in traffic loading to single load conditions. The most widely
used load equivalency factor are those developed at the AASHTO Road Test
(AASHTO, 1972). A “load equivalency factor” represents the number of ESALs for
the given weight-axle combination. The AASHTO (2002) Guide for the Design of New
and Rehabilitated Pavement Structures adopts the load spectra approach in M-E design
of pavements. In essence, the load spectra approach uses the same data that ESAL
approach uses only it does not convert the loads to ESALs – it maintains the data by
axle configuration and weight.
For Nigerian traffic condition, traffic analysis could be based on the number of axle
loads of commercial vehicles expressed in terms of an equivalent 80kN single axle
load. There are no load equivalency factors developed in Nigeria, therefore, the
AASHTO equivalency factors could be used in design. Traffic analysis procedure
36
suggested by Oguara (1985) involves the determination of the number of 80kN
equivalent standard axle load (ESAL) as follows:
ESAL = FV TxN∑ (2.10)
TF = ∑V
F
N
ExNA (2.11)
Where,
NV = number of commercial vehicles
NA = Number of axles
TF = Truck or commercial vehicle factor
EF = Load equivalency factors
The truck factors could be calculated from specific truck/ commercial vehicle axle
and weight data. Shook et al, (1982) presented typical truck factors for different
classes of highways and vehicles in the United States. AASHTO (1993)
recommended the estimation of design ESAL from traffic volume. This involves
converting the daily traffic volume into an annual ESAL amount. Pavements are
typically designed for the critical lane or “design lane”, which accounts for traffic
distribution (Pavement interactive, 2008). The ESALs per year is given by:
ESALs per year = (Vehicle/day) x (Lane Distribution Factor) x (days/yr.) x
(ESALs/vehicle) (2.12)
The design ESAL is given by:
ESAL = ESALs per year x ( )
g
gn
11 −+ (2.13)
Where,
n = design period
g = annual growth rate.
37
The Nigerian Highway manual recommended a procedure for estimation of traffic
repetitions (Nanda, 1981) using Table 2.6.
Table 2.6: Vehicle Classification (Nanda, 1981)
Class Description (Nanda, 1981)
Typical ESALs per Vehicle
1 Passenger cars, taxis, landrovers, pickups, and
mini-buses.
Negligible
2 Buses 0.333
3 2-axle lorries, tippers and mammy wagons 0.746
4 3-axle lorries, tippers and tankers 1.001
5 3-axle tractor-trailer units (single driven axle,
tandem rear axles)
3.48
6 4-axle tractor units (tandem driven axle,
tandem rear axles)
7.89
7 5-axle tractor-trailer units(tandem driven axle,
tandem rear axles)
4.42
8 2-axle lorries with two towed trailers 2.60
2.5.9 Material Properties
The ability to calculate the response of pavement structure due to vehicle load
depends on a proper understanding of the mechanical properties of the constituent
materials. In M-E pavement design, material characterization requires the
determination of the material stiffness as defined by the elastic modulus and
Poisson’s ratio. The elastic modulus can either be determined or correlated with
conventional test. In many cases where there is need for laboratory testing, the
method of testing the modulus should reproduce field conditions as accurately as
possible. Generally, the dynamic modulus, diametric resilient modulus, and indirect
tensile test are used for asphalt concrete and stabilized materials; the resilient
modulus test is mainly used for granular materials.
38
2.5.9.1 Elastic Modulus of Bituminous Materials
The dynamic modulus test can be used to determine the linear viscoelastic properties
of bituminous materials. The dynamic modulus is derived from the complex
modulus E* defined as a complex number that relates stress to strain for a linear
viscoelastic material subjected to sinusoidal loading at a given temperature and
loading frequency (Yorder and Witczak, 1975). The dynamic complex modulus test
accounts not only for the instantaneous elastic response without delayed effects, but
also the accumulation of cyclic creep and delayed elastic effects with the number of
cycles. The dynamic modulus test does not allow time for any delayed elastic
rebound during the test, which is the fundamental difference from the resilient
modulus test. The test is conducted as specified in ASTM D3497-79 on unconfined
cylindrical specimen100mm diameter by 200mm high using uniaxialy applied
sinusoidal stress pattern. Strains are recorded using bonded wire strain gauges and
a-channel recording system.
