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EFFECTS OF DEFECTS ON INTERLAMINAR PERFORMANCE OF COMPOSITES
Andrew Makeev*, Yuri Nikishkov, Guillaume Seon, and Erian Armanios Department of Mechanical and Aerospace Engineering
University of Texas at Arlington, Arlington, Texas, U.S.A.
Abstract
This work presents a methodology for accurate assessment of the effects of manufacturing defects on the interlaminar tensile (ILT) strength and fatigue performance of composites used in rotorcraft fatigue-critical structural designs. A primary failure mechanism for such structures is delamination. Although the ILT strength and fatigue material properties are essential for the development of analytical predictive methods for initiation of delamination at sites that give rise to interlaminar stresses, there are no reliable methods to determine such properties. A major technical challenge is the extreme sensitivity of the ILT to manufacturing defects including porosity that could lead to unacceptable scatter in test results. In this work, X-Ray Computed Tomography (CT) measurements of porosity defects present in curved-beam test articles, are integrated into finite element based stress analysis to capture the effects of defects on the ILT strength and fatigue behavior. Once the effects of manufacturing defects are captured through transfer of the CT measurements into a three-dimensional finite element model, their contribution to the scatter in the test data could be quantified, and reliable interlaminar material properties determined. The ability to extract accurate ILT material properties from curved-beam tests is verified through an alternative short beam test configuration and method. The proposed test provides a basis for assessing the effects of defects.
1. INTRODUCTION1
Currently, composite structural designs are based upon the same factor of safety as that of metals, 1.5, to determine the ultimate design load from limit load. This is in spite of the susceptibility of composite parts to variations in manufacturing processes compared to metal parts. In addition to material variation in the resin content, bulk factor, and fiber alignment, part fabrication process variations such as operator skill, tooling setup, humidity fluctuation and equipment control, are common causes that contribute to variation in part quality. Consequently, the increased sensitivity of composite part quality to material and process variations lowers production yields. Production yields of greater than 90% remain a “hit-and-miss” target [1].
The effects of manufacturing process parameters on structural strength and durability are not well understood. In particular, the effects of inadequate design method and manufacturing process used to produce carbon/epoxy and glass/epoxy composite aircraft fatigue-critical, flight-critical components, result in defects such as porosity and voids, impacting
1 Presented at the 39th European Rotorcraft Forum, Moscow, Russia, September 3-6, 2013.
* Corresponding author, e-mail: [email protected].
the residual capability and the useful life of these components.
Manufacturing defects can severely deteriorate matrix-dominated properties, resulting in degraded strength and fatigue structural performance. While it is not feasible to eliminate all defects in a composite part, it is possible to improve upon desing conservatism and address part durability and damage tolerance requirements once the defects and their effects are captured. Advanced structural methods that account for manufacturing defects in composite parts are needed to enable accurate assessment of their capability and useful life and enhance current design and maintenance practices.
One of the major barriers to accurately predict failure for polymer-matrix composites has been the lack of reliable matrix-dominated material properties which could be used as a basis for the development of accurate failure criteria [2, 3]. In particular, interlaminar tensile (ILT) strength and fatigue properties have been challenging to characterize. Accurate measurements of ILT strength and fatigue performance characteristics are needed to capture delamination failure which is one of the primary failure modes for rotorcraft composites. Glass-fiber and carbon-fiber reinforced epoxy-matrix prepreg composites, susceptible to delamination, are most commonly used in the design of rotorcraft composite structures.
Helicopter rotor systems are subject to extreme cyclic loads. The fatigue capability is a limiting factor for high-cycle components in dynamic systems [4]. Typical examples of the fatigue-critical primary composite structures include main rotor blade spars and yokes in commercial and military helicopters [5]. The primary failure mechanism for such structures is delamination. Accurate ILT and interlaminar shear (ILS) fatigue material properties integrated in reliable failure criteria are essential for the development of predictive methods able to capture fatigue delamination. In particular, Reference [3] successfully used ILT and ILS S-N fatigue curves in the formulation of stress-based and fracture-based fatigue failure criteria to predict the onset and propagation of matrix-dominated failure modes including delaminations. However, the development of failure prediction methods is currently limited by the lack of reliable ILT material properties.
