development of a forming limit diagram for a fibre …
TRANSCRIPT
Mechanics of Nano, Micro and Macro Composite Structures Politecnico di Torino, 18-20 June 2012
A. J. M. Ferreira, E. Carrera (Editors)
http://paginas.fe.up.pt/~icnmmcs/
DEVELOPMENT OF A FORMING LIMIT DIAGRAM FOR A FIBRE
METAL LAMINATE BASED ON A GLASS FIBRE REINFORCED
POLYPROPYLENE COMPOSITE
A. Sexton*, W.J. Cantwell
†, S. Kalyanasundaram
*
* Research School of Engineering
Australian National University
North Road, Canberra 0200, Australia
e-mail: [email protected], web page: http://cecs.anu.edu.au
† Centre for Materials and Structures
University of Liverpool
L69 3BX Liverpool, United Kingdom
e-mail: [email protected], web page: http://www.liv.ac.uk/
Key words: Composite structures, Fibre metal laminate, Experimental mechanics,
Formability.
Summary. This paper investigates the forming behaviour of a fibre metal laminate based on
aluminium and a glass fibre reinforced polypropylene composite at room temperature.
Specimens of varying geometry are stretched over a hemispherical punch to elucidate the
deformation behaviour of the laminate in several forming modes. An optical strain measuring
system is used to obtain the surface strain of the specimens throughout the forming process.
These results are compared to the forming of aluminium and a forming limit curve for the
fibre metal laminate is developed. One of the major conclusions from this study is that it is
possible to manufacture fibre metal laminates containing glass fibre composites using
forming techniques generally restricted to more ductile materials such as metals.
1 INTRODUCTION
Evidence of anthropological climate change is fuelling research into advanced materials.
These advanced materials are primarily of interest to the transport industry in an attempt to
reduce the fuel consumption and therefore emissions of aircraft and vehicles. According to the
International Energy Agency (2011), the transport sector is currently responsible for 23% of
energy-related CO2 emissions and it is expected that the transport sectors of emerging
economies will drive all net growth in demand for oil. This means that significant reductions
in greenhouse gas emissions can be achieved by targeting the transport industry for
improvement; alternative fuel, improved engine efficiency and reduction of the vehicle's
weight are some of the methods proposed to reduce fuel consumption. Reducing the weight of
vehicles is seen as a precursor for further improvements in efficiency through the principal of
mass decompounding [1]. Innovative design, which involves the optimisation of components
A. Sexton, W.J. Cantwell and S. Kalyanasundaram.
2
to attain higher performance from existing materials, and material substitution, where the
existing material is replaced by a higher performance material are two of the major methods
proposed for mass reduction. In addition to material substitution using alternative metals,
polymer composite materials are also gathering interest. Composite materials have both
advantages and disadvantages with respect to vehicle manufacture; they exhibit superior
specific strength and stiffness than steel but are prohibitively expensive for rapid production
of vehicles. However, the mass reduction using composite materials has been estimated at 20-
35% and 40-65% using glass-fibre and carbon-fibre reinforced composite materials
respectively [2]. Traditionally, thermoset composite materials were used in the production of
components for both automotive and aerospace applications; however, these materials suffer
from long and expensive manufacturing procedures which restrict their use to low volume
applications. The advent of low cost thermoplastic composite materials has led to the study of
the applicability of existing low cost rapid manufacturing techniques, unavailable to
thermoset composites, to thermoplastic composites.