By definition, the absolute value of the complex modulus *E is commonly referred
to as dynamic modulus.
E* = φε
σ
φε
σ
SinCos 0
0
0
0 + (2.14)
Where,
σ0 = stress amplitude (N/mm2)
ε0 = recoverable strain amplitude (mm/mm)
Ф = the phase lag angle (degrees)
For and elastic material, Ф = 0,, hence the dynamic modulus is calculated using
equation 2.15(Yoder and Witczak, 1975)
E* = 0
0*ε
σ=E (2.15)
39
Thus the elastic or dynamic modulus of bituminous materials may be determined by
dividing the peak stress σ0 to strain amplitude ε0 from dynamic modulus test.
The elastic modulus of bituminous materials can also be determined by means of the
diametric resilient modulus device developed by Schmidt (Schmidt, 1972) which is a
repetitive load test on cylindrical specimen 100mm diameter by 63mm high,
fabricated either by marshal apparatus or Hveen Kneading compactor. The repeated
load is applied across the diameter, placing the specimen in a state of tensile stress
along the vertical diameter. Linear Variable Differential Transducers (LVDT)
mounted on each side of the horizontal specimen axis measure the lateral
deformation of the specimen under the applied load. One of the major difference
between a resilient modulus test and a dynamic complex modulus test for asphalt
concrete mixtures is that the resilient modulus test has a loading of one cycle per
second (1 Hz) with a repeated 0.1 second sinusoidal load followed by a 0.9 second
rest period, while the dynamic modulus test applies a sinusoidal loading without
rest period.
Knowledge of the dynamic load and deformations allow the resilient modulus to be
calculated. Frocht (1948) gave expressions for the stresses σx and σy across the
diameter ”d” perpendicular to the applied load P as:
Horizontal Diametral Plane:
+
−=
22
22
4
4
..
2
xd
xd
dt
Px
πσ (2.16)
−
+−= 1
4..
222
2
xd
d
dt
Py
πσ (2.17)
τxy = 0 (2.18)
40
Vertical Diametral Plane:
dt
Px
..
2
πσ = (2.19)
−
++
−−=
dydyddt
Py
1
2
2
2
2
..
2
πσ (2.20)
τxy = 0 (2.21)
where,
t is the specimen thickness and x and y are the distance from the origin along
the x and y-axis.
Thus, if the horizontal deformation across a cylindrical specimen resulting from an
applied vertical load is known the modulus of elasticity can be calculated.
2.5.9.2 Prediction Model for Dynamic and Elastic Modulus of Asphalt Concrete
To perform a dynamic modulus test is relatively expensive. Efforts were made by
asphalt pavement researchers to develop regression equation to estimate the
dynamic modulus for a specific hot mix design. One of the comprehensive asphalt
concrete mixture dynamic modulus models is the Witczak prediction model
(Christensen et al, 2003). It is proposed in the AASHTO M-E Design Guide and the
calculations were based on the volumetric properties of a given mixture.
Witczak’s prediction equation is presented in equation 2.22a
[ ])22.2(
1
00547.0)(000017.0003958.00021.0871977.3
)(802208.0058097.0002841.0)(001767.0029232.0249937.1log
)log393532.0log313351.0603313.0(
34
2
38384
4
2
200200
*
ae
PPPP
VV
VVPPPE
f
abeff
beff
a
η−−−
+−+−+
+−−−−+−=
Where
*E = Dynamic modulus, in 105 Psi
41
η = Bituminous viscosity, in 106 Poise (at any temperature, degree of aging)
f = Load frequency, in Hz
Va = Percent air voids content, by volume
Vbeff = Percent effective bitumen content, by volume
P34 = Percent retained on 19mm sieve, by total aggregate weight(cumulative)
P38 = Percent retained on 9.51mm sieve, by total aggregate weight(cumulative)
P4 = Percent retained on 4.76mm sieve, by total aggregate weight(cumulative)
P200 = Percent retained on 0.074mm sieve, by total aggregate weight(cumulative)
Asphalt concrete elastic modulus can also be predicted using equation 2.22.
