Statistical Models for Analysis of Fatigue Life of Long Elements
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Transcript of Statistical Models for Analysis of Fatigue Life of Long Elements
+ model ARTICLE IN PRESS
Specimen length effect on parameter estimation in modelling
fatigue strength by Weibull distribution
Enrique Castillo a,*, Manuel Lopez-Aenlle b, Antonio Ramos b,
Alfonso Fernandez-Canteli b, Rolf Kieselbach c, Volker Esslinger c
a Department of Applied Mathematics and Computational Sciences, University of Cantabria and University of Castilla-La Mancha,
Avda. Castros sn, 39005 Santander, Spainb Department of Construction and Manufacturing Engineering, University of Oviedo, Oviedo, Spain
c EMPA, Dubendorf, Switzerland
Received 29 December 2004; received in revised form 23 November 2005; accepted 24 November 2005
Abstract
The paper deals with the problem of estimating the S–N field based on samples with different lengths and testing the hypothesis of length
independence of fatigue lifetimes. A Weibull model developed by Castillo et al. is used to discuss the problem and analyze two data samples of
prestressing wires and prestressing strands. The analysis shows that in the first case the length independence assumption cannot be accepted while
for the second case length independence seems to be a reasonable assumption. This shows that every case must be analyzed separately and that
assuming length independence can lead to unsafe design.
q 2005 Elsevier Ltd. All rights reserved.
Keywords: Weibull model; Size effect; Normalization; Censored data; Length independence analysis; Fatigue data evaluation; Staircase method; Bootstrap method
1. Introduction
The fatigue characterization of structural members or
mechanical components using the S–N field implies, unavoid-
ably, limited information, due to testing difficulties. When real
elements or components cannot be tested directly and have to
be replaced by reduced size specimens, the experimental
information obtained from the corresponding tests should be
used with caution, because these results can be strongly
dependent on the specimen size, material characteristics, and
test conditions. An extrapolation of the test results to other
conditions or sizes must be carefully done, and based on
empirical relations.
An interesting case of study is that of tendons in cable
stayed bridges, because the constituent elements of the
tendons—wires or cables—working conditions allow us to
establish a relatively simple model to derive, based on the
weakest link principle, the fatigue properties of the ensemble
from specimens much shorter than actual cables.
0142-1123/$ - see front matter q 2005 Elsevier Ltd. All rights reserved.
doi:10.1016/j.ijfatigue.2005.11.006
* Corresponding author. Tel.: C34 942201722; fax: C34 942201703.
E-mail address: [email protected] (E. Castillo).
The typical difficulty results from the material impossi-
bility of carrying out tests on specimens with actual long
lengths. One way to overcome this difficulty consists of
obtaining the fatigue resistance by testing short length
specimens and subsequently infer through extrapolation the
fatigue resistance of the real long elements. This is possible
only if a suitable model is available, which has to be based
on the weakest link model (see Fig. 1), according to which,
an element of length L can be considered to be divided into
a series of n fictitious sub-elements of small length L0, i.e.
LZnL0, and the failure occurs when the weakest sub-
element fails. Thus, the importance of performing a study
for comparing the life predictions for greater lengths based
on the theoretical model with the experimental results and
for checking the assumptions of the model, particularly the
statistical length independence assumption of the sub-
element strengths, becomes apparent.
The weakest link model may be based on statistical length
independence, asymptotic length independence, weak depen-
dence or any other assumptions related to the flaw distribution
among the different sub-elements [9]. By statistical length
independence we mean that the lifetime of different non-
overlapping pieces are statistically independent random
variables. If this property holds only for very long
International Journal of Fatigue xx (2006) 1–12
www.elsevier.com/locate/ijfatigue
Fig. 1. The weakest link model.
log N
log∆
σ βλδi
βkλkδik
β1λ1δi1
βnλnδin
β1=βk=βn=β
V
Fig. 3. S–N field showing schematically the cdfs of log N for different stress
ranges and their conversion to the normalized distribution.
Table 1
Results of the fatigue tests (in thousands of cycles) at constant stress ranges
[16]
Ds (N/mm2) Cycles
LZ140 mm LZ1960 mm LZ8540 mm
630 53, 63, 54, 73,
62
42, 48, 57
595 178
E. Castillo et al. / International Journal of Fatigue xx (2006) 1–122
+ model ARTICLE IN PRESS
non-overlapping pieces, we say that they are asymptotically
length independent.
However, in cases of not strong dependence the
asymptotic length independence assumption can be accepted
because it is supported by extreme value theory [4]. Its
application requires only the test length surpassing a
threshold length that has to be experimentally determined.
This length determines the boundary between the length
dependence and the length independence assumptions. In
such a case, the model used in the design can be notably
simplified. Consequently, in absence of a previous study, the
use of long test lengths is highly recommended with the
aim of minimizing, as much as possible, the risk of an
inappropriate extrapolation, based on the length indepen-
dence or other assumptions. Thus, the problem of length
dependence in the fatigue results is crucial and represents a
critical factor to be kept in mind in the fatigue design of
structural members. Frequently, these aspects are all ignored
what implies to consider fatigue results as length indepen-
dent. This means that accepting fatigue resistance results
obtained from short specimen lengths as valid for
considerably longer real lengths for life prediction, as it is
the case for cable stay or suspension bridges, can be
erroneous. The reasons for this worrying situation can be
found, firstly, in the insufficient statistical knowledge of the
designers, together with the lack of recognition of the
importance of the length effect on the safety of the structure
and, secondly, in the limited specimen length that can be
tested in standard test dynamic machines. It suffices to say
that fatigue studies reporting experimental results using
Fig. 2. Survival functions for different length rates L/L0Z1, 100, 1000 and N,
and range of failure probabilities implied in the extrapolation to very long
lengths from different length rates.
specimen lengths over 2 m are scarce in the literature
[11,14,16,19,20].