Fibre Metal Laminate (FML) systems are a composite material consisting of alternating
layers of fibre-reinforced composite and metal. The first generation of FML systems utilised
an aramid fibre reinforced thermoset composite called ARALL. This FML system was
developed in the 1970s by TU Delft and Fokker and studies on F-27 wing panels comprised
of this material showed great promise. A reduction in weight of 25% was achieved while
maintaining strength, and loads which would cause failure in monolithic aluminium caused
only minor damage in the FML [3]. However, it was found that the blunt notch strength of the
ARALL FML was critical and premature fatigue cracks appeared at doublers which were
bonded to increase strength. Other deficiencies were also found in the ARALL FML systems,
such as poor bonding between the aramid fibres and matrix material, moisture absorption and
failure of the fibre/matrix interface and fibre failure under tension-compression fatigue
loading [4]. These problems led to the development of FML systems such as GLARE, which
contains a glass-fibre reinforced thermoset composite. Studies showed that the GLARE FML
was not only less expensive than the ARALL FML but also resulted in greater weight
reductions and had superior fatigue resistance. This culminated in the use of GLARE in the
Airbus A380 upper fuselage where it has been shown to possess excellent impact and damage
tolerance properties. The disadvantage of these FML systems is that they utilise thermoset
polymers for the matrix material and suffer from the manufacturing difficulties inherent to
these materials. Thermoplastic polymers offer the ability to form preconsolidated sheets of
material with a manufacturing time comparable to metals. This would allow the use of FML
systems in rapid manufacturing applications.
The most commonly used method for the rapid manufacture of components from sheet
material is stamp forming. Sheet metal forming is a widely used manufacturing process in the
automotive industry which uses a die, blankholder and punch to rapidly create complex
components. Extensive research into the formability of metallic materials led to the
development of the Forming Limit Diagram (FLD) by Keeler and Backofen [5]. The FLD is
used to visualise the state of strain of the surface of a formed part and to evaluate the
A. Sexton, W.J. Cantwell and S. Kalyanasundaram.
3
performance of that material in a stamp forming process. The Forming Limit Curve (FLC) is a
limit on the FLD that defines the transition between safe states of strain and failure. The
failure of metals is determined by the onset of localised necking, therefore the FLD consists
of three regions, the safe region, the necked region and the failed region. A FLD with these
regions is shown in figure 1. However, studies by Morrow et al. [6] showed that certain
composite materials do not exhibit localised necking before failure.
Figure 1 – Forming limit diagram with three regions
Increased interest in composite materials for use in automotive applications has led to
increased research into the formability of thermoplastic composites. Lee et al. [7] and
Venkatesan et al. [8, 9, 10] determined that, by choosing optimal conditions for punch speed
and forming temperature, composites can exhibit formability comparable to metals. Cabrera et
al. [11] investigated the stamp forming of all polypropylene and glass-fibre reinforced
polypropylene composites and found that stretch forming is more desirable than draw forming
because the latter leads to higher forming energy and residual stresses. Recently, studies on
the formability of fibre metal laminates by Mosse et al. [12-15], Gresham et al. [16] and
DharMalingam et al. [17] have shown that it is possible to form FML systems using draw
forming under carefully controlled process parameters. These studies found that lower
blankholder forces and higher temperatures resulted in increased severity of wrinkling in the
flange and sidewall, whereas higher blankholder forces lead to tearing and fracture. Reyes and
Kang [18] performed preliminary investigations into the stretch forming of fibre metal
laminates and found that the deformation was comparable to aluminium of similar thickness
whilst requiring 25% less load. Previous studies by Sexton et al. [19] investigated the
deformation behaviour of a FML based on a self-reinforced polypropylene composite. This
study found that the FML exhibited a greater strain at failure and an increased forming
window. In addition, it was found that the FML system displayed a more even thickness
distribution compared to a similarly formed metal part.
This study evaluates the formability of a fibre metal laminate based on a glass-fibre
reinforced polypropylene composite using a real time photogrammetric strain measurement
system. The aim is to investigate and analyse the evolution of strain to failure and to develop
a FLD and FLC for the FML system. These results will then be compared to the formability
of aluminium specimens of similar geometry.
