deformation behaviour of chromium sheets in mechanical and laser bending
TRANSCRIPT
Deformation behaviour of chromium sheets in mechanicaland laser bending
K.C. Chana,*, Y. Haradab, J. Lianga, F. Yoshidac
aDepartment of Manufacturing Engineering, The Hong Kong Polytechnic University, Hung Hom, Kowloon, Hong KongbDepartment of Production Systems Engineering, Toyohashi University of Technology, Toyohashi, Japan
cDepartment of Mechanical Engineering, Hiroshima University, Higashi-Hiroshima, Japan
Received 4 June 2001
Abstract
Chromium is known to have limited room-temperature ductility but to exhibit apparent ductile-to-brittle transition behaviour at
temperatures ranging from 150 to 300 8C. In this paper, the deformation behaviour of a chromium sheet was investigated in roll-compression
and laser bending. Tensile tests and three-point bending tests were performed also to determine the basic mechanical properties of the
chromium sheet. The ductile-to-brittle transition temperature of the chromium determined by the tensile test was found to be 180 8C. While
the sheet could be bent to 908 at a temperature of 130 8C in three-point bending, it was possible to bend the sheet to the same bending angle
at a lower temperature (100 8C) in roll-compression bending, the presence of compressive stress in roll-compression bending being
considered to be the reason for the difference in the temperatures. A finite element stress analysis was also conducted to reveal the stress
distribution of the chromium sheet in roll-compression bending. Laser bending was demonstrated to be a possible process to deform
chromium sheets. A threshold laser power of 40 W is observed, below which bending is unlikely to occur. The bending angle was found
to increase with increasing laser power and number of irradiations, and decreasing scanning velocity. # 2002 Elsevier Science B.V.
All rights reserved.
Keywords: Chromium sheet; Ductile-to-brittle transition; Three-point bending; Laser-bending
1. Introduction
Chromium exhibits apparent ductile-to-brittle transition
behaviour at temperatures ranging from 150 to 300 8C.
Below this range, plastic deformation is virtually impossi-
ble. Even if plastic deformation of chromium can be accom-
plished at high temperatures, the induced tensile residual
stress will make the material of brittle nature at room
temperature. These are the main reasons why chromium
is rarely used as a bulk materials in industry, despite its high
corrosion and heat resistance. There have been research
efforts made to improve the mechanical properties and
workability of chromium [1–12]. It has been found that
the ductile-to-brittle transition temperature (DBTT) can be
lowered by: (i) using high purity chromium in which dis-
location locking is unlikely to occur [1–3]; (ii) deforming
the chromium at a low forming speed [4,5]; (iii) introducing
a small amount of plastic prestrain [1,5]; and (iv) applying
high hydrostatic pressure [6–9]. Ohmori et al. [10–12] have
recently reported that for some forming processes which
apply compressive stress such as rolling, upsetting and extru-
sion, chromium workpieces were successfully deformed
without any failure at a relatively low temperature.
The present paper reports the deformation behaviour of
chromium examined by two different techniques, namely
mechanical and laser bending. Laser bending is shown to be
particularly suitable for one-off or small batch production
and the shaping of hard and brittle materials, as no hard
tooling is required. In the process, repetitive irradiations of a
defocused laser beam are applied over the surface of metal
sheets [13,14]. Because of the development of a temperature
gradient across the sheet thickness, thermal stress is induced
and permanent deformation is produced. Chan and Liang
[15,16] have recently examined the deformation behaviour of
aluminium matrix based composites and Ti3Al-based inter-
metallic alloy. They have demonstrated that it is possible
to bend relatively brittle materials to large angle by laser
bending. For mechanical bending, roll-compression bending
is selected, in which a high roll-contact pressure is applied on
chromium sheets by using a roller-punch and a roller-die.
Journal of Materials Processing Technology 122 (2002) 272–277
* Corresponding author. Tel.: þ852-2766-4891; fax: þ852-2362-5267.
E-mail address: [email protected] (K.C. Chan).
0924-0136/02/$ – see front matter # 2002 Elsevier Science B.V. All rights reserved.
PII: S 0 9 2 4 - 0 1 3 6 ( 0 2 ) 0 0 0 1 4 - 6
2. Experimental material and procedures
A chromium plate of 2.5 mm thickness produced by
powder metallurgy was investigated in the paper, its che-
mical composition being shown in Table 1.
Fig. 1 presents a schematic illustration of the experimental
set-up for roll-compression bending. The bending load is
servo-controlled. In the experiments, chromium sheets were
bent using a roller-punch and a rotating die in an oil bath at
temperatures ranging from 50 to 150 8C. In order to examine
the temperature dependence of the flow stress and ductility
of chromium, tensile tests were performed in vacuum at
various temperatures in an Instron testing machine with a
cross-head speed of 10 mm/min. Three-point bending tests
were also carried out in air in order to obtain the basic
bending properties of the chromium. A schematic diagram
of the three-point bending test is shown in Fig. 2.