Researches have indicated that the dynamic modulus values of asphalt concrete
measured at a loading frequency of 4Hz is comparable with the elastic modulus
values (FDOT, 2007; TM 5-822-13/AFJMAN 32-1018, 1994). The elastic modulus can
then be predicted by modifying equation 2.22b as follows:
[ ])22.2(
1
00547.0)(000017.0003958.00021.0871977.3
)(802208.0058097.0002841.0)(001767.0029232.0249937.1log
)log393532.07919691.0(
34
2
38384
4
2
200200
be
PPPP
VV
VVPPPE
abeff
beff
a
η−−
+−+−+
+−−−−+−=
Where
E = Elastic modulus, in 105 Psi
η = Bituminous viscosity, in 106 Poise (at any temperature, degree of aging)
Va = Percent air voids content, by volume
Vbeff = Percent effective bitumen content, by volume
P34 = Percent retained on 19mm sieve, by total aggregate weight(cumulative)
P38 = Percent retained on 9.51mm sieve, by total aggregate weight(cumulative)
P4 = Percent retained on 4.76mm sieve, by total aggregate weight(cumulative)
P200 = Percent retained on 0.074mm sieve, by total aggregate weight(cumulative)
42
2.5.9.3 Elastic Modulus of Soils and Unbound Granular Materials
The elastic properties of subgrade soils and unbound granular materials for base and
subbase courses can be measured directly by the Resilient Modulus test using a
triaxial test device capable of applying repeated dynamic loads of controlled
magnitude and duration. The resilient (recoverable) deformation over the entire
length of the specimen could be measured with LVDT. The specimen size is
normally 100mm in diameter by 200mm high. The Resilient modulus is calculated by
dividing the repeated axial stress σd (equal to the deviator stress) by the recoverable
strain εr.
For unbound granular materials, the resilient modulus MR, which is stress
dependent, is given as (Shook et al, 1982):
MR = K1.θ.K2 (2.23)
Where, K1 and K2 are material constants experimentally determined and
θ = the sum of principal stresses.
If repeated load test equipment is not available, the Resilient Modulus of subgrade
may be estimated from CBR values by using the relationship developed by
Heukelom and Klomp, (1962) as:
MR(MPa) = 10.3 CBR (2.24a)
MR(psi) = 1500CBR (2.24b)
For subgrade soaked CBR value between 1 and 10%
For unbound base material layers, the resilient modulus may be assumed to be a
function of the thickness of the layer h and the modulus of the subgrade reaction
MRs (Emesiobi, 2000) as shown in equation (2.25)
43
MR = 0.2 x h0.45 x MRs (2.25)
Where,
h is in millimeters and MR must lie between 2 and 4 times MRs.
The AASHTO Guide for design of pavement structures (AASHTO, 1993)
recommends a standard method of calculating subgrade modulus. This method
involves calculating a weighted average subgrade resilient modulus based on the
relative pavement damage. Because lower values of subgrade resilient modulus
result in more pavement damage, lower values o subgrade resilient modulus is
weighted more heavily. The relative damage equation used in the 1993 AASHTO
Guide is:
fu = (1.18 x 108)32.2−
RM (2.26)
Where,
fu = relative damage factor
MR = resilient modulus in psi
Therefore, over an entire year, the average relative damage is given by:
n
uuuu
fnff
f
+++=
...21 Where, n = 12.
When triaxial test equipment for resilient modulus is not available, the U.S Army
Corps of Engineers (Hall and Green, 1975) recommends the estimation of resilient
modulus for unbound granular material using equation 2.27.
MR(psi) = 5409(CBR)0.71 (2.27)
Researches have also revealed some useful relationship between CBR and resilient
modulus “E” of stabilized laterite (Ola, 1980) as follows;
For soaked specimen,
E(psi) = 250(CBR)1.2 (2.28)
44
For unsoaked specimen
E(psi) = 540(CBR)0.96 (2.29)
2.5.9.4 Non-linearity of Pavement Foundation
The non-linearity of pavement foundation has been demonstrated both from insitu
measurement of stress and strain (Brown and Bush, 1972; Brown and Pell, 1967)
using field instrumentation, and through back-analysis of surface deflections bowls
measured with the Falling Weight Deflectometer. These non-linearity characteristics
have also been extensively studied using repeated load triaxial facilities and various
models proposed for use in pavement analysis. Some of these are quite sophisticated.