A. Sexton, W.J. Cantwell and S. Kalyanasundaram.
4
2 EXPERIMENTAL WORK
2.1 Materials and Laminate Preparation
The FML system investigated in this study comprises a glass-fibre reinforced
polypropylene composite, Twintex from OCV Reinforcements, and a 5005-O aluminium
alloy in a 2/1 configuration. This means that one 1mm thick composite layer was sandwiched
between two layers of 0.6mm aluminium. Two layers of a 50μm thick hot-melt polypropylene
film adhesive were used to bond the composite and aluminium to achieve a final thickness of
2.2mm for the FML. Adequate adhesion between the materials was ensured through
preparation of the bonding surfaces; the surface of the aluminium was etched in a 5% NaOH
solution for 5 minutes and the surfaces of the adhesive and composite were cleaned using
isopropyl alcohol.
The laminate stacking arrangement is illustrated in figure 2. Laminates of 230mm by
240mm were placed in a hydraulic press and heated to 155°C. Once the temperature was
achieved, a pressure of 1MPa was applied for 5 minutes after which the laminate was rapidly
water cooled. After bonding of the FML, the desired experimental geometries were obtained
using water jet cutting.
Figure 2 - Laminate stacking arrangement
2.2 Experimental Design
Seven specimens of varying width, shown in figure 3a, are stretched over a hemispherical
punch using the method developed by Hecker [20] to obtain all deformation conditions. The
widths used were 25, 50, 75, 100, 125, 150 and 200mm. These widths were chosen as they
provided a large number of specimens for the maximum possible width. Varying the width of
a specimen which is stretched over a hemispherical punch alters the lateral constraint on the
specimen. This means that, for specimens of reduced width, the sides of the specimen are not
subjected to high levels of stretch and are instead allowed to partially “draw” into the die,
which will lead to more negative values of minor strain. This effect is shown in figure 3b.
Using this method, the failure limit of the material can be found for deformation modes
ranging from uniaxial tension to biaxial stretch.
A. Sexton, W.J. Cantwell and S. Kalyanasundaram.
5
(a)
(b)
Figure 3 - Examined experimental specimens (a) and the effect of specimen geometry on the deformation
behaviour (b)
2.3 Evaluation of formability
A custom designed 300kN stamp press with a 100mm diameter hemispherical punch and
105mm open die, shown in figure 4a, was used to evaluate the forming of the fibre metal
laminate. A local data acquisition PC controls the feed rate and punch displacement. A
compression load cell measured the punch force and a linear potentiometer provided the
punch displacement. The experiments were conducted at a feed rate of 10mm/s and the depth
at failure was determined by a 2% drop from maximum load. A universal lubricant was used
to reduce friction between the punch and the samples. The formability of the fibre metal
laminate is assessed using the evolution of strain and the strain at failure on the surface of the
laminate. These results will be used to develop a forming limit diagram for the material and to
determine a safe forming limit under different deformation conditions. An open die is used to
facilitate measurement of the strain on the surface of the material throughout the forming
process using the ARAMIS strain measurement system, shown in figure 4b.
(a) (b)
Figure 4 - Experimental specimens (a) and the ARAMIS strain measurement system (b)
A. Sexton, W.J. Cantwell and S. Kalyanasundaram.
6
3 RESULTS AND DISCUSSION
3.1 Deformation Modes
The ARAMIS strain measurement system allows determination of the strain for every
point on the surface of the material. This allows the analysis of the strain at identified points
of interest such as regions of high strain, low strain and regions where failure occurs.
Figure 5 shows the evolution of surface strain at the pole of both the FML and aluminium
experimental specimens. These figures elucidate the theory that by altering the geometry of
the specimen it is possible to obtain the different deformation modes. The figures also
highlight three distinct behaviours in the evolution of surface strain at the pole;
• the pre-stretch region,
• initial biaxial stretch, and
• strain path to failure
The pre-stretch behaviour is caused by the lock ring used to securely clamp the specimen
and to prevent drawing of material into the die. The lock ring causes this stretch due to the
bend-unbend it introduces into the specimen. The blankholder force is controlled by six bolts
which are all tightened to the same torque. However, it was found that lower torques were
required for the smaller specimens compared to the larger specimens due to the possibility of
failure at the lock ring. The strain introduced into the specimens as a result of securing the
lock ring was obtained by taking the initial image of the specimen prior to the application of
blankholder force. Therefore, the state of zero strain indicated in the results corresponds to a
completely unloaded specimen.
