Journal of Statistical Theory and Applications

Volume 17, Issue 2, June 2018, Pages 340 - 358

Joint Modeling of Linear Degradation and Multiple Dependent Competing Risks Data under a Step-Stress Accelerated Degradation Test

Department of Statistics, Faculty of Mathematical Sciences, Shahid Beheshti University, Tehran, Iran
Ahmad Khodadadi*,
Department of Statistics, Faculty of Mathematical Sciences, Shahid Beheshti University, Tehran, Iran
Department of Statistics, Faculty of Mathematics, Statistics and Computer Sciences, Tehran University, Tehran, Iran
*Corresponding author
Corresponding Author
Received 13 February 2017, Accepted 14 June 2017, Available Online 30 June 2018.
DOI to use a DOI?
Dependent Competing Risk; Copula Function; Reliability Function; Step-Stress Accelerated Degradation Test

The step-stress accelerated degradation test (SSADT) is one of the most commonly used time-dependent types of stress loading tests that enables a shorter test duration. This test is more economical and flexible compared to accelerated degradation test or accelerated failure time (ADT/AFT) test plans. This test is suitable when constraints by test facilities, conditions, or samples exist. SSADT is more useful for developing products when there is inadequate knowledge for test conditions. Important aspects here are to evaluate each failure mode in the presence of the other modes by assuming some dependency structure between the failure modes due to the non-applicability of studying test units with isolated competing failure modes. This paper aims to propose a modeling approach to simultaneously analyze linear degradation data and failure time data with dependent competing risks in an SSADT experiment. We use the copula function to consider the dependency structures between two failure modes. The proposed model is applied to acceleration data, to simulation data sets and two real data sets- bus tire data set and plastic substrate active matrix light-emitting diodes (AMOLED) data set, accompanied by sensitivity analysis.

Copyright © 2018, the Authors. Published by Atlantis Press.
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1. Introduction

The development of engineering and science technology have led to increased public awareness and insistence on product quality, in addition to consumer production laws and regulations that concern product reliability and profit consideration from the high costs of failures, repairs, and warranty programs. Hence, the products become increasingly more reliable, with an extended product life.

Under these circumstances it is difficult to assess product reliability according to traditional life-testing procedures based solely on time to failure under normal operation conditions. It is more difficult to obtain sufficient time to failure data to estimate their lifetime efficiency.

In order to overcome this difficulty, reliability practitioners have attempted to design methods that obtain failures quickly by exposing the products to acute environmental conditions without the introduction of additional failure modes other than those observed under normal conditions. The term accelerated life testing (ALT) describes these methods. ALT models can be categorized to accelerated failure time (AFT) model where stresses take effect on the failure time multiplicatively, the proportional odds (PO) model [3] that stresses take effect on an increased odds of failure rate, the proportional hazard (PH) model [6] in which stresses take effect on the failure rate multiplicatively, the extended hazard regression (EHR) model [5], the extended linear hazard regression (ELHR) model [7], in which both AFT and PH models are incorporated, and the proportional odds (PO) model [3] that stresses take effect on an increased odds of failure rate. Although ALT assesses the lifetime characteristics of the components with high reliability, this procedure may involve the collection of only a few failures.

To handle this problem, accelerated degradation testing (ADT) is considered as an alternative method. ADT combines degradation testing with ALT by means of testing the products in harsh environments and measuring the degradation of products during the acceleration test. In contrast to the ALT method in which the failure time is recorded, in the ADT method, both the failure information and degradation information may be obtained. As a result, the product reliabilities can be estimated more accurately. However, this method is generally very costly and usually requires a moderate sample size to be implemented. The ADT method also has its own difficulties in terms of not being applicable for evaluating the lifetime of a newly developed or a very expensive product with a few available units at hand. As a result, and to ensure enough failed units in a limited testing period, it is more realistic to consider multiple stress-type accelerated life testing methods. Most previous literature that discuss designing ALT/ADT plans have focused on the application of a single stress type, which usually requires a long test duration, complicated stress level selection process, large sample sizes, and high test costs. Literature about designing an ADT began at the end of the last century. Key references that pertain to ALT and ADT include [19], [23] and [26].