For granular materials, the use of stress dependent bulk and shear modulus provides
a much more sounder basis for analysis than the simple “k-θ” model in which the
resilient modulus is expressed as a function of the mean normal stress and usually, a
fixed value of Poisson’s ratio is adopted, typically 0.3.
For fine grained soils, emphasis has been placed on the relationship between resilient
modulus and deviator stress following the early work done by Seed et al (1962). For
saturated silty- clay, Brown et al (1987) suggested the following model based on a
series of good quality laboratory tests;
Gr =
m
r
or
q
P
C
q
'
(2.30)
Where Gr = Resilient shear modulus
qr = Repeated deviator stress
P0’ = Mean normal effective stress
C, m = Constant for the particular soil
For partially saturated soils with degree of saturation in excess of 85%, the same
equation was valid with P0’ being replaced by the soil suction.
45
2.5.9.5 Poisson’s Ratio
The Poisson’s ratio µ is defined as the ratio of lateral strain εL to the axial strain εa
caused by a load parallel to the axis in which the strain is measured (Oguara, 1985).
Values of Poisson’s ratio are generally estimated, as most highway agencies use
typical values as design inputs in elastic layered analysis. Table 2.7 gives typical
Poisson’s ratio values by various agencies.
Table 2.7: Poisson’s Ratio Used by Various Agencies (Oguara, 2005)
Material Original Shell Oil Company
Revised Shell Oil Company
The Asphalt Institute
Kentucky Highway Department
Asphalt Concrete 0.5 0.55 0.40 0.40
Granular Base 0.5 0.53 0.45 0.45
Subgrade 0.5 0.35 0.45 0.45
If deformations are monitored from either static or dynamic test, an approximate µ
value could be obtained from equation (2.28):
µ =
∆−
0
11
2
1
V
V
aε (2.31)
Where,
V = volume of the material
2.5.9.6 Climatic Conditions
The mechanical parameters of both bounded and unbound layers in pavement
structures are seasonally affected. It is therefore important to understand their
seasonal variations in order to be able to predict their effect on pavement
performance. In mechanistic design, two climatic factors, temperature and moisture
are considered to influence the structural behaviour of the pavement, for instance,
temperature influences the stiffness and fatigue of bituminous materials and is the
major factor in frost penetration. Moisture conditions influence the stiffness and
strength of base course, subbase course and subgrade.
46
In most pavement design procedures, the effect of the environment is accounted for
by including them in the material properties. The mean annual air temperature
MAAT or mean monthly air temperature MMAT have been generally used in
pavement design analysis. Because the effect of freezing and thawing is very serious
in temperate regions, more attention has been directed towards design of pavement
to resist spring thaw effects. These efforts have several times led to loss of subgrade
supporting capacity, a phenomenon called spring break up.
In Mechanistic design, the effect of environmental factors is included in the analysis.
The moisture and temperature variation for each sub-layer within the pavement, or a
representative temperature need to be determined. In the Asphalt institute design
method, pavement temperature can be determined by (Witczak, 1972):
MMPT = MMAT( ) ( )
+
+−
++ 6
4
34
4
11
zz (2.32)
Where,
MMPT = mean monthly pavement temperature
MMAT = mean monthly air temperature
Z = depth below pavement surface (inches)
Pavement design is usually predicated on a subgrade which is assumed to be near-
saturation. The design may be based on subgrade with lower moisture content if
available field measurement indicates that the subgrade will not reach saturation.
For Nigerian climatic condition, the most damaging environmental factor is rainfall,
which unfortunately has not received as much attention as that of frost or freeze-
thaw action. Although the soaked CBR test has been used to simulate the worst
environmental conditions, this may be over conservative in the dry regions of
Nigeria. The provision of adequate drainage facility and proper compaction of
47
pavement materials will go a long way to alleviate the effect of the environment ,
especially rainfall on pavements (Oguara, 1985).
2.6 Pavement Response Models
Mechanistic-empirical design procedure requires calculation of the critical structural
responses (stresses, strains or displacements) within the pavement layers induced by
traffic and/ or environmental loading. These responses are used to predict damage
in the pavement system which is later related to the pavement distresses (cracking or
rutting). Basically, two types of mechanistic models are commonly used to model
flexible pavements; the layered elastic model (LEA) and the finite element model
(FEM). Both of these models can easily be run on personal computers and only
require data that can be realistically obtained.