It is interesting to notice that carrying out tests using
larger specimen lengths [2] entails considerable advantages:
(a) lower cost due to shorter fatigue life of specimens, (b)
less runouts, (c) smaller scatter and a more reliable
estimates, and (d) more reliable extrapolation results. This
can be explained by the fact that when testing a specimen
550 377
520 321
500 404, 2000a
480 773, 849
470 332, 780, 2000a
460 626, 1082,
2000a
138
450 599, 2000a
440 473, 957, 515,
1226
430 1039, 1234
420 712, 725, 780,
1248, 2000a (4)
215
400 2000a(3)
380 300
360 281, 474, 359,
506, 364, 2000a
272, 332, 334
340 350, 619,
2000a(2)
320 512, 594, 431,
2000a
455, 49,200
300 455, 2000a(3) 909, 2000a(2)
a The limit number of cycles, 2.000, has been reached without failure.
Table 2
Model parameters according to Castillo et al. when analyzing prestressing
wires of lengths 1960 and 8540 mm
b B C l di
LZ1960 LZ8540
2.51 8.13 (3380
cycles)
18.93
(166.5 Mpa)
2.78 1.210 0.813
E. Castillo et al. / International Journal of Fatigue xx (2006) 1–12 3
+ model ARTICLE IN PRESS
of length nL0 we are really testing n pieces of length L0
(weakest link principle).
On the other side, carrying out these kind of tests with
longer specimens requires using special and more expensive
suitable equipment and testing at a lower test frequency,
due to the larger absolute oscillatory elongation of the free
length in the case of larger specimens. This involves a
slight increment of the costs for the same number of test
specimens but this number can be reduced when longer
specimens are tested. This illustrates that the optimal test
with respect to cost and reliability corresponds to long
specimens (see Fig. 2).
In all cases, including the cases of length independence or
asymptotic length independence hypotheses, the extrapolation
up to real lengths, will always be more reliable if performed
from long specimens, as it can easily be seen from Fig. 2, in
which the range of the probabilities implied in the extrapol-
ation is considerably shorter.
Note that when the length goes to infinity, the probability of
having the minimum lifetime goes to one, and this causes the
survival function to be vertical (see Fig. 2).
On the other hand, if S(x) is the survival function for a piece
of unit length and length independence is assumed, the survival
function of a specimen of length L is S(x)L. When L/N, S(x)
can only take values 0 (when S(x)!1) and 1 (when S(x)Z1).
This causes the vertical jump from 1 to 0 in Fig. 2.
It should also be borne in mind that extrapolation, although
necessary for design, is always problematic since the
theoretical results cannot be fully validated by laboratory
experiments on account of the much larger actual length of the
real structural members. In this paper, fatigue test results for
650600550
500
450
400
350
300
250
2001e+08
1e+07
1e+06
1e+05
1e+04
∆σ [
MP
a]
Number of cycles
B=8.12 (3381 Cycles) C=18.93 (166 MPa) A=2.50 D=1.21 E=–2.29
P=0.05
P=0
P=0.5
P=0.95
FailureRunout
Expected Failure
L=1960 mm
Fig. 4. S–N fields when adjusting data of prestre
prestressing wires and strands with different lengths are
analyzed by means of the model proposed by Castillo et al.
[2,9], whereby the validity of the length independence
hypothesis will be checked.
2. The model of Castillo et al.
2.1. Modelling the S–N field
The S–N field deals with two variables related to each other:
the fatigue life, N, and the stress range, Ds. The problem
consists of developing a non-linear regression model to
describe the S–N field and to estimate the model parameters.
Castillo et al. [2,9], proposed a statistical model for the analysis
of fatigue results able to consider specimens with different
lengths. The model is based on the following physical and
statistical considerations:
(1) Weakest link principle. If a longitudinal element is
divided into ‘n’ sub-elements, the fatigue life of the
whole element corresponds to the fatigue life of the
weakest element.
(2) Stability. The cumulative distribution function (cdf)
model must be applicable to different lengths.
(3) Limit value. The cdf should encompass extreme lengths,
i.e. the case of a length going to infinity. Thus, the cdf
must belong to a family of asymptotic functions.
(4) Limited range of the random variables involved. The
variables Ds and N have a lower bound.
(5) Compatibility. The cdf related to the stress range E(N,
Ds) must be compatible with the cdf related to the fatigue
life F(Ds, N). The Weibull distributions fulfill the
requirements 1–4 and can be applied here.
The last condition allows us to establish a functional
equation. (see [1,3,5,9]) the solution of which leads, without
additional requirements to the following model for the cdf of
the fatigue life N at the stress range Dsk
FðlogN;DskÞZ1Kexp KLi
L0
ðlogNKBÞðlogDskKCÞ
DCE
� �A� �; (1)
650600550
500
450
400
350
300
250
2001e+08
1e+07
1e+06
1e+05
1e+04
∆σ [
MP
a]
Number of cycles
B=8.125 (3381 Cycles) C=18.93 (166 MPa) A=2.50 D=0.81 E=–3.42
P=0.05
P=0
P=0.5
P=0.95
FailureRunout
Expected Failure
L=8540 mm
ssing wires of lengths 1960 and 8540 mm.
0
0.2
0.4
0.6
0.8
1
2.5 3 3.5 4 4.5 5 5.5
P
V
Weibull distribution:β=2.51, δ=1.21, λ=2.78
L=1960 mm
∆σ=630 [MPa]∆σ=460 [MPa]∆σ=420 [MPa]∆σ=380 [MPa]∆σ=360 [MPa]
∆σ=340 [MPa]∆σ=320 [MPa]∆σ=300 [MPa]∆σ=260 [MPa]
0
0.2
0.4
0.6
0.8
1
2.5 3 3.5 4 4.5
P
V
Weibull distribution:β=2.51, δ=0.81, λ=2.78
L=8540 mm
∆σ=630 [MPa]∆σ=360 [MPa]∆σ=320 [MPa]∆σ=300 [MPa]∆σ=280 [MPa]
Fig. 5. Cdfs when adjusting data of prestressing wires of lengths 1960 and 8540 mm.