(a)
(b)
Figure 5 - Evolution of the surface strain at the pole of the experimental FML (a) and aluminium (b) specimens
The deformation behaviour at the pole of the specimens following the pre-stretch is a
region of biaxial stretch. This behaviour is caused by the shape of the punch. In the initial
stages of contact between the punch and the specimen only the region in contact with the
punch deforms. Therefore, for a hemispherical punch, the pole region of the specimen will
A. Sexton, W.J. Cantwell and S. Kalyanasundaram.
7
exhibit a deformation mode consistent with biaxial stretch. At a depth of approximately 3-
5mm the strain behaviour again changes. Figure 6 elucidates the nature of the change in
deformation behaviour at this depth which is caused by a change in the evolution of the minor
strain. This change occurs due to the reduced width of the experimental specimens in the
lateral direction which means that after a certain depth there is no more material in that
direction to allow biaxial stretch.
Figure 6 - Evolution of the minor strain in the FML specimens with increasing forming depth
The strain path to failure allows the determination of the strain ratio in the specimens,
which can be used to identify the approximate deformation mode experienced by each
specimen. These strain ratios are shown in table 1.
(a)
Specimen 25mm 50mm 75mm 100mm 125mm 150mm 200mm
Strain Ratio (β) 0.24 -0.06 -0.19 0.01 0.25 0.42 0.9
(b)
Specimen 25mm 50mm 75mm 100mm 125mm 150mm 200mm
Strain Ratio (β) -0.43 -0.2 -0.07 0 0.27 0.6 1
Table 1 - Strain ratio for the FML (a) and aluminium (b) experimental specimens
It can be seen from both figure 5 and table 1 that the FML specimens exhibit vastly
different strain ratios to aluminium specimens of similar geometry. The aluminium specimens
show the validity of using specimens of varying width as proposed by Hecker. The 25mm
aluminium specimen exhibits a strain ratio which is close to the ratio used to define uniaxial
tension, the 100mm specimen deforms in the plane strain mode and the 200mm specimen
displays balanced biaxial stretch. The other aluminium specimens allow the analysis of the
range between these deformation modes. The different behaviour of the FML is more
pronounced in the 25, 50 and 75mm specimens. Instead of demonstrating the range from
uniaxial tension to plane strain, as shown by the equivalent aluminium specimens, there
appears to be no discernible pattern in the strain ratio and deformation behaviour. The
behaviour displayed by the 75mm specimen is of particular interest as it does not follow the
same trend as any of the other FML specimens. In addition to this it also exhibits different
strain behaviour compared to the aluminium specimen. A reason for this behaviour could be
A. Sexton, W.J. Cantwell and S. Kalyanasundaram.
8
caused by delamination of the specimen during the forming process as shown in figure 7. The
75mm specimen was the only specimen in which delamination was observed.
Figure 7 - Delamination occurring in the 75mm specimen
The difference in the strain state at failure is due to the aluminium specimens deforming to
a greater depth than the FML specimens. However, this depth does not consider the
aluminium experiencing localised necking in the regions surrounding the punch. In metal
forming studies a material which has commenced localised necking is considered to be failed
because this rapidly leads to material fracture [21], therefore this data alone cannot be used to
determine the depth at failure or the state of strain which causes failure in either of the
material systems. Further analysis of the specimens was undertaken to determine the depth of
failure and the state of strain at the region that failed first.
Figure 8 shows the forming limit diagram for the experimental geometries. These figures
show the overall strain behaviour of the FML and aluminium specimens. It can be seen that
the FML behaviour is not only different at the pole but the strain ratios for all visible points
exhibit differences. The FML specimens appear to partially behave like the monolithic
aluminium but are restricted from the peaked levels of major strain which is apparent in the
aluminium specimens. The highlighted region in figure 8b shows the peaked major strain.
This peaked behaviour occurs in regions to the side of the pole.