2.6.1 Layered Elastic Model
A layered elastic model can compute stresses, strains and deflections at any point in
a pavement structure resulting from the application of a surface load. The layered
elastic model assumes that each pavement layer is homogenous, isotropic and
linearly elastic (Burmister, 1945) and could be used to analyze pavement distress
(Peattie, 1963). The layered elastic approach works with relatively simple
mathematical models and thus, requires some basic assumptions. These assumptions
are:
i. Pavement layers extend infinitely in the horizontal direction.
ii. The bottom layer (usually the subgrade) extends infinitely downwards.
iii. Materials are not stressed beyond their elastic ranges.
Layered elastic models require a minimum number of inputs such as Thickness of
the pavement layers, Material properties (modulus of elasticity and Poisson’s ratio)
and Traffic loading (Weight, wheel spacing, and axle spacing) to adequately
characterize a pavement structure and its response to loading. The outputs of a
48
layered elastic model are the stresses, strains, and deflections in the pavements.
Layered elastic computer programs are used to calculate the theoretical stresses,
strains and deflections anywhere in a pavement structure. Table 2.8 and Figure 2.5
however, show few critical locations that are often used in pavement analysis.
Table 2.8: Critical Analysis Locations in a Pavement Structure
Location Response Reason for Use
Pavement Surface Deflection Used in imposing load restrictions during spring thaw and overlay design
Bottom of HMA Layer Horizontal Tensile Strain Used to predict fatigue in the HMA layer
Top of intermediate Layer (Base or Surface)
Vertical Compressive Strain
Used to predict rutting failure in the base or subbase
Top of Subgrade Vertical Compressive Strain
Used to predict rutting failure in the subgrade
1. Pavement surface deflection 2. Horizontal tensile strain at the bottom of bituminous layer 3. Vertical compressive strain at top of base 4. Vertical compressive strain at top of subgrade
Figure 2.5: Critical Analysis Locations in a Pavement Structure (Pavement Interactive, 2008)
49
2.6.2 Finite Elements Model
The Finite Element Method (FEM) is a numerical analysis technique for obtaining
approximate solutions to engineering problems. In a continuum problem (e.g., one
that involves a continuous surface or volume) the variables of interest generally
posses infinitely many values because they are functions of each generic point in the
continuum. For example the stress in a particular element of pavement cannot be
solved with one simple equation because the functions that describe its stresses are
particular to each location. However, the finite element method can be used to divide
a continuum (the pavement volume) into a number of small discrete volumes in
order to obtain an approximate numerical solution for each individual volume rather
than an exact close-form solution for the whole pavement volume. Fifty year ago the
computations involved in doing this were incredibly tedious, but today computers
can perform them quite readily. In the finite element analysis of flexible pavements,
the pavement and subgrade is discretized into a number of elements with the wheel
load at the top of the pavement. The FEM assumes some constraining values at the
boundaries of the region of interest (pavement and subgrade) and is used to model
the nonlinear response characteristic of pavement materials. The FEM approach
works with more complex mathematical model than the layered elastic approach so
it makes fewer assumptions. Generally, FEM must assume some constraining values
at the boundaries of the region of interest.
2.7 Flexible Pavement M-E Distress Models (Failure Criteria)
The use of mechanistic approach requires models for relating the output from elastic
layered analysis (i.e stress, strain, or deflections) to pavement behaviour (e.g.
performance, cracking, rutting, roughness etc) as elastic theory can be used to
compute only the effect of traffic loads.
50
The main empirical portions of the mechanistic-empirical design process are the
equations used to compute the number of loading cycles to failure. These equations
are derived by observing the performance of pavements and relating the type and
extent of observed failure to an initial strain under various loads. Currently, two
failure criteria are widely recognized; one relating to fatigue cracking and the other
to rutting deformation in the subgrade. A third deflection-based criterion may be of
special applications (Pavement interactive, 2008). Most of the principles in
mechanistic-empirical design of highway pavements are based on limiting strains in
the asphalt bound layer (fatigue analysis) and permanent deformation (rutting) in
the subgrade.
