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7/27/2019 Materials Science and Engineering -Mechanical properties and microstructure of Ermel
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Materials Science and Engineering A 387–389 (2004) 845–851
Mechanical properties and microstructure of carbon fibre reinforcedcarbon materials produced by chemical vapour infiltration
R. Ermel, T. Beck ∗, O. Vöhringer
Institute of Materials Science and Engineering I, University o f Karlsruhe (TH), Kaiserstr. 12, D-76131 Karlsruhe, Denmark
Received 25 August 2003; received in revised form 25 November 2003
Abstract
Correlations between mechanical properties, fibre architecture, matrix texture and fracture behaviour of carbon fibre reinforced carbon
CFC-materials produced by chemical vapour infiltration are investigated using results from tensile and four-point-bending tests, polarized
light microscopy and scanning electron microscopy. Mechanical testing was performed at temperatures from 20 up to 1600 ◦C. Samples
were tested in the as-received state and after heat treatment at T = 2200 ◦C. The heat treatment leads to an increasing Young’s modulus
and brittleness, which corresponds with an increasingly distinct layer structure of high textured matrix carbon. A rise of test temperature up
to 1400 ◦C also leads to a larger Young’s modulus and increasing brittleness. However, at T = 1600 ◦C the material shows a pronounced
pseudoductile behaviour. Scanning electron micrographs show in this case a lot of concentric cracksbetween the sublayers of the high textured
matrix. The fracture behaviour is explained by a multiple delamination between these layers.
© 2004 Elsevier B.V. All rights reserved.
Keywords: Carbon/carbon-composites; Fracture behaviour; High-temperature properties; Tensile test; Four-point-bending test; Microstructure
1. Introduction
High strength at temperatures up to 1800 ◦C and a good
chemical resistance in neutral and reducing environments
are outstanding properties of carbon fibre reinforced carbon
(CFC). The capability to pseudoductile fracture behaviour in
the case of an appropriate fibre architecture and matrix tex-
ture predestinates CFC as a material for components, which
undergo extremely high thermal and mechanical loadings.
Pseudoductile behaviour of such a composite consisting of
two brittle components occurs if an appropriate strength
of the fibre–matrix interface results from the manufactur-
ing process. Then, matrix initialized cracks deflect at the
fibre–matrix interfaces and a locally limited debonding be-
tween fibres and matrix takes place and the fibres will bridge
the crack. Additionally, fibre fracture during further load-
ing can cause so-called fibre-pullout, consuming additional
energy for crack propagation [1–3].
The fracture toughness of CFC can be further increased
if the crack deflection occurs not only at fibre–matrix inter-
∗ Corresponding author. Tel.: +49-721-608-4159;
fax: +49-721-608-7451.
E-mail address: [email protected] (T. Beck).
face but also in the matrix itself [4]. This behaviour requires
a matrix consisting completely, or at least partially, of high
textured pyrolytic carbon, which is deposited in concentric
layers around the fibre. Tests on chemical vapour infiltrated
(CVI) fibre-felts show, that a material with a larger volume
fraction of high textured matrix shows a more pronounced
pseudoductility than composites with medium or low tex-
tured matrices [5].
The CVI process can be described as follows: methane
diffuses into the fibre-preform, where it cracks into hydrogen
and elementary carbon and latter is deposited on the surface
of the fibres until the fibre structure is completely densified.
Because of an exact understanding of the CVI process [6,7],
it is possible to produce a composite of high density within a
time of a few days. The parameters of the infiltration process
must be optimized to get a complete densification combined
with the desired texture of the carbon matrix [8].
This work presents the results of four-point-bending and
tensile tests at temperatures from 20 up to 1600 ◦C on two
different CVI-CFC-materials. Some specimens were heat
treated at T = 2200 ◦C after manufacturing which results in
a weak partial graphitization of the high textured pyrolytic
matrix carbon. Fractographic investigations with SEM and
a microstructure analysis with polarized light microscopy
0921-5093/$ – see front matter © 2004 Elsevier B.V. All rights reserved.
doi:10.1016/j.msea.2003.12.075
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846 R. Ermel et al. / Materials Science and Engineering A 387–389 (2004) 845–851
Fig. 1. Microstructure of CVI-CFC.
(PLM) are used for the interpretation of the results of me-
chanical testing.