A major technical challenge to characterizing ILT behavior is extreme sensitivity to manufacturing defects including porosity that could lead to significant scatter in test results. Composite helicopter rotor components are typically thick and oftentimes have areas with tight radius of curvature [4], which make them especially prone to porosity defects. Test articles representative of curved structural details in composite parts, adopted by the rotorcraft industry, are prime candidate to better understand the effects of porosity. However, there is no consensus on the accept/reject criteria for assessing the effects of porosity on strength and fatigue performance. It has been determined that porosity volume content is not a reliable basis for capturing the effects of defects.
A relatively simple test specimen that could become a standard across the industry for characterizing porosity in composite structures, along with the analysis methodology able to determine the key elements for capturing of the effects of defects on structural performance, would be extremely beneficial.
To the best of the authors’ knowledge, there are no standard test methods for the assessment of ILT fatigue performance in composites. However, there are two American Society for Testing and Materials (ASTM) standard methods for measuring ILT strength.
Currently, ASTM D 6415 curved-beam (CB) test is a standard practice for measuring the ILT strength [6]. Figure 1 shows a typical CB test setup for a 6.6 mm (0.26-inch) thick unidirectional carbon/epoxy tape system. The failure mode is tensile delamination that starts in the radius area, typically at about two third of the thickness corresponding to the maximum interlaminar tensile stress location, and quickly propagates through the flanges. ASTM D 6415 provides a closed-form approximation of the ILT strength [6–8].
Figure 1. ASTM D 6415 test setup and tensile delamination failure of a unidirectional IM7/8552 carbon/epoxy CB specimen. Dashed lines indicate the area subject to CT scanning.
The authors measured ASTM D 6415 CB strength for multiple unidirectional carbon-fiber and glass-fiber reinforced epoxy-matrix prepreg tape composites. Based on their experience, the curved-beam strength data typically exhibit large scatter. For example, for 6.6 mm (0.26-inch) thick CB coupons manufactured from Hexcel IM7/8552 unidirectional tape [9] and cured per manufacturer’s specifications, the average ASTM D 6415 interlaminar tensile strength value varies between 68.9 MPa (10 ksi) and 82.7 MPa (12 ksi) with a coefficient of variation (COV) usually higher than 20%. This raises doubts concerning the adequacy of the ASTM D 6415 standard as a coupon-independent test for measuring ILT material strength. Large scatter in material characterization test results may reflect manufacturing quality as much as the material properties.
Another method for assessing the ILT strength is ASTM D 7291 which applies a tensile force normal to the plane of a composite laminate using adhesively bonded thick metal end-tabs [10]. As noted in Ref [10], through-the-thickness strength results generated using this method will not, in general, be comparable to ASTM D 6415 since ASTM D 7291 subjects a relatively large volume of material to a quasi-uniform stress field while ASTM D 6415 subjects a small volume of material to a non-uniform stress field. Moreover, characterizing ILT strength using ASTM D 7291 is perhaps more challenging than ASTM D 6415 as failure could occur in the bond lines between the composite and the metal end-tabs.
Carbon/epoxy CB specimen configurations were studied in Ref [11] to establish a method for assessing ILT strength. It was noted that “Strength data obtained from curved beam test specimens can be very relevant to the design process. Specimens with curved geometries present unique manufacturing problems that do not occur in flat panels. Consequently, failure modes and strengths obtained
20 mm
from curved beam specimens with manufacturing flaws will closely resemble those in the actual structure with similar flaws. However, if a specimen does not contain any significant flaws, a true material property may be measured.” Reference [11] recorded a significant CB strength reduction (up to a factor of four) in low-quality CB specimens due to large voids detected based on a cross-section cut using a diamond saw. However, large scatter in the strength data observed in high-quality CB specimens could not be explained due to the lack of available three-dimensional nondestructive inspection techniques with micro-focus ability at that time. This work shows that microscopic defects present in high-quality CB specimens (with extremely low porosity content) cause large scatter in curved-beam strength and fatigue behavior.