Figure 8 - Forming limit diagrams for the FML (a) and aluminium (b) specimens
The evolution of the strain at the pole of the FML specimens shows that the specimens can
exhibit deformation behaviour from plane strain to biaxial stretch. The 100mm and 200mm
specimens, which most accurately represent these deformation modes, were therefore chosen
for further comparison of the surface strain with aluminium. In addition, the 25mm FML
Region of peak strain
A. Sexton, W.J. Cantwell and S. Kalyanasundaram.
9
specimen was also selected for comparison as the aluminium specimen reflected the
behaviour of uniaxial tension.
3.2 Strain Evolution
The meridian major strain on the surface of selected FML and aluminium specimens is
shown in figure 9. This information is useful for determining the points at which failure will
occur in specimens as the strain in certain regions will increase more rapidly than other areas
and therefore fail earlier. The evolution of the strain on the surface of the experimental
specimens was captured for every millimetre of forming depth.
(a)
(b)
(c)
Figure 9 - Meridian strain distribution for the experimental specimens exhibiting the uniaxial tension (a), plane
strain (b) and biaxial stretch (c) deformation modes. FML and aluminium strain distributions are on the left and
right respectively
Figure 9 shows the meridian strain distribution along a section through the specimen for
A. Sexton, W.J. Cantwell and S. Kalyanasundaram.
10
the 25mm, 100mm and 200mm specimens at depth increments of 5mm up until failure in the
FML specimens. The section chosen was oriented along the longitudinal axis of the
specimens, which also corresponds with the fibre direction in the composite material. In these
distributions, the centre of the specimen occurs at approximately 50mm along the section and
the edges of the die are at the 0 and 100mm distances. These distributions show that FML
specimens show a slightly more uniform strain distribution than the aluminium specimens.
This is advantageous to the forming of parts as it corresponds to a more even thickness
distribution. However, compared with the meridian strain distribution of a FML based on a
self-reinforced polypropylene composite [19] it can be seen that the stiffer glass fibres and the
single lamina nature of the composite do not allow as much distribution of the strain in the
aluminium layer.
Figure 9a shows the strain distribution for the 25mm specimens. This figure shows the
FML specimen failing at a depth of 18.9mm. This was then compared to the observed onset of
localised necking in the aluminium specimen, which was found to occur at 23.5mm. Figure
9b shows the meridian strain for the 100mm FML and aluminium specimens. In this case the
failure depths of the FML and the aluminium respectively were 21.2mm and 19.6. The
localisation of strain in aluminium specimens, prior to localised necking, can be seen
occurring to the side of the pole region. This is not yet the localised necking which precedes
failure but the increase in strain in these regions shows that the aluminium specimens can very
rapidly lose quality during forming. The 200mm specimens show that, for equivalent forming
depths, the FML and aluminium specimens show approximately the same strain at the pole. It
can be seen, however, that the regions surrounding the pole in the aluminium specimens are
increasing at a faster rate than the pole. This behaviour, even prior to necking, lowers the
quality of the formed part by causing an uneven thickness distribution across the surface of
the part.
3.3 Failure of the experimental specimens
The failure of the experimental specimens was dependent on the specimen geometry. The
larger specimens such as the 100, 125, 150 and 200mm specimens displayed failure which
was visible to the optical measurement system. Similar to metals, the failure occurred in the
region to the side of the pole and along the longitudinal axis. It was observed, however, in the
200mm specimen that failure occurred in both the warp and weft fibre directions leading to
the conclusion that the failure of the laminate was precipitated by fibre breakage. Supporting
this assertion is that, contrary to previous studies on the forming of composite and FML
systems [6, 19], this study found that some localised necking appeared in the FML specimens
prior to the appearance of a tear. The appearance of a neck immediately before tearing
supports the failure of the composite layer. This is because there was no localisation of strain
in this region, compared to the other regions, before the observation of the localised neck.
Figure 10 shows the final three images of the surface of a FML specimen before failure.