2.7.1 Fatigue Failure Criterion
Fatigue cracking is a phenomenon which occurs in pavements due to repeated
applications of traffic loads. Accumulation of micro damage after each pass on a
bituminous pavements leads to progressive loss of stiffness and eventually, to
fatigue cracking. Repeated load initiate cracks at critical locations in the pavement
structure, i.e. the locations where the excessive tensile stresses and strains occur. The
continuous actions of traffic cause these cracks to propagate through the entire
bound layer. The fatigue criterion in mechanistic-empirical design approach is based
on limiting the horizontal tensile strain on the underside of the asphalt bound layer
due to repetitive loads on the pavement surface, if this strain is excessive, cracking
(fatigue) of the layer will result.
The cracks in the asphalt layer may initiate at the bottom of the layer and propagate
to the top of the layer, or may initiate at the top surface of the asphalt layer and
propagate downwards. In Practice pavements are subjected to a wide range of traffic
and axle loads, to account for the contribution of the individual axle load
applications, the linear summation technique known as Miner’s hypothesis (Miner’s
51
Law) is used to sum the compound loading damage that occurs, so that the total
damage can be computed as follows:
∑=
=i
i f
i
N
nD
1
(2.33)
Where,
D = Total cumulative damage
ni = Number of traffic load application at strain level i
Nf = Number of application to cause failure in simple loading at strain level i
This equation indicates that the determination of fatigue life is based on the
accumulative damage level D. Failure occurs when D > 1 and a redesign may be in
order. When D is considerably less than unity, the section may be under designed.
The relationship shows that pavement sections can fail due to fatigue after a
particular number of load applications (Oguara, 2005).
Studies carried out by various researchers have shown that the relationship between
load repetitions to failure Nf and strain for asphalt concrete material is given as:
Nf =
b
t
a
ε
1 (2.34)
Where
Nf = Number of load applications to failure
tε = Horizontal tensile strain at the bottom of asphalt
bound layer
a and b = Coefficients from fatigue tests modified to reflect
insitu performance
Various equations and curves have been developed based on this relationship. Pell
and Brown (1972) used the following in developing their fatigue curves:
52
Nf =
8.3
11 1108.3
−
t
xε
(2.35)
Figure 2.6 shows typical fatigue curves from Freeme et al for layered elastic analysis
(Freeme et al, 1982).
Many other equations have also been developed to estimate the number of
repetitions to failure in the fatigue mode for asphalt concrete. Most of these rely on
the horizontal tensile strain at the bottom of the HMA layer, εt and the elastic
modulus of the HMA. One commonly accepted criterion developed by Finn et al
(1977) is:
Log Nf =
−
−
− 36 10log854.0
10log291.3947.15 ACt Eε
(2.36)
Where,
Nf = Number of cycles to failure
εt = Horizontal Tensile Strain at the bottom of the HMA layer
EAC = Elastic Modulus of the HMA
The above equation defines failure as fatigue cracking over 10 percent of the wheel
path area.
Figure 2.6: Typical Fatigue Curves (Source: Oguara, 2005)
53
The Asphalt Institute (1982) developed a relationship between fatigue failure of
asphalt concrete and tensile strain at the bottom of the asphalt layer follows:
Nf 854.0291.3 )()(0796.0 −−= EItε (2.37)
Where,
Nf = Number of load repetitions to to prevent fatigue cracking
εt = Tensile Strain at the bottom of asphalt layer
EI = Elastic modulus of asphalt concrete (psi)
2.7.2 Rutting Failure Criterion
Permanent deformation or rutting is a manifestation of both densification and
permanent shear deformation of subgrade. As a mode of distress in highway
pavements, pavement design should be geared towards eliminating or reducing
rutting in the pavement for a certain period. Rutting can initiate in any layer of the
structure, making it more difficult to predict than fatigue cracking.
Current failure criteria are intended for rutting that can be attributed mostly to weak
pavement structure. This is typically expressed in terms of the vertical compressive
strain (εv) at the top of the subgrade layer as:
Nf =
4843.46
18 1010077.1
−
v
xε
(2.38)
Where,
Nf = Number of repetions to faulre
εv = Vertical compressive Strain at the top of the subgrade layer
The above equation defines failure as 12.5mm (0.5inch) depression in the wheel
paths of the pavement.