Table 3
Check of the length independence assumption when analyzing prestressing
wires of lengths 1960 and 8540 mm
Length (mm) dI
Estimate Length indepen-
dence assump-
tion
95%-confidence
interval
1960 1.21 1.21 [0.75, 3.60]
8540 0.813 0.673 [0.32, 2.79]
Reference length LZ1960 mm.
Table 4
Kolmogorov–Smirnov test when analyzing data of prestressing wires of lengths
1960 and 8540 mm
Length (mm) Kolmogorov–Smirnov test
K–S statistic Significance level (%)
1960 0.134 9.85
8540 0.113 69.75
Table 5
Model parameters according to Castillo et al. when analyzing data of
prestressing wires of lengths 140, 1960 and 8540 mm
b B C l di
LZ140
LZ1960
LZ8540
3.86 9.70
(16271
cycles)
19.31
(229.78 Mpa)
0.649 2.329 0.934 0.608
E. Castillo et al. / International Journal of Fatigue xx (2006) 1–124
+ model ARTICLE IN PRESS
where N is the fatigue life measured in cycles, Dsk is the stress range,
PZF(log N; Dsk) is the probability of failure, L0 is the reference
length, Li is the specimen length and A, B, C, D and E are the
parameters to be estimated with the following meaning:
A shape parameter of the Weibull distribution.
B Threshold value for N or limit number of cycles.
C Threshold value for Ds or endurance limit.
D scale parameter.
E Parameter fixing the position of the limit curve or zero
probability curve.
This S–N field, which isoprobability curves, i.e. the curves joining
points with the same probability of failure, are equilateral hyperbolas,
allows the probabilistic prediction of fatigue failure under constant
amplitude loading.
From expression (1) one can identify the parameters of the
normalized Weibull distribution
FðN;DskÞZ1Kexp KLi
L0
VKlk
dik
� �bk
at the stress range Dsk with the model parameters A, B, C, D
and E:
lðDskÞZBKED
logDskKC;dðDskÞZ
D
logDskKC
L0
Li
� �1=A
;
bðDskÞZA;FðlogN;logDskÞZf ðl;d;bÞ:
(2)
Then, it becomes apparent that the location, l(Dsk), and the
shape, b(Dsk), parameters are not length dependent, which
implies that the zero probability curve is the same for all
lengths. The scale parameter d(Dsk) is the only length
dependent parameter. Considering two lengths L1 and L2, for
the same stress range Dsk we obtain
dðL1Þ
dðL2ÞZ
DlogDskKC
L0
L1
� �1=A
DlogDskKC
L0
L2
� �1=AZ
L2
L1
� �1=A
5dðL1Þ
ZdðL2ÞL2
L1
� �1=A
; (3)
an expression that establishes the relation that must exist
between the scale parameters if length independence holds.
650600550
500
450
400
350
300
250
200 1e+09
1e+08
1e+07
1e+06
1e+05
1e+04
∆σ [
MP
a]
Number of cycles
B=9.70 (16271 Cycles) C=19.25 (229 MPa) A=3.86 D=2.33 E=–0.28
P=0.05
P=0
P=0.5
P=0.95
L=140 mm
FailureRunout
Expected Failure
650600550
500
450
400
350
300
250
200 1e+09
1e+08
1e+07
1e+06
1e+05
1e+04
∆σ [
MP
a]
Number of cycles
B=9.70 (16271 Cycles) C=19.25 (229 MPa) A=3.86 D=0.93 E=–0.69
P=0.05
P=0
P=0.5P=0.95
L=1960 mm
FailureRunout
Expected Failure
0
0.2
0.4
0.6
0.8
1
0.8 1 1.2 1.4 1.6 1.8 2 2.2 2.4
P
V
Weibull distribution:β=3.86, δ=0.93, λ=0.65
L=1960 mm
∆σ=630 [MPa]∆σ=460 [MPa]∆σ=420 [MPa]∆σ=380 [MPa]∆σ=360 [MPa]∆σ=340 [MPa]∆σ=320 [MPa]∆σ=300 [MPa]∆σ=260 [MPa]
650600550
500
450
400
350
300
250
200 1e+09
1e+08
1e+07
1e+06
1e+05
1e+04
∆σ [
MP
a]
Number of cycles
B=9.70 (16271 Cycles) C=19.25 (229 MPa) A=3.86 D=0.61 E=–1.06
P=0.05
P=0
P=0.5P=0.95
L=8540 mm
FailureRunout
Expected Failure
0
0.2
0.4
0.6
0.8
1
0.8 0.9 1 1.1 1.2 1.3 1.4 1.5 1.6
P
V
Weibull distribution:β=3.855, δ=0.608, λ=0.649
L=8540 mm
∆σ=630 [MPa]∆σ=360 [MPa]∆σ=320 [MPa]∆σ=300 [MPa]∆σ=280 [MPa]
0
0.2
0.4
0.6
0.8
1
0.5 1 1.5 2 2.5 3 3.5 4 4.5
P
V
Weibull distribution: β=3.86, δ=2.33, λ=0.65
L=140 mm
∆σ=595 [MPa]∆σ=550 [MPa]∆σ=520 [MPa]∆σ=500 [MPa]∆σ=480 [MPa]∆σ=470 [MPa]∆σ=460 [MPa]∆σ=450 [MPa]∆σ=440 [MPa]∆σ=430 [MPa]∆σ=420 [MPa]∆σ=400 [MPa]
Fig. 6. Left graphs: S–N fields when adjusting data of prestressing wires of lengths 140, 1960 and 8540 mm. Right graphs: cdfs for normalized results when adjusting
data of prestressing wires of lengths 140, 1960 and 8540 mm.