The objective of this work is to develop efficient and accurate methods to capture the effects of porosity on the ILT strength and fatigue material behavior. Once the effects of manufacturing defects are understood, their contribution to the scatter in test data could be quantified, and reliable material properties extracted.
ADTM D 6415 CB specimens are well suited for assessing the effects of porosity on ILT strength and fatigue performance. Porosity can be easily introduced in the CB specimens; the CB radius area susceptible to delamination onset is far away from the attachments of the test fixture; and the nondestructive inspections can be limited to that area. Therefore, such specimens could arguably be the most suitable candidates to assess the effects of porosity on ILT strength and fatigue behavior.
The ability to extract accurate ILT material properties from CB tests must first be verified. To this end, the recently developed short-beam (SB) method [12] is expanded to enable measurement of the ILT strength for pristine material structure; and establish a rigorous basis for assessing the effects of manufacturing defects in the CB specimens. It is worth noting that failure of a SB specimen also occurs due stressing small volume of material. As the manufacturing process to produce flat SB specimens is simpler compared to CB specimens, the SB specimens are relatively free of defects and can potentially be used as a baseline for determining ILT material strength.
2. SHORT-BEAM METHOD
Short-beam (SB) specimens are prismatic coupons with uniform rectangular cross-sections and subject to three-point bending. Reference [12] provides the details of the methodology for assessing multiple stress-strain constitutive relations, based on the SB tests and the digital image correlation (DIC) technique-based deformation measurement. The dimensions of the SB coupons and the test fixture attachments were modified compared to ASTM D 2344 [13] in order to
generate accurate stress-strain curves as well as consistent failure modes [12, 14]. SB test coupons have been machined in the zero-degree and 90-degree directions from unidirectional tape panels and loaded in the 1-2 (in-ply), 1-3 (interlaminar) and 2-3 principal material planes to characterize the shear stress-strain relations; Young’s moduli in the zero-degree and 90-degree directions; and Poisson’s ratios. The fiber direction is denoted as 1 (zero-degree); the in-ply transverse direction as 2 (90-degree); and the laminate thickness direction as 3 (interlaminar direction.)
To characterize ILT material properties in this work, six SB specimens were machined in the thickness direction from a 106-ply thick IM7/8552 carbon/epoxy unidirectional tape panel cured at 177⁰C (350⁰F) per prepreg manufacturer’s specifications [9]. The cured ply-thickness was approximately 0.183 mm (0.0072 in) resulting in 19.4-mm (0.76-in) panel thickness. The SB specimen length was 19.4-mm (0.76-in). The coupons were 3.8-mm (0.15-in) thick, and 2.8-mm (0.11-in) wide. The coupon thickness corresponds to the in-ply 90-degree principal material direction; and the 2-3 principal material plane is the plane of loading. Figure 2 shows a schematic of a SB coupon and the loading conditions.
Figure 2. A SB coupon machined from a thick plate in the interlaminar (thickness) direction; loading conditions; and the interlaminar tensile failure.