2. Experimental details
2.1. Investigation of the microstructure
The investigation of the microstructure is carried out by
polarized light microscopy (PLM) on specimens cut per-
pendicular to the fibre direction. The measurement of the
Fig. 2. Material 1: UD- and fibre-felt-layers (a) and material 2: 2D-0/0/90/90 (b).
extinction angle of polarized light characterizes the texture
of pyrolytic carbon, so that a separation in isotropic (ISO),
low (LT), medium (MT) und high textured (HT) carbon is
possible [9].
Fig. 1 shows an example of a carbon fibre surrounded by
matrix-layers with different textures.
2.2. Mechanical testing
Mechanical testing of the CFC-samples is performed on
an electromechanical testing machine. Because of the sus-
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R. Ermel et al. / Materials Science and Engineering A 387–38 9 (2004) 845–851 847
Fig. 3. Stress–strain curve from tensile test at T = 20 ◦C, surface and longitudinal strain-distribution of three states of this tensile test (a). Scanning
electron micrograph of the corresponding fracture surface (b).
ceptibility of CFC against oxidation the tests at high temper-
atures are carried out in a vacuum chamber at an air-pressure
of p < 10−8 bar. With inductive heating of the specimens test
temperatures up to 1800 ◦C can be reached. The crosshead
speed for four-point-bending tests is 2.0 mm/min and for
the tensile tests 0.5 mm/min. The integral strain is mea-
sured with a capacitive extensometer. Additionally an op-
tical extensometer based on grey-scale-correlation-analysis
allows for an integral as well as locally resolved determi-
nation of the strains even at the highest test temperatures
[10].
2.3. Specimen geometry
The bending samples have a size of L × B × H = 52mm
× 6 mm × 1.6 mm and the distances of the inner and the
outer support are L0 = 20mm and La = 45 mm, respectively.
Assuming a linear elastic behaviour the fictitious bending
strength σ R∗ is calculated according to:
σ ∗R =
3F m
La−Li
2
BH 2(1)
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848 R. Ermel et al. / Materials Science and Engineering A 387–389 (2004) 845–851
Table 1
Investigated materials
Designation Preform Preform-
manufacturer
Fibre
volume ratio
Fibre type
Material 1 UD/felt layer Dunlop About 20% HT
Material 2 2D-0/0/90/90 Sintec 22.5% HT
using F m as maximum load. The elastically calculated sur-
face strain results from the deflection between the inner
supports. The gauge length of the tensile specimens is L0
= 15 mm with a cross-section of B × H = 2 mm × 3mm.
3. Materials
The investigated CFC-materials consist of infiltrated
preforms with a different fibre architecture (Fig. 2). Ma-
terial 1 is made of two different layers, a unidirectional
(UD) C-fibre and a fibre-felt layer. Material 2 consists of a two-dimensional preform with a sequence of the layers
in 0◦ /0◦ /90◦ /90◦ direction. Within each layer, 80% of the
fibres are orientated in the main direction.
The specimens are taken from the infiltrated preform
in such a way that the directions of the load-axis and fi-
Fig. 4. Comparison between σ –εt curves of heat treated and as-received
specimens from tensile test (a) and four-point-bending test (b).
bres are parallel (Fig. 2). The sequence of the layers of
the specimens from material 1 are chosen in order to get
UD-layers at both surfaces of the samples. Table 1 sum-
marizes fibre architecture, fibre volume ratio and fibre
type.
The parameters of the CVI-process are the same for both
materials. Due to that, the matrix in both materials mostlyconsists of high textured pyrolytic carbon with a thin layer
of low textured pyrolytic carbon around the fibres. Material
1 is characterized by a density of ρ = 1.82 g/cm3 and an
open porosity of P = 7%, the respective values of material
2 are ρ = 1.76 g/cm3 and P = 10%.
Fig. 5. SEM-pictures of fracture surfaces of material 1 in the as-received
(a) and the heat treated state (b) after four-point-bending at T = 20 ◦C.
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4. Results and discussion
4.1. Material 1
Under tensile loading material 1 in the as-received state
shows a marked pseudoductile behaviour with pronounced
fibre-pullout as presented in a typical stress–strain curve and
Fig. 6. Representative stress–strain curves for tensile and
four-point-bending tests (a) and scanning electron micrographs of the
fracture surface of four-point-bending (b) and tensile samples (c).
the corresponding fracture surface for a test temperature of
20 ◦C in Fig. 3. The fracture surface of four-point-bending
specimens shows less pronounced fibre-pullout compared
with tensile specimens.
Additionally, in Fig. 3a the surface and the local
strain-distribution in longitudinal direction is represented
in three states of the tensile test. Distinct concentrationsof strain can be found at a relatively low total strain of εt
= 0.45% (phase 2) before a crack on the surface can be
noticed.