Table 6
Test of the length independence assumption when analyzing data of
prestressing wires of lengths 140, 1960 and 8540 mm
Length (mm) di
Estimate Length indepen-
dence assump-
tion
95%-confidence
interval
E. Castillo et al. / International Journal of Fatigue xx (2006) 1–12 5
+ model ARTICLE IN PRESS
2.2. Parameter estimation
The model allows, in a first step, the estimation of B and C
which are the hyperbolas asymptotes in the model. Next, in a
second step, the other parameters A, D and E can be estimated.
Taking into account that the mean value of the Weibull
distribution is mZlCdG 1Cð1=bÞð Þ, from expression (1) one
obtains
140 2.329 1.850 [1.516, 3.045]
1960 0.934 0.934 [0.650, 1.863]
8540 0.608 0.638 [0.380, 1.547]
Reference length LZ1960 mm.
ðmkKBÞðlogDskKCÞZKEDCDG 1C1
A
� �L0
Li
� �1=A
ZKi; (4)
Table 7
Model parameters according to Castillo et al. when analyzing data of
prestressing wires of lengths 140, 1960 and 8540 mm
Length (mm) Kolmogorov–Smirnov test
K–S statistic Significance level (%)
140 0.155 3.26
1960 0.180 5.27
8540 0.112 60.63
Table 8
Comparison between the stress level at 2!106 cycles (endurance limit)
calculated according to the model of Castillo et al. and the staircase method for
50% probability of failure
Length (mm) Ds (Mpa)
Castillo’s model
Using 1960 and
8540 mm
Using 140, 1960
and 8540 mm
Staircase
method [13]
140 – 410 420
1960 305 315 330
8540 290 295 305
E. Castillo et al. / International Journal of Fatigue xx (2006) 1–126
+ model ARTICLE IN PRESS
where Ki, the expression between the two equality signs in (4),
is a length dependent constant, and mk is the mean value of
log N at stress range Dsk. This means that for every length the
probability curve associated with the mean value is also
represented by a hyperbola. Expression (4) suggests to estimate
first B and C by minimizing
QðB;C;K1;.;KtÞZXt
iZ1
Xn
kZ1
Xm
jZ1
logNikjKBKKi
logDskKC
� �2
(5)
with respect to B, C and K1, K2,., Kt, where t is the number of
different lengths considered here, n is the number of stress
ranges and m the number of tests conducted at each stress
range. Once the values of the parameters B and C are known,
Eq. (1) becomes a three parameter Weibull distribution and A,
D and E can be estimated by standard methods thanks to the
fact that results for different stress ranges and lengths can be
statistically normalized.
The model allows us to pool all the fatigue data points for
different stress ranges, into a unique population (stress range).
Note that all them belong to Weibull distributions with the
Table 9
Fatigue test results (in thousands of cycles) for prestressing strands for constant am
Ds (N/mm2) Cycles
LZ490 mm LZ1100 mm
630 56, 60, 62, 67, 84 59, 62, 64, 70, 7
460 95, 103, 106, 11
300 576, 727
290 1292, 2000a(4) 467, 494, 625, 1
(4)
280 513, 674, 2000a(
270 384, 989, 2000a
260 2000a(2)
250
230
a The limit number of cycles, 2.000, has been reached without failure.
same shape parameter, b, but different parameters for location
(l), and scale (d). This is called statistical normalization of the
S–N field (see Fig. 3). This procedure is based on the fact that
the Weibull distributions remains stable with respect to
location and scale transformations, that is, if a variable X
follows a Weibull distribution, W(b, d, l), that is denoted
XwW(b, d, l), and it is transformed by ZZ(XKa)/b, where a
and b are real constants, then ZwWðððlKaÞ=bÞ;ðd=bÞ;bÞ, i.e.
another Weibull distribution is obtained. The normalizing
process helps to overcome the limitation of the low number of
specimens tested at each different test level [9]. Thus, in the
evaluation of the Weibull parameters all the specimens are
pooled together, so that we have a larger sample size and then,
a better reliability of the evaluation is thus achieved.
Since unfortunately fatigue tests are scarce, costly and
lengthy normally available fatigue samples are small.
However, the model allows us using all the data lengths, i.e.
pooled together. This reduces the problem because then the
effective sample size is the sum of the sample sizes for all
lengths.
When the former transformation is applied to the fatigue
case, X is used to denote the original variable, that is the
number of cycles to failure, and Z is used to denote the
normalized variable. Different normalizations can be done,
simply, by assigning different values to the parameters a and b.
One possible normalized variable, denoted as V, can be defined
as VZ(log NKB)(log DsKC), that allows us to pool all the
data together as if they were tested at the same stress level.
Provided that the variable log N for the length Li follows a
Weibull distribution W(lk, dik, bk) at the stress range k, the
Weibull cdf for the new variable V is given by:
FðV;l;di;bÞZ1Kexp KVKl
di
� �b" #
(6)
Here, the normalized parameters l, di and b can be expressed
as a function of the model parameters, as lZKED,
diZDL0
Li
� �1=A
, bZA. Once l, d1, d2,.,dt and b are known,
the model parameters A, D and E can be calculated. It becomes
apparent that the parameters D and E depend of the reference
length. The estimation of l, d1, d2,.,dt and bmay succeed using
plitude loading [11]
LZ1960 mm LZ3860 mm
1 50, 57, 59, 65, 67 51, 63, 65, 74
5, 189
376, 508
294, 2000a 287, 309, 347, 440, 614 374, 696, 749, 2000a
3) 1984, 2000a
359, 870, 2000a
909, 2000a(2)
2000a
Table 10
Model parameters according to Castillo et al. when analyzing strands of lengths
1100, 1960 and 3860 mm
b B C l di
1100 LZ1960
LZ3860
2.73 9.23
(10174 -
cycles)
18.92
(164.19
Mpa)
1.61 1.032 0.824 0.923
650600550500
450
400
350
300
250
200
1e+09
1e+08
1e+07
1e+06
1e+05
1e+04
∆σ [
MP
a]
Number of cycles
B=9.22 (10174 Cycles) C=18.92 (164 MPa), A=2.72, D=1.03, E=–1.57
P=0.05
P=0
P=0.5P=0.95
L=1100 mm
FailureRunout
Expected Failure
650600550500
450
400
350
300
250
200
1e+09
1e+08
1e+07
1e+06
1e+05
1e+04
∆σ [
MP
a]
Number of cycles
B=9.23 (10174 Cycles) C=18.92 (164 MPa) A=2.72 D=0.84 E=–1.95
P=0.05
P=0
P=0.5P=0.95
L=1960 mm
FailureRunout
Expected Failure
650600550500
450
400
350
300
250
200
1e+09
1e+08
1e+07
1e+06
1e+05
1e+04
∆σ [
MP
a]
Number of cycles
B=9.23 (10174 Cycles) C=18.92 (164 MPa) A=2.72 D=0.92 E=–1.74
P=0.05
P=0
P=0.5P=0.95
L=3860 mm
FailureRunout
Expected Failure
Fig. 7. Left graphs: S–N fields when adjusting data of prestressing strands of lengths 1
data of prestressing wires of lengths 1100, 1960 and 3860 mm.