To assess the ILT strength, the SB specimens were placed in an ASTM D 2344 test fixture with a 12.7-mm (0.5-inch) diameter loading nose and 3.18-mm (0.125-inch) diameter supports; and loaded in an electromechanical load frame at a constant 1.27 mm/min (0.05 in/min) crosshead displacement rate till failure. It is worth noting that the ASTM standard loading nose diameter is 6.35 mm (0.25 inches). The support length was 14.99 mm (0.59 inches). All SB specimens failed in tension in the middle of the specimen as schematically shown in Figure 2. The average failure load value was 209 N (47 lbs), which was too low to introduce any compressive damage
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6415 recommends 25.4-mm (1-inch) width. The width has been reduced based upon previous tests of both 25.4-mm (1-inch) and 12.7-mm (0.5-inch) wide CB specimens which resulted in similar interlaminar strength values as well as scatter. Specifically, the most recent batch of six 1-inch wide and 6.60-mm (0.26-inch) thick unidirectional IM7/8552 CB tests conducted by the authors resulted in an average ASTM D 6415 ILT strength of 77.2 MPa (11.2 ksi) and a 21.4% COV which are close to the 72.5 MPa (10.5 ksi) ILT strength and the 26.5% COV resulting from the 12.7-mm (0.5-inch) wide CB specimens of the same thickness, tested in this work.
The average 72.5 MPa (10.5 ksi) ASTM D 6415 CB strength value is significantly lower compared to the 116.5 MPa (16.9 ksi) value generated based on the SB tests. Also, the 26.5% COV in the CB strength is more than eight times higher compared to the 3% COV in the ILT strength reported from the SB tests.
4. REFINEMENT OF THE CURVED-BEAM METHOD TO ACCOUNT FOR POROSITY
ASTM Standard D 6415 underscores the sensitivity of measured ILT strength to void content. Consequently, the test results may reflect manufacturing quality as much as material properties [6]. An industrial computed tomography (CT) system with a 225 KV Microfocus X-ray tube and Varian 4030E series flat panel detector, built by North Star Imaging, Inc. was utilized in this work to detect porosity in the CB test specimens. The micro-CT scans were accomplished at 40 kV tube voltage and 400 μA target current at 0.5 frames per second and 10.5x magnification resulting in 0.5Χ10-3 in (12 μm) scan resolution. The dashed lines in Figure 1 outline the area of the CT scan. Specimen cross-sectional images were obtained from the 3D volumetric model reconstructed in the efX-CT software by North Star Imaging. About 1,000 through-the-width section images, approximately 1200×1600 pixels in size, were used for void detection in each specimen. Void identification, classification and measurement were performed by the Numerical Technology Company software. The software applied binary threshold transformation based on the pixel intensity found at local minima between air and material peaks on the pixel histogram (representing the number of pixels at a given intensity) for the full scan volume; and then used object labeling and elliptical shape fitting for void measurements and calculation of the porosity volume. The CT based measurements were conducted on all ten 12.7-mm (0.5-inch) wide specimens.
Figure 4. Void geometry in CB specimen 6.
Figure 4 shows examples of voids found in a representative CB specimen. Voids typically have the largest aspect ratios in the fiber direction resulting in thin curved shapes, and often degenerating into noodle-like shapes. Void thickness was found to be the smallest void dimension in all specimens. This geometry can be attributed to the expansion of air pockets that exhibit the largest resistance, in the thickness direction, due to curing pressure. It is worth noting that the porosity content in the CB specimens was low, e.g. the porosity content in the laminate thickness-based 6.6 × 6.6 × 6.6 mm3 (0.26 × 0.26 × 0.26 in3) cube volumes throughout the CT scans in the CB radius area was less than 0.12%. However, it is not the volume but the presence of individual voids at critical locations that reduces failure loads and causes large scatter.
The porosity volume alone is not sufficient for describing the effects or severity of voids. Indeed, a single large void located close to the mid-plane in the CB radius area is worse than a few dispersed smaller voids that add up to the same total volume. Reference [17] indicates that the porosity volume often does not correlate well with the degradation in structural performance.
Post-failure CT scans of the CB specimens confirmed that delamination progresses through longer voids located around the mid-section of the specimens. Figure 5 shows typical cracks in a representative failed specimen. For all specimens, critical voids were identified in the CT scans before specimen failure and confirmed as the origin of delamination in the corresponding post-failure CT scans. Critical voids are located in the vicinity of the maximum interlaminar tensile stress (about two third of the thickness in the middle of the radius area). Table 1 lists the geometry and reference locations of the critical voids.