Under this situation, a constant stress ADT is not applicable. Tseng et al. [30] have proposed a step stress ADT (SSADT). In this accelerated life testing all samples are tested together under step stresses, which lead to a shorter test duration and the need for a smaller sample size. SSALT/SSADT is often preferred to constant stress ALT/ADT because it can avoid a high stress start point and possibly additional, unrelated failure modes. Concise reviews of SSALT have been presented by Nelson [19]. Liao [14] discussed how to efficiently design a SSADT experiment with an optimal sample size and termination time. Numerous papers have been published following the gradual development of degradation models. Park et al. [24] studied the optimum method of SSADT in the case of destructive measurement. More general time-varying-stress ALTs were considered by [12] and [2]. Turner [31], as well as Fan and Wang [10], discussed the statistical analysis of ALTs. Peng et al. [25] reported a model-based review of SSADT in terms of gradual development and improvement of degradation models which were categorized as degradation path models and Markovian models [17], and stochastic process based models [20].

Due to the existence of competing failure modes and non-applicability of studying test units with isolated competing failure modes, it is necessary to evaluate each failure mode in the presence of other modes by assuming some dependency structure between the failure modes. Recently, most researches of SSADT plans are based on an underlying assumption of one mode of failure. However, due to the complexity of high reliable products, their reliability should be evaluated by more than one mode of failure. Few works have focused on multiple degradation mechanisms or general multiple mechanism failure. Overviews of joint modeling of failure times and degradation data, as well as design problems have been discussed by [11], [15] and [21]. Liu and Qiu [16] proposed a method for planning multiple step-stress ALT with competing risks. Pan and Sun [22] presented an SSADT model with two performance characteristics based on gamma processes. Of note, in these SSADT models, a common but unrealistic assumption of researchers is the independency of the failure modes. However if the assumption of independence is violated, then the result may not be trustworthy and could result in an inaccurate estimation of the products lifetime. In this paper, we have extended the SSADT model proposed by Haghighi and Bae [11] in order to estimate reliability function in the presence of dependent competing risks.

Numerous researchers have applied the copula method to the dependence analysis of competing failures in the SSALT method (However this has not been studied in SSADT.). Simon and Wilke [27] presented an approach to the estimation of a nonparametric competing risk duration model based on an assumed dependence structure and illustrated the framework by analyzing the effect of reduced unemployment benefit entitlements on the duration of unemployment in Germany. Eryilmaz [8] studied the problem of estimating the parameter of the common distribution of component lifetime from a system lifetime data. It was assumed that the common component distribution was exponential, and that the component lifetimes were dependent through a completely known exchangeable Archimedean copula. Few studies reported the statistics for ALT with dependent competing failures. Although Xu and Tang [32] performed a pilot study on the statistics for ALT on the basis of the copula, this study was only a special case with an exponential distribution of all the competing failure modes; the copula was assumed to be a Gumbel copula, not a study with more general applications.

As previously mentioned, failure modes are usually dependent because of coupling factors such as running under the same working conditions. Therefore, the assumption that all the competing failure modes are independent is not true in practice. The statistics of SSADT based on this assumption may lead to incorrect results for product lifetime and reliability. However this has not been studied. In this paper, we propose a modeling approach for jointly analyzing linear degradation data and dependent failure times simultaneously recorded during the SSADT. Under the modeling approach, a step-stress accelerated test has been taken into account for unit failures with dependent multiple modes (competing risks). In each level of stress under the SSADT, we assume that failure times, their failure modes, and the amount of degradation at the moment of failures are recorded for failed units. For the units that have not failed at the end of each step-stress, only the amount of degradation is recorded. We apply the copula model to combine the marginal distribution of the competing failure models with the time to failure distribution of the products, and derived a general statistical model for SSADT with dependent competing failures. It is widely believed that the copula method is the most convenient and important tool for solving dependence problems. Finally, we have derived a likelihood function for failure-times from degradation data to provide maximum likelihood estimates (MLEs) of the parameters of the proposed model and the reliability function.