E. Castillo et al. / International Journal of Fatigue xx (2006) 1–12 7
+ model ARTICLE IN PRESS
the maximum likelihood method [7,8,18]. Since the probability
density function (pdf) of a Weibull distribution is given by
f ðV ;l;d;bÞZexp KVKl
di
� �b" #
b1
di
VKl
di
� �bK1
; (7)
the value of the parameters l, d1, d2,.,dt and b can be obtained
by maximizing with respect to l, d1, d2,.,dt and b the
loglikelihood of the sample:
0
0.2
0.4
0.6
0.8
1
1.6 1.8 2 2.2 2.4 2.6 2.8 3 3.2
P
V
Weibull distributionβ=2.73, δ=0.82, λ=1.61
L=1960 mm
∆σ=630 [MPa]∆σ=300 [MPa]∆σ=290 [MPa]∆σ=280 [MPa]
V
0
0.2
0.4
0.6
0.8
1
1.6 1.8 2 2.2 2.4 2.6 2.8 3 3.2 3.4
P
Weibull distribution:β=2.73, δ=1.03, λ=1.61
L=1100 mm
∆σ=630 [MPa]∆σ=460 [MPa]∆σ=300 [MPa]∆σ=290 [MPa]∆σ=280 [MPa]∆σ=270 [MPa]∆σ=260 [MPa]
0
0.2
0.4
0.6
0.8
1
1.6 1.8 2 2.2 2.4 2.6 2.8 3 3.2 3.4
P
V
Weibull distribution: β=2.73, δ=0.92, λ=1.61
L=3860 mm
∆σ=630 [MPa]∆σ=290 [MPa]∆σ=270 [MPa]∆σ=250 [MPa]∆σ=230 [MPa]
100, 1960 and 3860 mm. Right graphs: cdfs for normalized data when adjusting
Table 11
Check of the length independence assumption when analyzing data of
prestressing strands of lengths 1100, 1960 and 3860 mm
Length (mm) di
Estimate Length indepen-
dence assump-
tion
95%-confidence
interval
1100 1.030 1.030 [0.615, 2.538]
1960 0.824 0.834 [0.481, 2.339]
3860 0.923 0.650 [0.314, 2.014]
Reference length LZ1960 mm.
Table 12
Kolmogorov–Smirnov test when analyzing data of prestressing strands of
lengths 1100, 1960 and 3860 mm
Length (mm) Kolmogorov–Smirnov test
K–S statistic Significance level (%)
1100 0.191 64.18
1960 0.135 52.73
3860 0.118 63.18
Reference length LZ1960 mm.
Table 13
Model parameters according to Castillo et al. when analyzing data of
prestressing strands of lengths 490, 1100, 1960 and 3860 mm
b B C l di
LZ490
LZ1100
LZ1960
LZ3860
3.2 10.31
(28608
cycles)
19.23
(220.
2 Mpa)
0.339 0.891 0.651 0.513 0.537
E. Castillo et al. / International Journal of Fatigue xx (2006) 1–128
+ model ARTICLE IN PRESS
LZKXn
iZ1
ViKl
di
� �b
CðbK1ÞXn
iZ1
logViKl
di
� �Cnlogb
KXn
iZ1
logdi: (8)
The application of this procedure does not require the
assumption (3), related to the length independence assumption.
Nevertheless, once the parameters are estimated the length
independence assumption can be checked. Other methods for
the estimation of the model parameters have been developed by
Castillo et al. [7,8]. However, since the aim of the paper is to
study the length effect, the estimation method is not the main
point in the paper and any good estimation method can be used.
2.3. The case of censored data (runouts)
Experimental programs in fatigue usually involve the presence
of censored data, i.e. tests interrupted before failure of the
specimen occurs, due to accidental causes or because the limit
number of cycles has been reached. This type of data is called
censored data or runouts. In such cases, it is possible to resort to
specific statistical techniques, as for instance the E–M algorithm,
based on an iterative process to deal with these censored data in
the statistical analysis. This technique consists of:
(1) Estimate the model parameters considering only the results
associated with failures.
(2) Assign to the censored results their expected failure values,
based on the estimated model parameters.
(3) Re-estimate the model parameters but considering the data
associated with real failures plus the expected ones
associated with the runouts.
(4) Repeat steps 2 and 3 until convergence of the process.