For laser bending, samples of thickness of 0.5 mm and
dimensions of 10 mm � 20 mm were prepared by wire
electro-discharge machining. An 80 W YAG laser unit
operating in continuous wave (CW) mode was used in the
experiments to scan the specimens with laser powers of 48
and 68 W, scanning velocities ranging from 10 to 25 mm/s,
and the number of irradiations being from 10 to 50. No time
was allowed between two successive irradiations and the
laser was scanned back and forth along the same path in
multiple irradiations. An image processing system was used
to measure the bending angle to an accuracy of �0.58. No
graphic coating was applied and a defocused laser beam with
a diameter of 1.3 mm was used to avoid surface melting. The
experimental set-up is described in Ref. [14].
3. Results
3.1. Tensile and three-point bending tests
Fig. 3 shows the nominal stress vs. nominal strain curves
of chromium sheets tested at temperatures of 120, 150, 180
and 200 8C. It is found that chromium is relatively brittle at
temperatures of below 180 8C. The relationship between
fracture strain (defined as ef ¼ lnðA0=AfÞ, where A0 and Af
are cross-sectional areas of initial and fractured specimens,
respectively) and temperature under tensile tests is shown in
Fig. 4. The temperature dependence of the maximum (non-
dimensional) curvature k (t0/r, where t0 denotes the initial
thickness of the specimen and r the radius of the mid-plane
of the bent plate) obtained in three-point bending tests is
shown in Fig. 5. At temperatures of above 130 8C, the
specimens can be successfully bent up to an angle of 908,at which the curvature k is 0.35.
The ductile-to-brittle transition behaviour of chromium
can be explained by the concept of brittle fracture stress sfrac
Table 1
Chemical composition of the chromium specimens (wt.%)
C P S Fe H O N Cr
0.004 0.002 0.003 0.130 0.0004 0.006 0.008 Balance
Fig. 1. Schematic illustration of roll-compression bending (dimensions: mm).
Fig. 2. Schematic diagram of three-point bending (dimensions: mm).
K.C. Chan et al. / Journal of Materials Processing Technology 122 (2002) 272–277 273
[17], which states that for a tensile stress greater than sf, the
material fractures in a brittle manner. If plastic flow is
assumed to occur independently of brittle fracture at a flow
stress sflow, the fracture is brittle when sfrac is smaller than
sflow, and the fracture is ductile when sfrac is larger than
sflow. Using the experimental results of the tension test, sfrac
is determined as 310 MPa (true stress). Since sflow
decreases rapidly with temperature, and sfrac is almost
temperature independent, a sharp ductile-to-brittle transi-
tion occurs in chromium. It is interesting to note that
in three-point bending, chromium can be successfully bent
up to 908 at a temperature of 130 8C, which is much lower
than the DBTT of 180 8C determined by the tensile test. It
is considered that the difference in temperature is because
the strain achieved in bending is much smaller than that in
tensile test. Based on simple calculations, the maximum
surface strain of the sheet bent to 908 is 0.16. According to
Fig. 3, this amount of strain can be achieved in tensile test at
a temperature of 130 8C.
3.2. Roll-compression test
Fig. 6 shows the experimental results for roll-compression
bending. It has been demonstrated that it is possible to bend
chromium to a degree of 908 at a rather low temperature of
100 8C, which is smaller than the temperature of 130 8Cobtained in three-point bending. The presence of compres-
sive stress in the process is considered to be the reason for
the difference in temperature. It is also found that only under
a certain level of compressive load bending of chromium is
possible, and that the load is temperature-dependent.
Although compressive stress is beneficial in the forming
of chromium, a very large compressive load will result in
early stage fracture, as shown in Fig. 6. In order to under-
Fig. 3. Nominal-stress vs. nominal-strain curves in tension tests on chromium at various temperatures.
Fig. 4. Fracture strain ef vs. test temperature in tension tests on chromium.
274 K.C. Chan et al. / Journal of Materials Processing Technology 122 (2002) 272–277
stand this phenomenon, a finite element stress analysis
was conducted using the FE code ABAQUS [18]. The
plane-strain condition was assumed in the analysis. The
relationship between the effective stress and the effective
plastic strain was given by the equation:
s ¼ 125 þ 386e0:41 MPa
that was determined from the stress–strain curve obtained at
180 8C. Young’s modulus and Poisson’s ratio were assumed
as 250 GPa and 0.3, respectively. The calculated stress
distribution (longitudinal stress) in roll-compression bend-
ing under 10 kN compression is illustrated in Fig. 7, where a
large tensile stress of over 267 MPa is found in the vicinity
of the punch-contact area. This could be the reason for early
stage fracture of the specimen under a large punch load.
3.3. Laser bending
Fig. 8 shows the relationship between the laser bending
angle (a) and the number of irradiations (N). It has been
demonstrated that it is possible to bend chromium sheets
Fig. 5. Maximum non-dimensional curvature k vs. test temperature in three-point bending on chromium (k ¼ t0=r, where t0 is the initial thickness of the
specimen (2.5 mm) and r the minimum radius at middle surface of the specimen. Symbols (~) and (~) show the results for successfully bent and fractured
specimens, respectively).