L
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W
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Table 1. GeCB specimmeasured fris measuredspecimen.
Spec Void Lemm (mi
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3 1.4 (5
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5 2.6 (1
6 5.6 (2
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8 0.21 (
9 0.27 (
10 0.6 (2
Avg 1.9 (7
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ength il)
Width, mm (mil)
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90) 1.3 (49
56) 0.5 (18
28) 0.5 (18
00) 1.2 (47
220) 2.4 (94
68) 0.7 (28
(8.1) 0.3 (12
(11) 0.17 (6.8
25) 0.22 (8.7
76) 0.8 (31
ows the trenn of the voidby 3.21 kN ( of an ideao calculate ta 116.5 MPaased on the
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distance frominimum pofor the pointdistance coconsidered that distancinterlaminar distance of point-stress average-stre
Figure 10interlaminar stress (top)
The averageksi) for the ksi) for the acurved-beamand comparD 6415 [6]. values founagree with ttests. Noteaverage-streonly 2.1% aASTM D 64that the repristine (free
om the voidoint was ident-stress and arresponding as the optimce was use
tensile stre19 μm (7.3×1method and
ess method.
0. Charactetensile stre
and the aver
e ILT strengtpoint-stress average-stresm specimensred to the str The averagd using the the 116.5 MPe that COV ess based Iand 3.2% com415 approximefined ILT se of defects)
d, a uniquentified as shoaverage-stresto the minimal characteris
ed to determngth value. 10-4 in) was dd 89 μm (3.5
eristic distaength (ILTS) rage-stress (b
th values are method and ss method. Rs are summaresses calculae interlaminarefined CB t
Pa (16.9 ksi)in the poin
LT strength mpared to 26
mation. Low strength is amaterial prop
e and distinown in Figurss methods.
mum COV castic distancemine the re A characte
determined fo5×10-3 in) fo
ance and using the p
bottom) meth
124.3 MPa 110.4 MPa
Results for tharized in Tabated using Aar tensile stretest methodo) ILT from thent-stress and
calculations6.5% COV inscatter sugg
appropriate aperty, and th
nctive re 10 The
an be ; and
efined eristic or the or the
the point-hod.
(18.0 (16.0 e ten ble 2
ASTM ength ology e SB d the s are n the gests as a e CB
test ILT s
Tabinterwith
Spec
1
2
3
4
5
6
7
8
9
10
Avg
COV
5.
Thison faand curvASTservcell ratioFiguCBdelacurvthroulocaamocoinin delaobse
is useful forstrength.
le 2. Failurerlaminar tensporosity defe
cFailure Load, kN (lbs)
2.24 (503)
1.34 (302)
1.89 (425)
2.61 (586)
1.27 (286)
0.93 (210)
1.85 (416)
2.47 (555)
2.45 (550)
2.06 (463)
1.91 (430)
V 28.2%
EFFECTS OPERFORMA
s Section preatigue testing
12.7-mm (0ved-beam speTM D 6415 tvo-hydraulic lcapacity, and
o and 5 Hz ure 11 shows
specimensaminations inved-beam spugh the flantions of the
ong the specide with thethe poros
aminations aserved in som
r assessing t
e load, ASTsile strength (ects.