For a limit number of cycles N0, the normalized variable for
runouts will be
V0ZðlogN0KBÞðlogDsKCÞ; (9)
and since the Weibull distribution for VRV0 is
FðVjvRV0ÞZ1Kexp KV0Kl
di
� �b
KVKl
di
� �b" #
;
VjvRV0;
(10)
and the expected value of the rth order statistic of a sample of
size q from an uniform distribution U(0,1) is r/(qC1), the
censored result V0 can be replaced by the V solutions, obtained
from
1Kexp KV0Kl
di
� �b
KVKl
di
� �b" #
Zr
qiC1;
rZ1;2;.;qi;
(11)
where qi is the number of runouts coinciding at the same stress
range, Dsk, and the same limit number of cycles, N for rZ1,
2,.,qi. Thus:
VZlCdi
V0Kl
di
� �b
Klog 1Kr
qiC1
� �" #;
rZ1;2;.;qi:
(12)
3. Examples of application of the proposed method
3.1. Prestressing wires
With the aim of validating the model for analyzing the
influence of the specimen length, the results of an experimental
fatigue program, carried out on prestressing wires with different
lengths [16] at the EMPA (Swiss Federal Testing and Materials
Laboratory), in Dubendorf (Switzerland), were evaluated. The
nominal value of the tensile strength of this material was RmZ1700 MPa. All the tests were conducted under constant
amplitude loading using specimens with three different lengths,
E. Castillo et al. / International Journal of Fatigue xx (2006) 1–12 9
+ model ARTICLE IN PRESS
140, 1960 and 8540 mm, where the stress ranges and resulting
fatigue life in cycles are shown in Table 1.
For parameter estimation the techniques described in Section
2 were applied. The GAMS tool [6,18] was used to solve the
optimization problem. Initially, only the specimens with lengths
1960 and 8540 mm were considered in the analysis. The
parameter estimates are shown in Table 2.
Figs. 4 and 5 represent, respectively, the S–N field for each of
the two lengths studied and the cdf associated with the
normalized variable V. Assuming that the length independence
hypothesis is satisfied and taking as reference length that of
1960 mm, it is possible to calculate the value of the d parameter
associated with the length 8540 mm as d8540Zd1960(1960/8540)1/2.51Z0.673 as represented in Table 3. A
certain discrepancy can be observed between the value directly
estimated and the one resulting from the length independence
assumption. The validity of the length independence hypothesis
was checked using the bootstrap technique [10,12,15]. Thousand
bootstrap simulations were performed considering the par-
ameters in Table 2 for LZ1960 mm and using the length
independence assumption for LZ8540 mm. Thus, 1000 values
of d were simulated for every length and thousand values of the
Kolmogorov–Smirnov statistic were obtained. The 95%
confidence interval for the d estimates and for the Kolmo-
gorov–Smirnov statistic is included in Tables 3 and 4,
respectively.
650600550
500
450
400
350
300
250
200 1e+1
1e+09
1e+08
1e+07
1e+06
1e+05
1e+04
∆σ [
MP
a]
Number of cycles
B=10.26 (28575 Cycles) C=19.20 (220 MPa) A=3.2 D=0.89 E=–0.38
P=0.05
P=0
P=0.5P=0.95
L=490 mm
FailureRunout
Expected Failure
650600550
500
450
400
350
300
250
200 1e+09
1e+08
1e+07
1e+06
1e+05
1e+04
∆σ [
MP
a]
Number of cycles
B=10.26 (28575 Cycles) C=19.20 (220 MPa) A=3.2 D=0.53 E=–0.66
P=0.05
P=0
P=0.5P=0.95
L=1960 mm
FailureRunout
Expected Failure
Fig. 8. S–N fields when adjusting data of prestressing wires of lengths (f
From Table 3, it can be observed that the d estimates fall
inside the 95% confidence interval of the feasible values. Thus, it
can be assumed that the test results fulfill the length
independence assumption. This can also be verified by means
of the Kolmogorov–Smirnov test. For the length 1960 mm a
significance level of 9.85% was obtained, while it was 69.75% in
the case of a length 8540 mm. Consequently, the length
independence assumption can be accepted for a 5% significance
level, and then it can be concluded that the length independence
assumption can be used for extrapolation purposes from 1960 to
8540 mm, and therefore they can be jointly analyzed. Finally, all
the lengths 140, 1960 and 8540 mm, were analyzed together
giving the estimates in Table 5.
Fig. 6 represents the S–N fields on the left, and the cdfs,
associated with the normalized variable V for each of the lengths
on the right.
Table 6 shows the parameter estimates associated with
lengths 140 and 8540 mm when the length independence
assumption is assumed to hold and the reference length is
1960 mm. The results obtained from the simulations performed
by the bootstrap method are shown in Tables 6 and 7. It can be
noticed that the d estimates for lengths 1960 and 8540 mm fall
inside the 95% confidence interval. Table 7 shows the results
obtained by the Kolmogorov–Smirnov test. The estimate
corresponding to 140 mm cannot be accepted for a 5%
significance level. Thus, the consideration of this length in the
650600550
500
450
400
350
300
250
200 1e+09
1e+08
1e+07
1e+06
1e+05
1e+04
∆σ [
MP
a]
Number of cycles
B=10.26 (28575 Cycles) C=19.20 (220 MPa) A=3.2 D=0.65 E=–0.52
P=0.05
P=0
P=0.5P=0.95
L=1100 mm
FailureRunout
Expected Failure
650600550
500
450
400
350
300
250
200 1e+09
1e+08
1e+07
1e+06
1e+05
1e+04
∆σ [
MP
a]
Number of cycles
B=10.26 (28575 Cycles) C=19.20 (220 MPa) A=3.2 D=0.53 E=–0.66
P=0.05
P=0
P=0.5P=0.95
L=3860 mm
FailureRunout
Exp. Failure
rom left to right and top to bottom) 490, 1100, 1960 and 3860 mm.