These figures show the rapid evolution of a neck to failure in the FML. In the time between
the first and second images, a fraction of a second, the fibres in the composite layer have
A. Sexton, W.J. Cantwell and S. Kalyanasundaram.
11
failed which transfers the entire load to the aluminium layer and causes it to neck and
subsequently tear.
Figure 10 - Appearance of localised neck prior to failure
However, as shown in figure 11, the 25mm and 50mm specimens experienced failure at the
lock ring. Therefore, the development of the FLC from these specimens was determined by
using the pole as a safe point and the regions to the side of the punch as marginal points. This
ensures that no point which might be close to failure is considered safe and therefore
constructs a conservative FLC.
Figure 11 - Failure at the lock ring in the 50mm (left) and 25mm (right) specimens
As stated previously, the larger specimens failed in the region visible to the optical
measurement system. Therefore, information about the exact state of strain at failure could be
determined and “failed” points included on the FLC. This failure, shown in figure 12,
presented as a tear in the aluminium layer and fibre breakage in the composite layer.
.
Figure 12 - Failure behaviour of the larger FML specimens
Neck Failure
A. Sexton, W.J. Cantwell and S. Kalyanasundaram.
12
The forming limit curves constructed for the FML and aluminium are shown in figure 13.
This display is advantageous as it allows the direct comparison of the forming limits of the
FML and aluminium. It is demonstrated in the figure that the FLC of the aluminium is slightly
higher than the FML. The FML FLC agrees with the theory that the glass fibre will fail at a
strain of approximately 4-8%, with the marginal region occurring in the region between these
strain values. The localised necking in the FML specimens can be seen from the failed points
in the figure which are at much higher strain values than can be sustained by a glass fibre
composite. In addition, they display significantly higher strain results than the marginal data
points which were taken prior to an observation of a neck such as in figure 10. The FLC for
the FML shows that, at room temperature, the strain in the glass fibre limits the ability of the
FML to deform using the stamp forming process.
(a)
(b)
Figure 13 – Forming limit curve for the FML (a) and aluminium (b)
4 CONCLUSIONS
The deformation behaviour of a FML based on a glass fibre reinforced polypropylene
composite has been observed, analysed and compared to the forming of aluminium using an
optical strain measurement technique. This technique allowed the comparison of not only the
final state of strain in the formed parts but also the evolution of the strain to failure. This
study has established that fibre metal laminates constructed from high-stiffness, low strain to
failure composites is possible with some restrictions. Firstly, the strain behaviour of the
laminate is different to that exhibited by the monolithic aluminium specimens, with negative
strain ratios difficult to attain. This behaviour could be explained by the limited draw of the
fibres in the lateral direction. Additionally, the strain at failure for the FML is determined by
the maximum strain in the glass fibre, about 4-8%, which is lower than the failure strain of the
aluminium. By orientating the glass fibre at an angle from the longitudinal axis it would be
possible to achieve higher strains in the laminate due to lower strains in the glass fibres. In
addition, a higher temperature could lead to improved forming through softening of the
composite matrix which would allow the fibres in the composite to draw in more easily.
Finally, it was demonstrated that, unlike other composites and fibre metal laminate systems,
this particular FML exhibited necking in the aluminium layer prior to failure. This study
shows that, by optimising some of the forming parameters, it could be possible to process
glass fibre reinforced fibre metal laminates.
A. Sexton, W.J. Cantwell and S. Kalyanasundaram.
13
REFERENCES
[1] A.B. Lovins and D.R. Cramer. Hypercars, hydrogen and the automotive transition.
International Journal of Vehicle Design, 35, 50-85 (2004).
[2] S. Das. The cost of automotive polymer composites: a review and assessment of
DOE’s lightweight materials research. Technical Report ORNL/TM-200/283, Energy
Division, Oak Ridge National Laboratory (2001).
[3] C.A.J.R Vermeeren. An historic overview of the development of fibre metal laminates.
Applied Composite Materials, 10, 189-205 (1999).
[4] J.F. Laliberté, C. Poon, P.V. Straznicky and A. Fahr. Applications of fiber-metal
laminates. Polymer Composites, 21, 558-567 (1999).