54
The relationship between rutting failure and compressive strain at the top of the
subgrade is represented by the number of load applications as suggested by Asphalt
Institute (1982) in the following form:
Nr 477.49 )(10365.1 −−= cx ε (2.39)
Where,
Nf = Number of load repetitions to limit rutting
εc = Tensile Strain at the bottom of asphalt layer
Rutting criterion is based on limiting the vertical compressive subgrade strain, if the
maximum vertical compressive strain at the surface of the subgrade is less than a
critical value, then rutting will not occur for a specific number of traffic loadings.
Presented in Table 2.9 are permissible vertical compressive subgrade strains for
various number of load applications by some agencies, Figure 2.7 shows 5 criterion
for limiting vertical compressive subgrade strain (Claessen et al, 1977). The Shell
criterion (Shell Criterion, 1977) corresponds to an average terminal rut depth of
13mm, whereas the Monismith and McLean criterion [Monismith and Mclean, 1971]
is based on a terminal rut depth of 10mm.
Table 2.9: Limiting Vertical Compressive Strain in Subgrade Soils by Various Agencies (Source: Oguara, 2005)
Number of load Repetitions to
Failure Nf
(10-6)
Original Shell
Model
(10-6)
Kentucky
(10-6)
TRRL
(10-6)
Chevron Model
(10-6)
Revised Shell
Model
(10-6)
California
(10-6)
103 2700 790 3122 2400 4979 2700
104 1680 639 1639 1400 2800 1680
105 1050 502 860 800 1575 1050
106 650 364 451 500 885 650
107 420 227 237 300 498 420
108 260 89 124 170 280 260
55
2.8 Layered Elastic Analysis Programs
A number of computer programs based on layered elastic theory (Burmister, 1945)
have been developed for layered elastic analysis of highway pavements. The
program CHEVRON (Warren and Dieckman, 1963) developed by the Chevron
Research Company is based on linear elastic theory. The program can accept more
than 10 layers and up to 10 wheel loads. Huang and Witczak (1981) modified the
program to account for material non-linearity and named it DAMA. The DAMA
computer program can be used to analyze a multi-layered elastic pavement structure
under single or dual-wheel load, the number of layers cannot exceed five. In DAMA,
the subgrade and the asphalt layers are considered to be linearly elastic and the
untreated subbase to be non-linear, instead of using iterative method to determine
Figure 2.7: Rutting Criteria by Various Agencies (Source: Oguara, 2005)
56
the modulus of granular layer, the effect of stress dependency is included by
effective elastic modulus computed according to equation (2.39)
E2 = 10.447h1-0.471h2-0.041E1-0.139E3-0.287K10.868 (2.40) Where, E1, E2, E3 are the modulus of asphalt layer, granular base and subgrade
respectively; h1, h2 are the thicknesses of the asphalt layer and granular base. K1 and
K2 are parameters for K-θ model with k2 = 0.5
ELSYM5 developed at the University of California for the Federal Highway
Administration Washington, is a five layer linear elastic program for the
determination of stresses and strains in pavements (Ahlborn, 1972). The program can
Analyze a pavement structure containing up to five layers, 20 multiple wheel loads.
The KENLAYER computer program developed based on Burmister’s elastic layered
theory by Yang H. Huang at the University of Kentucky in 1985, incorporates the
solution for an elastic multiple-layered system under a circular load. KENLAYER
can be applied to layered system under single, dual, dual-tandem wheel loads with
each layer material properties being linearly elastic, non-linearly elastic or visco-
elastic. It can be used to compute the responses for maximum of 19 layers with an
output of 190 points.
The WESLEA program was developed by U.S. Army Corps of Engineers. The
current version can analyze more than 10 layers with more than 10 loads.