0
0.2
0.4
0.6
0.8
1
0.4 0.6 0.8 1 1.2 1.4 1.6 1.8
P
V
Weibull distribution:β=3.20, δ=0.89, λ=0.34
L=140 mm
∆σ=630 [MPa]∆σ=290 [MPa]
0
0.2
0.4
0.6
0.8
1
0.4 0.6 0.8 1 1.2 1.4
P
V
Weibull distribution:β=3.20, δ=0.65, λ=0.34
L=1100 mm
∆σ=630 [MPa]∆σ=460 [MPa]∆σ=300 [MPa]∆σ=290 [MPa]∆σ=280 [MPa]∆σ=270 [MPa]∆σ=260 [MPa]
0
0.2
0.4
0.6
0.8
1
0.4 0.5 0.6 0.7 0.8 0.9 1 1.1 1.2 1.3
P
V
Weibull distribution:β=3.20, δ=0.51, λ=0.34
L=1960 mm
∆σ=630 [MPa]∆σ=300 [MPa]∆σ=290 [MPa]∆σ=280 [MPa]
0
0.2
0.4
0.6
0.8
1
0.4 0.6 0.8 1 1.2
P
V
Weibull distribution:β=3.20, δ=0.54, λ=0.34
L=3860 mm
∆σ=630 [MPa]∆σ=290 [MPa]∆σ=270 [MPa]∆σ=250 [MPa]∆σ=230 [MPa]
Fig. 9. Cdfs when adjusting data of prestressing strands of lengths 490, 1100, 1960 and 3860 mm.
Table 14
Check of the length independence assumption when analyzing data of
prestressing strands of lengths 490, 1100, 1960 and 3860 mm
Length (mm) di
Estimate Length indepen-
dence assump-
tion
95%-confidence
interval
490 0.891 0.838 [0.777, 5.430]
1100 0.651 0.651 [0.643, 5.196]
1960 0.513 0.544 [0.563, 4.974]
3860 0.537 0.4398 [0.415, 4.881]
Reference length: LZ1960 mm.
E. Castillo et al. / International Journal of Fatigue xx (2006) 1–1210
+ model ARTICLE IN PRESS
joint analysis is not in line with the results for the other lengths
leading to a reduction of the significance level of these.
Therefore, it can be concluded that the results corresponding
to the 140 mm specimens do not fulfill the length independence
assumption. Nevertheless, it should be said that since 140 mm is
a fairly short length, the determination of the real free length of
the specimens is not exempt from error. Moreover, as mentioned
above, the test strategy adopted, rather oriented to the staircase
method, due to the lack of a suitable model at the time when the
tests were planned, caused an irregular distribution of the results
all over the S–N field and a high number of runouts relative to
the total number of data points. Finally, it should be also added
that the frequency resulting for testing the length 140 mm was
133 Hz, considerably higher than the frequencies used for the
remaining lengths 1960 and 8540 mm (6 and 0.4 Hz, respect-
ively). Table 8 illustrates a comparison between the values of the
endurance limit calculated for 50% probability of failure at 2!106 cycles using the model of Castillo et al. and the staircase
method (see [13,16,17]). In the light of these results, it can be
concluded that the results from the model proposed by Castillo et
al. show a good agreement with the results furnished by the
staircase method. Moreover, the former brings additional
advantages, since it allows us to calculate, for given probability
of failure, the number of cycles to failure for whatever stress
level all over the whole S–N field, including the possibility of
extrapolation concerning cycles or test lengths, something that is
not possible for the staircase method.
3.2. Prestressing strands
The study of fatigue of prestressing wires was then extended
to prestressing strands from the same experimental program
conducted at the Swiss Federal Testing and Materials
Laboratory EMPA in Dubendorf, Zurich (Switzerland) [16].
The nominal value of the tensile strength of this material was
RmZ1800 MPa. All the tests were conducted under constant
amplitude loading using four different lengths: 490, 1100, 1960
and 3860 mm, as shown in Table 9. The program strategy, as in
the case of prestressing wires, was focussed to the application of
the staircase method for determining the endurance limit. Also
here, the results are predominantly gathered in the lower part of
the S–N field with the same consequences as before. The
Table 15
Kolmogorov–Smirnov test when analyzing data of prestressing strands of
lengths 490, 1100, 1960 and 3860 mm
Length (mm) Kolmogorov–Smirnov test
K–S statistic Significance level (%)
490 0.158 59.45
1100 0.0934 60.55
1960 0.0965 87.05
3860 0.0838 89.25
Reference length LZ1960 mm.
Table 16
Comparison between the stress level at 2!106 cycles (endurance limit)
calculated according to the model of Castillo et al. and the staircase method for
50% probability of failure
Length (mm) Ds (MPa)
Castillo’s model
Using 1100,
1960 and
3860 mm
Using 490, 1100,
1960 and
3860 mm
Staircase
method [13]
490 – 290 –
1100 285 273 280
1960 270 265 260
3860 260 268 –
E. Castillo et al. / International Journal of Fatigue xx (2006) 1–12 11
+ model ARTICLE IN PRESS
procedure described in Section 2 was applied for the parameter
estimation. Initially, test lengths of 1100, 1960 and 3860 mm
were considered in the analysis. The parameter estimates are
shown in Table 10. Fig. 7 represents the S–N field for each one
of the lengths studied and the cdf associated with the variable V,
respectively.
The values of the d parameter associated with test lengths
1100 and 3860 mm assuming length independence are shown in
Table 11 where 1960 mm has been taken as the reference length.
The estimate falls inside the 95% confidence interval for all the
lengths. Table 12 represents the results of the Kolmogorov–
Smirnov test. As can be seen all the estimates can be accepted at
5% significance levels. Then it can be concluded that the results
for the three lengths fulfill the length independence assumption
and therefore can be jointly analyzed.
Subsequently, a joint analysis considering all the lengths 490,
1100, 1960 and 3860 mm was undertaken. The resulting
parameters are shown in Table 13.
Figs. 8 and 9, represent the S–N field and the cdfs associated
to the variable V for each of the lengths, respectively.
As it can be observed, the quality of the adjustment for the S–
N field, as well as for the cdfs is acceptable for the four specimen
lengths, although, considering the low number of results related
to the shortest length, it seems risky to establish conclusions
concerning this length.