This paper is organized as follows. In Section two, we describe the copula functions, the competing risks framework in the SSADT method and express the likelihood and reliability funcrion. In Section three, we provide three examples from simulation and real data in an attempt to compare the efficiency of the SSADT plan proposed in this paper considering dependency between failure modes using the copula functions and that given by [11]. In Section four we have performed sensitivity analysis for the effect of chaning the copula function and the change-point of the stress on parameter estimation under a simple SSADT. Finally, conclusion and possible directions for future study are discussed in Section five.

2. The proposed model

This section is divided into three subsections. In the first subsection, we briefly explain the concept of copula function and in the second subsection, we discuss SSADT in the competing risks framework and give likelihood function in this method. In the third subsection, we describe a methodology for step-stress reliability function.

2.1. Copula Function

There is a need for more realistic modeling of a stochastic dependency structure that contain all information about dependent random variables, which goes beyond the measure of linear correlation coefficients and has the capability to capture co-dependency outside the world of elliptical distributions, particularly in situations where marginal functions are known and joint distributions may be unknown. Alternative methods for capturing co-dependency have been considered. One class of alternatives is the copula-based dependencies that have been introduced in statistical literature by [28]. This approach allows one to model the dependence structure independently of marginal distributions. This approach provides an alternative and frequently more useful representation of multivariate distribution compared to traditional approaches such as multivariate normality. Note that an independent copula implies zero correlation but the opposite is false. Joe [13] and Nelsen [18] have discussed this more thoroughly.

Formally, copulas can be defined as follows. Suppose that we have two marginal CDFs, GX1(x1), FX2(x2) where X1, X2 are the random variables. Sklar’s theorem states that every bivariate cumulative distribution function

of a random vector (X1,X2) can be expressed by involving only the marginals GX1(x1) and FX2(x2) as
where C is a copula. Differentiating with respect to x1,x2 leads to:
where c(u1,u2)=C(u1,u2)u1u2 is the density of the copula C.

The random variables X1 and X2 are said to be independent if:


According to Sklar’s canonical representation, if R be a 2-dimensional survival function with margins R1,R2, then R has a copula representation:

where Č is survival copula. Č is unique if the margins are continuous. The relation between copula and survival copula is:

There are some 1-parameter copulas that can be used. For example: the elliptical family (i.e. Gaussian, t) and Archimedean family (i.e. Frank, Gumbel, Clayton). One of the popular Archimedean copulas is the Frank copula. It is a symmetric copula (for bivariate data) given by


Its generator is:

where: θ ∈ (−∞,∞) \ {0}. In general, our motivations to use the Frank copula in joint modeling of linear degradation and multiple dependent competing risks data are summarized as follows:
  1. 1)

    It has a simple closed form with one parameter.

  2. 2)

    It includes positive and negative dependency.

  3. 3)

    It has symmetric dependence.

In this paper, we use the Frank copula to describe the dependence of the degradation and hard failure time. Č and C are equal in Frank copula. This dependency can be measured using copula parameter θ. There is an explicit relation between the Kendall’s tau and the parameter of Frank copula (θ). Specifically,


The relations between copula parameter, θ, correlation coefficient, ρ, and Kendalls tau, τθ, are given for some values of θ in Table 1.

θ = −1 τθ = −0.1100185 ρ = −0.1644861
θ = −200 τθ = −0.9801645 ρ = −0.9995137
Table 1.

Relation between copula parameter and correlation coefficients

2.2. The competing risks framework in the SSADT method

To express the framework of competing risks in SSADT, we must initially explain the concept of SSADT. Suppose that degradation models are linear and the rate of degradation depends only on current stress [30]. Although linear degradation has been considered by numerous authors, including [29], it appears that the simultaneous analysis of degradation and failure-time data with multiple failure modes is rare, especially when failure modes are dependent. This is attributed to the fact that inference on the parameters in the joint model is complicated under an SSADT. The inference procedure under the linear degradation model can be adapted to more general degradation models under an SSADT. In this section, we use a cumulative exposure model for SSADT data. This model is presented in [19].