ASTM D 6415 ILTS, MPa (ksi)
Repome(ks
83.4 (12.1) 1
52.3 (7.6) 1
70.3 (10.2) 1
92.8 (13.5) 1
50.0 (7.3) 1
37.7 (5.5) 1
68.8 (10.0) 1
94.6 (13.7) 1
93.9 (13.6) 1
81.5 (11.8) 1
72.5 (10.5) 1
26.5%
OF DEFECTSANCE
esents S-N cg of CB coup0.5-in) wide ecimens wertest fixture woad frame wd subjected t
frequency, s examples o
after fatignitiated in tpecimens; anges. It ise delaminatecimens; ane location of sity-free sps well as delae of the curve
the effects of
TM D 6415 (ILTS) for CB
efined ILTS, oint-stress ethod, MPa si)
Reavme(ks
23.1 (17.9)
25.1 (18.1)
25.8 (18.2)
23.8 (18.0)
19.0 (17.3)
25.2 (18.2)
29.3 (18.7)
25.8 (18.2)
23.9 (18.0)
21.5 (17.6)
24.3 (18.0)
2.1%
S ON THE ILT
curves determpons. Twenty
IM7/8552 ure tested in fwas placed iwith 25 kN (5to cyclic load
to delaminaof fatigue delague testing.the radius aand quickly s worth notitions were nd did not the maximum
pecimen. amination braed-beam cou
f porosity on
and refinedB specimens
efined ILTS, verage-stress ethod, MPa si)
115.1 (16.7)
109.3 (15.8)
105.7 (15.3)
109.1 (15.8)
103.3 (15.0)
112.9 (16.4)
112.0 (16.2)
113.0 (16.4)
109.3 (15.9)
113.8 (16.5)
110.4 (16.0)
3.2%
T FATIGUE
mined basedy 36-ply thickunidirectionalfatigue. Thein a uniaxial5.5 kip) loads at 0.1 loadation failure.aminations in. Fatiguearea of the
propagateding that thenot uniformnecessarily
m ILT stressSecondary
anching wereupons.
n
d s
d k l
e l
d d . n e e d e
m y s y e
Figure 11. curved-beam
The ILT peacalculated fapproximatiodeformed shcalculation [loading up fatigue testinplotting the and the intethe number ksi) static ILASTM D 64
The interlamsquares fit 12. A largenoted. Sucreliable assebased uponapproximatiohomogeneoCB test spec
Post-failure typically pasthe radius apresence ofspecimens being locateradial locati(about 2/3 ovoids on theThe porositylow, e.g. thickness-ba0.26 in3) cubcurved-beamTherefore,
Examples m fatigue test
ak stresses dfrom a closeon listed inhape of each[6] was obtaito the peak
ng. The ILTratio of the in
erlaminar tensof cycles to
T strength w15 CB tests.
minar tensilefor the powee scatter witch a poor coessment of In the ASTMon is
ous (defect-frecimens [6 – 8
CT scans sses throughrea of the CBf larger indivgives reaso
ed relatively on of maximof the thicknee delaminatioy content in tthe porosityased 6.6 x 6be volumes thm radius ait is not th
of delaminatt specimens.
during fatigueed-form geom ASTM D
h specimen, uned from thek fatigue loa S-N curve w
nterlaminar tesile strength failure. The
as generated
e S-N curveer-law are ph a low R2 vorrelation doLT fatigue m
M D 6415. this standee) anisotrop8].
showed thh the longer B specimens.vidual criticaln for the defar away fro
mal interlaminess). The pon path is shohe CB fatiguy content 6.6 x 6.6 mmhroughout threa was lehe porosity
tions in IM7/
e testing weremetric ILT s6415 [6].
used in the se initial monoad value priowas generateensile peak sagainst the lo
e 72.5 MPa d based on th
e and the lrovided in Fvalue of 0.33es not provi
material propeThe ILT s
dard assupic material in
hat delaminvoids locate
. In particula voids in seelamination com the theorenar tensile sresence of laown in Figuree specimensin the lam
m3 (0.26 x 0.e CT scans i
ess than 0.volume but
/8552
e first stress
The stress otonic or to ed by stress og of (10.5 he 10
east-igure 37 is ide a erties stress umes n the
nation ed in r, the
everal crack etical
stress arger e 11.