Fig. 6. Maximum non-dimensional curvature k vs. compressive load in roll-compression bending at various temperatures (open symbols (&) and (*) and
filled symbols (&), (*) and (~) show the results for successfully bent and fractured specimens, respectively).
K.C. Chan et al. / Journal of Materials Processing Technology 122 (2002) 272–277 275
using multiple irradiations and low laser powers. The bend-
ing angle is found to increase linearly with increasing
number of irradiations. A similar phenomenon has been
observed with other materials [15,16]. Fig. 9 shows the a–N
curve of the chromium at a constant power of 68 W and at
laser scanning velocities of 10 and 20 mm/s. At a small
number of irradiations, the bending angles obtained at
the scanning velocity of 10 mm/s are significantly larger
than those for 20 mm/s. The difference is reduced when the
number of irradiations is increased. It is considered that the
effect of the scanning velocity is reduced when the number
of irradiations is large. The effect of scanning velocity on
bending angle is also illustrated in Fig. 10. It is found that the
bending angle decreases with an increase in the scanning
velocity. At a power of 48 W, the bending angle drops more
rapidly at high velocities, which is considered to be related
to the total laser energy applied to the sheet. Fig. 11 shows
the effect of the laser input power on the bending angle of
the chromium sheet at a number of irradiations of 30. A
threshold laser power of about 40 W is observed, below
which bending is unlikely to occur. The laser bending angle
increases with increasing laser power, but at high powers the
rate of change in bending angle becomes less. A temperature
gradient is formed across the sheet thickness in laser bending.
If the temperature gradient is too small because of inap-
propriate setting of the processing parameters, such as too
low an input power, no or small bending angles are observed.
Fig. 7. Distribution of longitudinal stress in roll-compression bending
under 10 kN compression.
Fig. 8. a–N curves at different laser powers.
Fig. 9. a–N curves at different laser scanning velocities.
Fig. 10. Influence of the laser scanning velocity on the bending angle.
276 K.C. Chan et al. / Journal of Materials Processing Technology 122 (2002) 272–277
Although, laser bending is shown to be feasible for
chromium sheet, it is worthwhile to examine the stress state
of the sheet during bending. In laser bending, thermal
expansion occurs at the upper surface of the sheet during
heating, which leads to an intermediate bending stage called
‘‘reverse bending’’. The reverse bending angle is related to
the amount of thermal expansion of the upper layer of the
sheet and a substantial compressive stress arises in this layer.
Being bent away, the bottom layer is also subjected to
compressive stress. During cooling, thermal contraction
occurs at the upper layer as there is heat lost by conduction.
The sheet will then be bent towards the laser beam, which is
called ‘‘positive bending’’. Since the amount of reverse
bending is much smaller than that of positive bending, an
overall positive bending angle is observed after cooling.
However, during positive bending, the stress at the heat
zone will change from compression to tension, which is
not beneficial for large deformation of chromium sheets.
As compared to roll-compression bending, laser bending
is considered to be a powerful and cost effective means to
deform chromium sheets at small strain or in the making
prototypes. Roll-compression bending is a more appropriate
process for large deformation or for making chromium
components, although it involves tooling cost and the pro-
cessing temperature is still around 100 8C. More research is
needed to improve this process so that it can deform
chromium sheets at an even lower processing temperature.
4. Conclusions
Chromium sheets are shown to be able to be deformed
by roll-compression and laser bending. In roll-compression
bending, the sheet can be bent to 908 without fracture at a
temperature of 100 8C. This temperature is significantly
lower than the ductile-to-brittle transition temperature
(180 8C) determined by the tensile test, and is also lower
than the minimum temperature at which the sheet can be
bent to the same bending angle in conventional three-point
bending. The presence of compressive stress in roll-com-
pression bending is considered to be advantageous in the
bending of chromium sheet. However, a finite element stress
analysis reveals that a very large compressive stress, which
will result in a large longitudinal tensile stress, is harmful to
the process and leads to early stage fracture. Laser bending is
also demonstrated to be able to deform chromium sheets
using multiple irradiations and low laser power. At a laser
power of 68 W, a maximum bending angle of 23.58 is
obtained at a scanning velocity of 10 mm/s, and at a number
of irradiation of 50. The laser bending angle is found to
increase with an increase in input power and in the number
of irradiations, and with a decrease in scanning velocity. It is
considered to be very worthwhile to further examine the
deformation behaviour of chromium sheet using a high
power laser which may enable the sheet to be deformed
to a large strain level with a lesser number of irradiations.
Acknowledgements
The work described in this paper was partly supported by
a grant from the Research Grant Council of the Hong Kong
Special Administration Region (Project No. PolyU 5166/
97E).
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K.C. Chan et al. / Journal of Materials Processing Technology 122 (2002) 272–277 277