[5] S.P Keeler and W.A. Backofen. Plastic Instability and Fracture in Sheets Stretched
Over Rigid Punches, ASM Transactions Quarterly, 56, 25–48 (1963).
[6] C. Morrow, S. DharMalingam S. Venkatesan and S. Kalyanasundaram, Stretch
Forming Studies on Thermoplastic Composite, Proceedings of 6th Australasian
Congress on Applied Mechanics, Perth, Australia, December 2010.
[7] J.H. Lee and J.H. Vogel. Biaxial stretch forming of thermoplastic composite sheets,
Proceedings of the 27th International SAMPE Technical Conference, Albuquerque,
NM, October 1995.
[8] S. Venkatesan and S. Kalyanasundaram, Finite Element Analysis and Optimization of
Process Parameters during Stamp Forming of Composite Materials, Proceedings of 9th
World Congress on Computational Mechanics and 4th Asian Pacific Congress on
Computational Mechanics, WCCM/APCOM2010, Sydney, Australia, July 2010.
[9] S. Venkatesan and S. Kalyanasundaram, A Study on the Real Time Strain Evolution in
Glass Fibre Reinforced Composites during Stamp Forming, Proceedings of 6th
Australasian Congress on Applied Mechanics, Perth, Australia, December 2010.
[10] S. Venkatesan and S. Kalyanasundaram, Effect of Preheat Temperature on
Formability of Consolidated all-PP Composite Materials during stamp forming,
Proceedings of 6th Australasian Congress on Applied Mechanics, Perth, Australia,
December 2010.
[11] N.O. Cabrera, C.T. Reynolds, B. Alcock and T. Peijs. Non-isothermal stamp forming
of continuous tape reinforced all-polypropylene composite sheet, Composites: Part A,
39, 1455–1466 (2008).
[12] L. Mosse, W. Cantwell, M.J. Cardew-Hall, P. Compston and S. Kalyanasundaram. A
study of the effect of process variables on the stamp forming of rectangular cups using
fibre-metal laminate systems, Advanced Materials Research, 6-8, 649–656 (2005).
[13] L. Mosse, P. Compston, W.J. Cantwell, M. Cardew-Hall and S. Kalyanasundaram.
The effect of process temperature on the formability of polypropylene based fibre–
metal laminates, Composites: Part A, 36, 1158–1166 (2005).
[14] L. Mosse, P. Compston, W. Cantwell, M. Cardew-Hall and S. Kalyanasundaram. The
development of a finite element model for simulating the stamp forming of fibre-metal
laminates, Composite Structures, 75, 298–304 (2006).
[15] L. Mosse, P. Compston, W. Cantwell, M. Cardew-Hall and S. Kalyanasundaram.
A. Sexton, W.J. Cantwell and S. Kalyanasundaram.
14
Stamp forming of polypropylene based fibre-metal laminates: The effect of process
variables on formability, Journal of Materials Processing Technology, 172, 163–168
(2006).
[16] J. Gresham, W. Cantwell, M.J. Cardew-Hall, P. Compston and S. Kalyanasundaram.
Drawing behaviour of metal-composite sandwich structures, Composite Structures, 75,
305–312 (2006).
[17] S. DharMalingam, P. Compston and S. Kalyanasundaram. Forming analysis of metal-
composite sandwich structures, Proceedings of the 14th European Conference on
Composite Materials, Budapest, Hungary, June 2010.
[18] G. Reyes and H. Kang. Mechanical behavior of lightweight thermoplastic fiber-metal
laminates, Journal of Materials Processing Technology, 186, 284– 290 (2007).
[19] A. Sexton, W. Cantwell and S. Kalyanasundaram. Stretch forming studies on a fibre
metal laminate based on a self-reinforcing polypropylene composite, Composite
Structures, 94, 431-437 (2012).
[20] S.S. Hecker. Simple technique for determining forming limit curves, Sheet Metal
Industries, 52, 671–676 (1975).