From Table 14, it can be observed that the d parameter
estimate falls inside the 50 and 95% confidence intervals of the
acceptable values. Thus, the test results confirm the length
independence assumption. This can be also verified by means of
the Kolmogorov–Smirnov test. Table 14 shows the results
obtained for the parameter d associated with lengths 490, 1960
and 3860 mm, assuming length independence and taken
1100 mm as the reference length. The result obtained for length
1960 mm is the only one that falls outside the 95% confidence
interval. Again, it can be verified that the presence of results that
do not fulfill the length independence assumption is not in line
with the adjustment of the rest of the results. In order to check
the quality of the estimate the results of the Kolmogorov–
Smirnov test are shown in Table 15. All of them can be accepted
for a 5% significance level.
It can be summarized that the four studied lengths cannot be
jointly analyzed, since they do not fulfill the length indepen-
dence assumption. This could be due to the fact that the length
490 mm is below the length independence threshold length, or,
that the number of results available related to this length is too
small and is concentrated in only two different stress levels.
Table 16 illustrates a comparison between the values of
the endurance limit calculated for 50% probability of failure
at 2!106 cycles using the model of Castillo et al. and the
staircase method [13,16,17]. This demonstrates a good
correspondence between both methods and the same
comments, expressed at the end of Section 3.1 are pertinent
here again.
4. Conclusions
The main conclusions of this work are the following:
(1) The applicability of the model proposed by Castillo et al.
for determining the S–N field of two different types of
prestressing steels, wires and strands, including different
lengths have been studied. The model allows us to
determine the S–N curves for both materials for different
probabilities of failure and different confidence intervals
by considering a relatively reduced number of tests even
if the test plan, set up in the absence of a general
regression model at the time of the research made, is far
from being optimal. The potential of the model of
Castillo et al. enabling to establish an adequate test
strategy is being developed at present by the authors.
(2) A methodology to check the length independence
hypothesis, based on the bootstrap technique, is proposed
here. This can be applied to determine the threshold
length, above which the length independence assumption
can be accepted. The analysis shows that the length
independence assumption cannot be accepted for the
prestressing wires data, while it is a reasonable
assumption for the prestressing strands data.
(3) The Kolmogorov–Smirnov test has been successfully
applied to check the quality of the adjustment.
(4) The results of the endurance limit, obtained using the
model of Castillo et al. and the staircase method are
compared here. A good agreement has been obtained.
Nevertheless, the superiority of the model presented here
is obvious since it allows us to calculate, for a given
probability of failure, the number of cycles to failure for
any stress level, all over the whole S–N field, and
additionally it makes feasible an extrapolation concerning
E. Castillo et al. / International Journal of Fatigue xx (2006) 1–1212
+ model ARTICLE IN PRESS
cycles or test lengths, which is outside the capacities of
the staircase method.
References
[1] Aczel J. Lectures in functional equations and their applications.
Mathematics in science and engineering, vol. 19. London: Academic
Press; 1966.
[2] Castillo E, Fernandez Canteli A, Esslinger V, Thurlimann, B. Statistical
model for fatigue analysis of wires, strands and cables. IABSE proceedings,
1985. p.82–5.
[3] Castillo E, Galambos J. Lifetime regression models based on a functional
equation of physical nature. J Appl Probab 1987;24:160–9.
[4] Castillo E, Hadi AS, Balakrishnan N, Sarabia, JM. Extreme values and
related models with applications in engineering and science. Wiley series in
probability and statistics; 2005.
[5] Castillo E, Iglesias A, Ruiz-Cobo MR. Functional equations in applied
sciences. Mathematics in science and engineering, vol. 199. Amsterdam:
Elsevier; 2005.
[6] Castillo E, Conejo A, Pedregal P, Garcia R, Alguacil N. Building and
solving mathematical programming models in engineering and science.
London: Wiley; 2001.
[7] Castillo E, Hadi AS. Modeling lifetime data with application to fatigue
models. J Am Stat Assoc 1995;90(4311):1041–54.
[8] Castillo E, Fernandez Canteli A, Hadi AS. On fitting a fatigue model to
data. Int J Fatigue 1999;21:97–106.
[9] Castillo E, Fernandez Canteli A. A general regression model for lifetime
evaluation and prediction. Int J Fract 2001;107:117–37.
[10] Chernick MR. Bootstrap methods. Wiley series in probability and statistics.
London: Wiley; 1999.
[11] Cullimore MSG. The fatigue strength of high tensile wire cable subjected to
stress fluctuations of small amplitude. Memoires Assoc Int de Ponts et
Charpentes 1976;32(1):49–56.
[12] Davison AC, Hinkley DV. Bootstrap methods and their application.
Cambridge series in statistical and probabilistic mathematics; 1997.
[13] Dixon WJ, Massey Jr FJ. Introduction to statistical analysis. 3rd ed. NY,
USA: McGraw-Hill; 1969.
[14] Edwards AD, Picard A. Fatigue characteristics of prestressing strand. Proc
Inst Civ Eng 1972;53:323–36.
[15] Efron B, Tibshirami RJ. An introduction to the bootstrap. London/Boca
Raton: Chapman & Hall/CRC; 1993.
[16] Fernandez Canteli A, Esslinger V, Thurlimann B. Ermudungsfestigkeit von
Bewehrungs- und Spannstahlen. Bericht Nr. 8002-1, Institut fur Baustatik
und Konstruktion, ETH Zurich; 1984.
[17] Huck M, Schutz W, Zenner HM. Ansatz und Auswertung von
Treppenstufenversuchen im Dauerfestigkeitsbereich. Industrieanlagen —
Betriebsgesellschaft mbH, Bericht b-TF-742B; February 1978.
[18] Lopez Aenlle M. Fatigue characterization of composites subject to random
and block loading (in Spanish). Doctoral thesis, University of Oviedo; 2000.
[19] Tide RHR, van Horn DA. A statistical study of the static and fatigue
properties of high strength prestressing strand. Fritz Eng. Laboratory.
Report No. 309.2, Lehigh University; June 1966.
[20] Warner RF, Hulsbos CL. Fatigue properties of prestressing strand. PCI J
1966;11(2):25–46.