Let n units be placed on the test. The testing time starts in τ0 = 0. All of the units are first subjected to a normal stress, S0. Afterwards, at changing time stress τ1, all surviving units are moved to the stress level S1 until time τ2. The stress on a unit is thus increased step by step until it fails. So, we have a sequence of changing time points of stress τi,i = 0,…,m + 1. The levels of stresses, S, can be expressed as:


As previously mentioned, we consider the linear degradation process: {Z(t);t > 0} as Z(t) = t/A,AR, where A is a random variable with a distribution function of FA(a; η) for the q-dimensional vector of parameters η, which is influenced by stress levels. As a result, a density function of A under the SSADT can be written as:

where η changes corresponding to the i-th level of stress for i = 0,…,m. The degradation process at time t under the SSADT can be written as:
where ai is the observed value of A in stress level Si,i = 0,…,m.

Let Tij be the failure time of i-th level of stress for the j-th unit, where i = 1,…,m and j = 1,…,ni and Zijs be degradation values at time Tij. Suppose we have s failure modes at each level of stress. Therefore failure time is defined as: Tij=min{Tij1,Tij2,,Tijs} where the failure-times caused by each failure modes are dependent. The failure mode at the i-th level of stress for the j-th unit is denoted by:


Under SSADT, we observe the data set {Tij,Vij,Zij}. Suppose that the rates of failures corresponding to different failure mechanisms are increasing functions of degradation values (e.g., [15]). Let λik(z(t)) be the failure rate of the k-th failure mode at the i-th level of stress at time t. Then, the conditional reliability function of the k-th failure mode at normal stress S0 given the value of degradation can be derived as:


Under a cumulative exposure model in a SSADT ( [30]) the failure time at time t under the i-th level of stress due to the k-th failure mode has an equivalent failure-time, denoted by t. This would be the time that produces the same amount of cumulative degradation under normal stress. Thus, the equivalent failure-time under normal stress t is a solution of the equation:


The equivalent failure-time t at normal stress S0 is derived from (2.4) and (2.5) as:


According to [11], the failure rate at time t and the conditional reliability function corresponding to the k-th failure mode are given by:


Let T = min(T1,..,Ts) be the failure time of unit under dependent competing risks. Our goal is to model the reliability function of T. Denote the reliability function by RT(.). We have:


When failure modes are dependent, we use the crude hazard function (λ(k)(t)) instead of marginal hazard function (λk(t)). The crude hazard function known as the ’cause-specific hazard rate’, is defined as:

is the crude density function and components of (t1,…,ts) are the observation of (T1,…,Ts). According to [9], the crude hazard function λ(k)(t) does not usually coincide with the marginal hazard λk(t), which is defined as:
where Rk(t) is the marginal reliability function. An exception is when the failure modes are mutually independent, but in most cases this assumption is unreasonable. Let competing risks be dependent. We use a copula modelling approach for specifying this dependency structure. According to (2.2), equation (2.7) in Frank copula become:
where Č is the survival copula. To solve the problem of identifiability, [4] used copula to characterize the relationship between the crude reliability functions and the marginals hazard functions. He showed that if the marginal Rk(tk) are continuous then C exists and is unique. In the following, we confine this study to the simplest situation of only two causes of failure (i.e., k = 2).

Analysis of reliability function requires that we choose a class of copulas. We use Franks family of copulas.

According to (2.9) and (2.10), the crude density functions can then be written as:

where θ ≠ 0 and

As mentioned earlier, λk(t) and λ(k)(t) do not coincide when failure modes are dependent. From (2.8) and (2.9), we can obtain the relation between them as following:


From the observed data at the end of each step of test and (2.8), (2.11) and (2.13), the likelihood function is obtained as the following form:

where γk is q-dimensional vector of parameters that correspond to the k-th competing risk, I(.) is an indicator function, aij is an observed value of A for the j-th unit at the i-th level of stress, aij ≡ (a0j,a1j,…,aij)T, and fAi(aij;η)=l=0ifA(alj;ηl), for i = 0,…,m.

The MLEs of γ¯(γ1,,γs)T and η¯(η0,,ηm)T, denoted by γ¯ˆ and η¯ˆ, cannot be obtained in closed form, thus a numerical method is required. To maximize the likelihood function, we use the function ’nlminb()’ in software R.

When we ignore the dependency between failure modes, the likelihood function changes to:

that is due to equation (2.1).