The EVERSTRESS (Sivaneswaran et al, 2001) layered elastic analysis program
developed by the Washington State Department of Transportation at the University
of Washington, was developed from WESLEA layered elastic analysis program. The
program can be used to determine the stresses, strains, and deflections in a layered
elastic system (semi-infinite) under circular surface loads. The program is able to
analyze up to five layers, 20 loads and 50 evaluation points. The program can
57
analyze hot mix asphalt (HMA) pavement structure containing up to five layers and
can consider the stress sensitive characteristics of unbound pavement materials. The
consideration of the stress sensitive characteristics of unbound materials can be
achieved through adjusting the layer moduli in an iterative manner by use of stress-
modulus relationships in equations 2.40 and 2.41
Eb = K1θK2 for granular soils ( 2.41)
Es = K3σdK4 for fine grained soils (2.42)
Where,
Eb = Resilient modulus of granualar soils (ksi or MPa)
Es = Resilient modulus of fine grained soils (ksi or MPa)
θ = Bulk stress (ksi or MPa)
σd = (Deviator stress (ksi or Mpa) and
K1, K2, K3, K4 = Regression constants
K1, and K2, are dependent on moisture content, which can change with the seasons.
K3, and K4 are related to the soil types, either coarse grained or fine-grained soil. K2
is positive and K4 is negative and remain relatively constant with the season.
The BISAR program was developed by the Shell Oil Company. The program was
developed based on linear elastic theory. BISAR 3.0 can be used to calculate
omprehensive stress and strain profiles, deflections, and slip between the pavement
layers via a shearspring compliance at the interface.
The proposed LEADFlex Program differed from the other layered elastic analysis
procedures in that while the other programs are capable of carrying out layered
elastic analysis to determine pavement stresses, strains and deflections using trial
pavement thickness as one of the inputs, the LEADFlex program is a comprehensive
58
program that is capable of computing pavement thickness and predict fatigue and
rutting strains in the asphalt pavement. In the final analysis, the program determines
adequate pavement thicknesses that will limit fatigue cracking of asphalt layer and
permanent deformation of subgrade, hence limit pavement failure.
2.9 Validation with Experimental Data
An appreciable amount of work has been performed to validate proposed models
with experimental data. Researchers Ullidtz and Zhang (2002) calculated
longitudinal and traverse strains at the bottom of asphalt, and vertical strains in the
subgrade using layered elastic theory, method of equivalent thickness, and finite
element methods. The authors assert various degrees of agreement between the
computed values and values from the Danish Road Testing Machine. They stated
that the critical factor is treating the subgrade as a non-linear elastic material.
Another study by Melhem and Sheffield (2000) carried out full instrumentation of
several pavement sections at three(3) stations at the South (SM-2A) and North (SM-
2A) lanes of the Kansas Accelerated Testing Laboratory (K-ATL). Tensile strains at
the bottom of the asphalt layer and compressive strains at the top of the subgrade
were calculated using ELSYM5 based on the multi-layer elastic theory while the
measured strains were determined using strain gauges. The relationship between
measured and calculated strains under FWD loading was compared using linear
regression analysis. The result indicated that coefficient of determination was very
good and concluded that the multilayer elastic theory for asphalt pavement is a good
estimator of pavement responses.
A significant study by Huang, et al. (2002) presented the results of various numerical
analyses performed with various structural models, both two and three dimensions
and considering both static and transient loading. Their calculated values were
compared to experimental values from the Louisiana Accelerated Loading Facility
59
(ALF) from three asphalt test values. The Authors concluded stress and strain
responses obtained with the three-dimensional finite element program ABAQUS
with rate-dependent viscoplastic models for the asphalt and elastoplastic models for
the other layers were close to experiment values.
Work done by the Virginia Tech Transportation Institute (Loulizi, et al., 2004)
compared measured pavement responses using layered linear elastic analysis subject
a single tire and one set of dual tires. The authors used several elastic layer programs
and two finite element approaches. They concluded that responses were
underestimated at high temperatures, but overestimated at low intermediate
temperatures. They recognized the need for more research considering dynamic
loading, layer bonding, and anisotropic material properties.
Pavement responses of horizontal tensile and vertical shear strains in the asphalt
layers were of interest in a study authored by Elseifi, et al. (2006). The field-
measured responses from the Virginia Smart Road were compared against finite
element predicted response incorporating a viscoelastic model using laboratory-
determined parameters. In addition, dimensions and vertical pressure measurements
of each tire tread were used in the simulation. The authors claim an average
predictions error of less than 15% between the calculated and field response values,
and concluded elastic models under-predict pavement response at intermediate and
high temperatures.