4.2. Influence of heat treatment
An influence of a heat treatment at T = 2200 ◦C for
2 h can be seen in tensile as well as in four-point-bending
tests (Fig. 4). In both cases the Young’s modulus in-
creases slightly while the plastic strain to failure decreases.
The influence of the heat treatment is more pronounced
in tensile tests. An increase of strength due to the heat
treatment observed in tensile tests cannot be noticed in
four-point-bending tests. The reason might be a larger scat-
ter of the flexural strength, caused by a different fracture be-
haviour. This can be seen in one case in which delamination
of a large area between unidirectional and felt-layer super-
poses the influence of fibre–matrix delamination. The cor-
responding σ R–εR,t curve is marked by an arrow in Fig. 4b.
An investigation of the fracture surfaces by SEM shows
for the heat treated sample (Fig. 5b) a more distinct laminar
structure of the high textured pyrolytic carbon, compared
to the as-received state (Fig. 5a). In addition, the matrix is
characterized by many cracks parallel to the layers. However,
the extent of pullout of fibres and matrix layers seems tobe reduced by the heat treatment. PLM investigations did
not show any change of the matrix texture due to the heat
treatment.
4.3. Material 2
A comparison between the stress–strain behaviour of ma-
terial 2 in tensile- and four-point-bending tests at T = 20 ◦C
Fig. 7. Stress–strain curves for T = 20, 1100, 1400 and 1600 ◦C.
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850 R. Ermel et al. / Materials Science and Engineering A 387–389 (2004) 845–851
Fig. 8. SEM-pictures of fracture surfaces after four-point-bending tests at T = 1600 ◦C (a) and at T = 20 ◦C (b).
is presented in Fig. 6a. A larger plastic elongation is found
in the tensile test. This agrees with SEM examinations of
the fracture surface after tensile and bending tests which
showed a larger extent of fibre-pullout and delamination of matrix layers for tensile specimens (Fig. 6b and c).
4.4. Influence of test temperature
Four-point-bending tests were carried out at temperatures
up to 1600 ◦C. The resulting surface stress–strain curves are
shown in Fig. 7 for temperatures of 20, 1100, 1400 and
1600 ◦C. Young’s modulus increases slightly with tempera-
ture while the scatter of the strength values decreases with
T . Up to T = 1400 ◦C, all samples show a brittle fracture be-
haviour. However, at T = 1600 ◦C the plastic fracture strain
of 0.3% is much higher than at lower T . An explanation is
given by SEM-observation of the fracture surfaces at high
magnification at which a high textured matrix streaked with
a lot of concentric cracks can be detected (Fig. 8a). The sur-face is very rough while the surface of the samples tested at
temperatures up to 1400 ◦C is much smoother (Fig. 8b). Ac-
cordingly, delamination between matrix layers can explain
the pseudoplastic behaviour at T = 1600 ◦C. Fibre-pullout
seems to be of subordinate significance, because the fracture
surfaces show a similar structure at all test temperatures.
5. Summary
Two CVI-CFC materials with a different fibre architec-
ture but with mainly the same matrix texture were tested
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R. Ermel et al. / Materials Science and Engineering A 387–38 9 (2004) 845–851 851
in four-point-bending and tensile tests at temperatures up
to 1600 ◦C. For both materials tensile loading led to a
more pronounced pseudoductility and fibre-pullout than
four-point-bending tests.
The consequence of heat treatment of material 1 at T
= 2200 ◦C after infiltration is a slightly higher Young’s
modulus and a lower plastic fracture strain than inas-received state. Scanning electron micrographs showed
a more distinct layer structure of the high textured ma-
trix and a smaller fibre and matrix layer pullout in the
case of heat treated specimens. A significant change of
the texture caused by heat treatment was not detected by
PLM.
Increasing test temperatures up to 1400 ◦C lead to increas-
ing Young’s modulus and a decreasing plastic fracture strain.
However, an influence of T ≤ 1400 ◦C on the fracture sur-
face and matrix microstructure cannot be noticed. Tests at T
= 1600 ◦C resulted in a relatively large plastic fracture strain
of about 0.3%, due to an increasing number of concentric
cracks within the high textured matrix. So, this pseudoplas-tic behaviour is attributed to delamination between matrix
layers.
Acknowledgements
The present study was performed in the Collaborative Re-
search Center 551: “Carbon from the gas phase”. Financial
support by the German Research Foundation (DFG) is grate-
fully acknowledged. The authors thank Prof. K.J. Hüttinger
for the infiltrated samples.
References
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