In order to prove the identifiability of likelihood function L, we show the identifiability of fi(k)(t). According to (2.3), τθ is a monotonic function in θ, [9]. Thus if θ1θ2 then Cθ1(u,v) ≠ Cθ2(u,v) for all (u,v) when Cθ(.,.) is Frank copula. According to equation (2.8), it follows that if θ1θ2 then fi(k)(t|θ1)fi(k)(t|θ2).

2.3. Step-Stress Reliability Function

The unconditional reliability (survival) function can be defined as:


Thus the estimate of reliability function is:


3. Examples

3.1. Simulation Study

In order to illustrate the proposed method, we generated n data sets under SSADT by considering a simple step-stress test with a changing time point of τ1 = 40. We suppose that the failure rates of two failure modes depends on the amount of degradation as λk(z(t)) = (θkz(t))νk for k = 1,2. In addition, we assume that the distribution of A in Z = t/A is Weibull with parameters α = 5 and β = 4.

For different sample sizes n = 30,50,80,200, given parameter values θ1 = 0.06, ν1 = 5, θ2 = 0.06 and ν2 = 5, we generated n random samples with B = 1000 replications based on the following steps. We consider the dependency between failure modes using Frank copula with parameter θ = 20.

  • Step 1:

    Generate random sample U of size n, where UUniform(0,1).

  • Step 2:

    Transform U, into the failure times T, based on the equation (2.12):

    where R1,R2 are the marginal reliability function of T1,T2.

  • Step 3:

    Generate random sample A of size n, where AWeibull(5,4).

  • Step 4:

    Transform A, into the degradation Z, based on Z = T/A.

Then, we transform data in normal use into the accelerated data with a changing time point of τ1 = 40. Let a0j,a1j denote the values of A for the j-th unit at the first (normal) and second level of stress. We observe a0j according to linear degradation path as t0j/z0j, where t0j, and z0j are failure time and degradation of j-th unit at normal stress, but a1j has been generated from a Weibull distribution with parameters α = 8, β = 5.5. From (2.6) and simulated a1j, the failure times in second level of stress can be computed.

The estimation of parameters of failure rates (θ1, ν1, θ2, ν2), the parameters of Ai, (α0, β0), and the copula parameter, θ, have been obtained using a numerical solution of the likelihood functions (2.14) and (2.15). Table 2 shows estimation results in two cases: independent and dependent failure modes. The estimated median of the lifetime (Mˆ), which is derived from (2.16) (R(tˆ0.5)=0.5), is shown in the Table 2. According to Table 2, it can be seen that the estimated parameters are different for the cases with and without dependency when the sample size is small. According to (2.3) and estimation of the copula parameter in Table 2, the dependency between failure modes is significant. The results provide insight into the sampling behavior of the estimators. They indicate that the MLEs approximate the true values of the parameters as the sample size n increases. Similarly, the standard errors (SE) and mean relative errors (MRE) decrease with increasing the sample size.

Dependent Independent

n Param. Estimate SE MRE Estimate SE MRE
n=30 α0 5.149 0.774 0.130 5.149 0.774 0.130
β0 3.964 0.161 0.031 3.964 0.161 0.031
θ1 0.059 0.009 0.105 0.038 0.026 0.403
ν1 5.411 1.199 0.193 4.006 2.502 0.426
θ2 0.060 0.006 0.080 0.035 0.025 0.424
ν2 5.626 1.262 0.216 3.663 2.319 0.405
θ 13.18 13.42 0.595 - - -
τθ 0.734 - 0 - -
M 38.76 - - 41.34 - -

n=50 α0 5.139 0.572 0.092 5.139 0.572 0.092
β0 3.996 0.114 0.023 3.996 0.114 0.023
θ1 0.059 0.005 0.067 0.037 0.024 0.399
ν1 5.228 0.893 0.136 3.628 2.193 0.389
θ2 0.059 0.005 0.068 0.039 0.023 0.345
ν2 5.208 0.873 0.136 3.953 2.151 0.348
θ 16.33 12.45 0.547 - - -
τθ 0.779 - 0 - -
M 38.35 - - 40.08 - -

n=80 α0 5.098 0.468 0.073 5.098 0.468 0.073
β0 3.995 0.096 0.019 3.995 0.096 0.019
θ1 0.059 0.004 0.057 0.037 0.024 0.390
ν1 5.151 0.673 0.104 3.594 2.082 0.362
θ2 0.059 0.004 0.055 0.040 0.023 0.338
ν2 5.186 0.683 0.108 3.937 2.072 0.322
θ 16.59 12.27 0.536 - - -
τθ 0.782 - - 0 - -
M 38.13 - - 39.74 - -