s was minate
.26 x n the 12%. t the
prescauspresthe Ichar
Figuthe A
The to reof thporocalcPoindistatestsstresASTthe voidmeathe mmodlocamodpeakdefecalcchardetestrestheILT normplottfailustrenaver
The in Fthanexpois mfatigappr
sence of indises the larsented in FiguILT stresses racterization.
ure 12. ILT SASTM D 641
methodologyefine the ILThe CB spec
osity in the ulation that
nt-stress andances determs were usedsses at critic
TM D 6415 IL20 curved-bs were det
asurement mmeasuremen
dels. Displal FE model
dels of the cuk fatigue loadect-free peaulating the ILracteristic disermined in Sss method, t89 μm (3.5×
stresses amalized by tted against tre to generngth values rage-stress m
ILT S-N curvigure 13. B
n 2% relative onent value
more than twicue curve basroximation.
ividual voids rge scatter ure 12. The must be inclu
S-N curve for5 stress appr
y presented S-N curve b
cimens, micrradius area,accounted f average-strmined from d to determincal voids andLT stress appbeam fatiguetected from
methods descnts were transacement bouls were genurved-beam sds. For the
ak stresses LT stresses astance from
Section 4. Sthe ILT stres×10-3 in) charat the peahe correspothe log of t
rate the ILT based on t
methods are l
ves from bothoth S-N curvdifference in determined fce the exponsed on the AThe 0.92 R2
at critical loin the fat
effects of crituded for a re
r IM7/8552 taroximation.
in Section 4 based on the ro-CT meas and the refor the pororess based c
the static cne the peak
d replace theproximation. coupons te CT scanscribed in Sesferred into lo
undary condnerated fromspecimens spoint-stress
were deteat the 19 μm
the void’s Similarly, in tsses were avracteristic disak fatigue onding ILT she number
S-N curvesthe point-streisted in Secti
h methods aves are similthe exponen
from the refinent correspoASTM D 6412 value corre
ocations thatigue resultstical voids on
eliable fatigue
ape based on
was appliedfatigue testsurements of
efined stressosity defects.characteristiccurved-beamk fatigue ILT closed-form For each of
ested, criticals using thection 4, andocal FE sub-itions in the
m the globalubject to themethod, the
ermined by(7.3×10-4 in)surface, as
the average-veraged overstance. Theloads were
strength; andof cycles tos. The ILTess and theion 4.
re presentedlar, with lessnt value. Thened method,onding to the15 ILT stressesponding to
t s n e
n
d s f s . c
m T m f l
e d -e l
e e y ) s -r e e d o T e
d s e , e s o
the point-strstress methothe R2=0.34approximatioability of thecapture theperformance
Figure 13. stress methmethod (bot
6. CONCL
This work infor porosity assessmentto the need to an accuraenable botmaintenanceunderstand performancebecome a st
CT measurecomposite element moILT strengthdefects wermeasurememodel, the sreliable matwere determ
ress method od reflect a h4 from the on. The e refined ILTe effects oe.
ILT S-N curvhod (top cuttom curve.)
LUSIONS
ntroduced strin compositet of their capafor a fundam
ate assessmeth safe ane. Technolog
their effecte could enatandard prac
ements of potest articlesdels to asses
h and fatigue re captured
ents into a scatter in theterial ILT str
mined.
and R2=0.94higher correla
ASTM D reduced sc
T stress anaof porosity
ves corresponrve) and the
ructural methe parts and enability and us
mental shift frent of part cond economigies to measts on stren
able that shictice.