n=200 α0 5.048 0.278 0.044 5.048 0.278 0.044
β0 4.000 0.061 0.012 4.000 0.061 0.012
θ1 0.059 0.003 0.036 0.053 0.003 0.110
ν1 5.080 0.408 0.065 4.987 0.511 0.082
θ2 0.059 0.003 0.035 0.053 0.003 0.111
ν2 5.084 0.402 0.064 4.975 0.508 0.080
θ 18.50 10.35 0.499 - - -
τθ 0.803 - - 0 - -
M 37.85 - - 37.48 - -
Table 2.

The MLEs of the parameters, and the associated SE and MRE for different sample sizes (θ1 = 0.06 , ν1 = 5, θ2 = 0.06, ν2 = 5, θ = 20)

The estimate of reliability function (Rˆ(t)) in two dependent and independent cases was also derived. In the dependent case, Rˆ(t) has been derived from (2.16). Figure 1 shows the reliability functions estimated using the proposed method in both dependent and independent cases (solid and dashed lines) with different sample sizes. They indicate that increasing the sample size decreases the difference between two curves. Figure 2 shows also the estimated reliability function in dependent case for simulation data with one thousand replications. It shows that the estimated reliability functions close together as the sample size increases.

Fig. 1.

The estimated reliability function in a dependent (solid line) and an independent (dashed line) case under the simple SSADT for simulation data with different sample sizes

Fig. 2.

The estimated reliability function in dependent case under the simple SSADT for simulation data with one thousand replications

3.2. Real Data

In this section, we transform two sets of real data into SSADT data by considering a simple step-stress test with a changing time point.

3.2.1. Bus tire data

We use real data collected from 53 bus tires in a normal use environment as presented in a study by [1] who have reported tire wear with two different failure modes: protector zone and side zone. These two failure modes are dependent since the failure rate of both of them depends on degradation.

The method is similar to the previous section with respect to a changing time point of τ1 = 60. According to τ1, 33 out of 53 failure times were at the use stress (S0). As in the previous section, a0j,a1j are the values of A for the j-th unit at the first (normal) and second level of stress, where a1j has been generated from a Weibull distribution with shape parameter, α = 10.60, and scale parameter, β = 4.50. According to the data at normal stress, the estimation of shape and scale parameters are: α = 11.1190, β = 4.4826.Table 3 shows the failure times and corresponding degradation data at each level of stresses.

S0 V = 1 T 36.8 47.3 50.8 51.0 51.2 52.1 53.0 53.8 54.3 55.0 55.2
56.2 56.8 56.9 57.1 57.4 57.9 58.3 58.6 59.3 59.6
Z(t) 9.5 13.4 13.4 12.1 11.3 12.1 12.8 12.5 13.4 13.0 12.8
13.3 13.3 13.2 12.0 12.7 10.8 12.2 12.1 13.4 13.4

V = 2 T 50.0 51.0 51.7 51.7 55.0 55.0 56.0 56.6 58.1 58.9 59.0
Z(t) 13.3 13.1 12.5 13.2 13.1 13.2 12.5 13.2 13.2 11.7 14.0

S1 V = 1 T 60.083 61.236 62.879 63.658 65.331 65.346 67.425 68.222 70.700 75.961
Z(t) 12.7 13.6 14.5 13.5 14.1 12.8 13.2 12.9 14.2 15.0

V = 2 T 61.311 65.338 65.473 65.609 65.759 69.664 70.457 73.064 73.182 74.588
Z(t) 13.6 13.2 13.8 13.7 13.3 13.6 13.6 15.0 15.0 15.0
Table 3.