orosity defec were integss the effectsbehavior. Othrough trathree-dimen
e test data wrength and f
4 to the averation compar6415 ILT s
catter reflectsalysis method
on the fa
nding to the pe average-s
hods that accnable an accseful life. It prom fleet statondition in ordical usage sure defects
ngth and faift and ultim
cts present ingrated into s of defects o
Once the effecansfer of thensional strucwas reduced;fatigue prope
rage-red to stress s the ds to
atigue
point-stress
count urate
points tistics der to
and s and atigue mately
n CB finite n the cts of e CT ctural ; and erties
ThisStan6415the Cat a D 64the Cinto the IresuIM7/rotorthe S
The propfatigcorrethe I
The becoof pIndespecdelathe candstreninhecurvpracand not tvoidand The meaappl
The charassostructestsdestsmaeffecthe and usefachiconddisp
ACK
ThisResethe grate
s work presndard D 64155 significantlyCB coupon telow volume c
415 includesCB radius ara finite elemILT material
ults of the m/8552 carbonrcraft applicaSB based ve
methodologperties was ue behavior.esponding toIM7/8552 tap
methodologome a standorosity on th
eed, porositycimens. Theamination lim
radius area didates to stungth. Althou
erent attributeved-beam tesctical value toshould be cothe porosity cs at critical locauses scatrefined CB
ans for defectlicable to vari
potential bracterize theociated noctural failure s. This wtructive inspallest voids acts on structupart conditiosize, and the
ful life are eving a funddition-based osition will be
KNOWLEDG
s work is spearch under University oefully acknow
sents a mod5 CB methody underestimest data are content. The
s measuremerea and trans
ment stress astrength prop
modified CB n/epoxy tape
ations, are in rification test
gy to deterfurther exte
. As an exao a 0.1 load pe composite
gy presenteard practice
he ILT strengy can be re
susceptibilitymits the nond
and makesudy the effecugh scatter ie of the CB ssting and an
o understandionsidered. content but tocations thattter in the st
B methodolot-tolerant desious structura
benefits of t material stn-destructivemodels exte
work shows pection is nand paramoural performaon in terms oeir influence established
damental shifstructural
e realized.
GEMENTS
ponsored by a Grant Awa
of Texas Arlwledged. Th
dification to d. The curre
mates the ILTaffected by p
e refinement ent of the critsitions defec
analysis modeperties. The tests prese
e compositeexcellent agrs.
rmine the Iended to cample, the ILratio was desystem.
ed in this for assessin
gth and fatigeadily intrody of the CB ra
destructive ins such speccts of porosityn the ILT st
specimens, thnalysis has ing the effectThis work shhe presence t reduce the trength and fgy provides
sign applicatioal configuratio
the ability toructure and
e measuremend well beythat accura
needed to qunt in deter
ance. Once kof critical deon residual , the ultimaft from statist
substanti
the US Offiard N00014-ington. Thise specimens
the ASTMent ASTM D
T strength asporosity evento the ASTMtical voids in
ct informationel to captureILT strength
nted for thee, popular inreement with
ILT materialharacterizing
LT S-N curveetermined for
work couldg the effectsue behavior.uced in CBadius area to
nspections tocimens goody on materialtrength is anhe subject ofa significant
ts of porosity,hows that it is
of individualILT strengthfatigue data. a practicalons, and it isons.
o accuratelytransfer the
ments intoyond the CBacy of non-quantify thermining theirknowledge ofefect locationstrength andate goal oftics-based toiation and
ice of Naval11-1-0916 tos support is
s used in this
M D s n M n n e h e n h
l g e r
d s .
B o o d l
n f t , s l
h . l
s
y e o B -e r f n d f o d
l o s s
work were manufactured by Bell Helicopter Textron. The authors are grateful to Mr. Edward Lee, Principal Engineer, Manufacturing R&D in this regard, and wish to thank Mr. Brian Shonkwiler, Research Associate and Ms. Paige Carpentier, PhD student, University of Texas Arlington, for their assistance with running the tests.
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The authors confirm that they, and/or their company or organization, hold copyright on all of the original material included in this paper. The authors also confirm that they have obtained permission, from the copyright holder of any third party material included in this paper, to publish it as part of their paper. The authors confirm that they give permission, or have obtained permission from the copyright holder of this paper, for the publication and distribution of this paper as part of the ERF2013 proceedings or as individual offprints from the proceedings and for inclusion in a freely accessible web-based repository.
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