Time failures and corresponding degradation data at the first and second level of stress for the bus tire data

All model parameters,(α0, β0, θ1, ν1, θ2, ν2, θ), have been estimated using a numerical solution of the likelihood functions (2.14) and (2.15) and reported in Table 4. The last column of Table 4 is the estimated median of the lifetime (Mˆ). According to (2.3), τθ = 0.81. The estimate of reliability functions was also derived. Figure 3 shows the reliability functions estimated using a Nelson-Aalen nonparametric method (dashed line) and the proposed method in both dependent and independent cases (dotted and solid lines). As we know, the nonparametric estimator of the survival function is weaker than the parametric estimators (dependent and independent case) due to the lack of distribution, and therefore it estimates the survival function more cautious, thus it is above the other curves. The nonparametric curve is closer to independent estimates, because as seen in Figure 1, estimating the reliability function in a dependent case is always lower than its estimation in the independent case. The difference between the two curves (solid and dotted lines) is obvious in Figure 3. As we see, ignoring dependency between failure modes led to overestimation of the reliability function.

Fig. 3.

Nonparametric (dashed line) and parametric estimated reliability function in a dependent (solid line) and an independent (dotted line) case under the simple SSADT for bus tire data

α0 β0 θ1 ν1 θ2 ν2 θ M
Dependent case 11.119 4.4826 0.0655 12.168 0.0663 13.046 20.22 55.88
Independent case 11.119 4.4826 0.0616 11.611 0.0647 17.269 56.79
Table 4.

The estimation of parameters with and without dependency for the bus tire data

3.2.2. AMOLED data

In the second example, the real data was collected from plastic substrate active matrix organic light emitting diode (AMOLED). AMOLED is an attractive light device compared to other display devices. In order to achieve SSADT data, the luminance degradation is accelerated using temperature. In this set of data, two failure modes (the organic layer peel-off from the substrate and delamination) expedited by temperature could be observed. We have assumed that the two failure modes are dependent. In the AMOLED data we have 20 failure times with corresponding degradation and different failure modes. The data are reported in [11] and shown in Table 5. The simulated failure times in the second level stress are obtained with a changing time point of τ1 = 1800 [13 failure times are in normal stress level (below 1800)] and the failure rate of each failure time depended on degradation data similar to the previous example.

S0 V = 1 T 1294.4 1462.4 1593.6 1713.4
Z(t) 90.42 97.37 88.49 95.18

V = 2 T 1565.8 1414.9 1592.7 1141.4 1514.4 1505.0 1509.6 1517.3 1267.1
Z(t) 97.30 93.08 90.82 97.80 97.42 96.02 93.28 90.24 98.43

S1 V = 1 T 2074.708 2400.158 1884.541 1883.251 1978.770 1872.205
Z(t) 90.20 87.37 84.46 85.27 76.87 91.69

V = 2 T 1824.737
Z(t) 97.067
Table 5.

Failures and corresponding degradation data at the first and second level of stress for the AMOLED data

A Weibull distribution with shape and scale parameters α = 10.749, β = 16.381 was fit to a0j, j = 1,…,13. The a1j were also generated according to a Weibull distribution with shape parameter 2.79 and scale parameter 10. The estimate of all parameters (α0, β0, θ1, ν1, θ2, ν2, θ) and the median of the lifetime Mˆ are listed in Table 6. As we see, these estimations are different with and without considering dependency. We can calculate the dependency of failure modes using (2.3) (τθ = 0.86). The estimate of reliability functions is shown in Figure 4. Ignoring dependency between failures modes has led to an overestimation of the reliability function.

Fig. 4.

Nonparametric (dashed line) and parametric estimated reliability function in a dependent (solid line) and an independent (dotted line) case under the simple SSADT for AMOLED data

α0 β0 θ1 ν1 θ2 ν2 θ M
Dependent case 10.749 16.38 0.0067 11.92 0.008 20.96 27.62 1765.95
Independent case 10.749 16.38 0.0074 14.59 0.0096 48.70 1844.03
Table 6.

The estimation of parameters with and without dependency

4. Sensitivity analysis

In this section, we performed two sensitivity analyses. The first analysis explored the effects of changing the copula function on parameter estimation. In the second sensitivity analysis, we sought to explore the impact of the change in change-point of the stress on the parameter estimation under a simple SSADT.

4.1. The effect of changing the copula function on parameter estimation

In order to investigate the effect of changing the copula function on parameter estimation, we applied both simulated and real data. Initially, we conducted a simulation study. The data were generated according to the different copulas (Frank, Clayton, and Gumble) following Section 3, Steps 1-4, where: α0 = 5, β0 = 4, θ1 = 0.06, ν1 = 5, θ2 = 0.06, ν2 = 5, θ = 20 and n = 30. Table 7 shows the estimated parameters. We determined that the Frank copula was more appropriate based on the actual value of the parameters, in addition to SE and MRE of the estimators.

(α0 = 5 , β0 = 4, θ1 = 0.06, ν1 = 5, θ2 = 0.06, ν2 = 5, θ = 20)

Copula Parameter Estimate SE MRE
Frank α0 5.1135 0.5686 0.0962
β0 3.9790 0.1520 0.0299
θ1 0.0602 0.0073 0.0923
ν1 5.3335 1.1876 0.1744
θ2 0.0605 0.0068 0.0870
ν2 5.2527 0.9841 0.1628
θ 17.2259 14.0303 0.6130

Clayton α0 5.0971 0.8331 0.1171
β0 3.9793 0.1567 0.0318
θ1 0.0560 0.0084 0.1049
ν1 4.7304 1.1916 0.1917
θ2 0.0555 0.0081 0.1058
ν2 4.6548 1.1062 0.1852
θ 30.4304 44.2251 2.1881

Gumble α0 5.2004 0.7574 0.1205
β0 3.9692 0.1555 0.0321
θ1 0.0649 0.0085 0.1290
ν1 6.1629 1.6670 0.2954
θ2 0.0655 0.0103 0.1448
ν2 6.2595 1.7361 0.3278
θ 50.313 60.86 5.4178
Table 7.

The MLEs of the parameters, and the associated SE and MRE for n = 30 in different copula

Additionally, we used real data based on the original bus tire data set to further investigate the effect of changing the copula function on parameter estimation, [1]. The assumption of dependency between failure modes was valid because we supposed that the failure rates of two failure modes depended on the amount of degradation. We fixed the value of τ1 at 62. Then, we generated accelerated failure times to determine the MLE of the parameters by using numerical methods with 2000 replications. Table 8 lists the results. The simulated and real data examples provided evidence that the parameters of ν1, ν2 and θ, were mostly affected by changing the copula function.

Copula function α0 β0 θ1 ν1 θ2 ν2 θ M
Frank 11.5890 4.5013 0.0637 11.6177 0.0657 13.5076 30.1010 56.886
Clayton 11.5890 4.5013 0.0647 13.0798 0.0644 13.3472 89.1893 57.1095
Gumble 11.5891 4.5013 0.0678 16.6345 0.0656 13.7697 25.1193 57.4576
Table 8.

The estimation of parameters using different copula function

4.2. The effect of the change-point of the stress on parameter estimation

In this section, we investigate the effect of the change-point of the stress on parameter estimation based on the original data set of bus tire data, [1]. Like the previous section, we generate accelerated failure times and estimate the parameters of likelihood function using numerical methods with 2000 replications. These steps are repeated for different values of τ1. The results are shown in Table 9. It is observed that, the change-point of stress has little effect on the estimates of (θ1, ν1, θ2, ν2, θ) , but the effect on the estimates of (α0, β0,M) is significant.

τθ 58 60 62 64 66 68 70
n01 17 21 23 24 26 27 28
n02 8 12 13 13 14 15 18
n11 14 10 8 7 5 4 3
n12 14 10 9 9 8 7 4
αˆ0 10.3883 11.1190 11.5890 11.6889 11.9279 11.5398 11.1419
βˆ0 4.3935 4.4826 4.5013 4.4992 4.5237 4.5826 4.6611
θˆ1 0.06365 0.06361 0.06368 0.06371 0.06375 0.06357 0.06352
νˆ1 11.5847 11.5581 11.6177 11.6647 11.7882 11.6169 11.5299
θˆ2 0.06564 0.0656 0.06570 0.06572 0.06541 0.06581 0.06571
νˆ2 13.4500 13.4081 13.5076 13.5613 13.3389 13.7345 13.5154
θˆ 30.6017 30.4961 30.1010 30.1349 31.42179 30.3591 32.8662
Mˆ 55.369 56.555 56.886 56.9045 57.3392 57.9129 58.6766
Table 9.

The effect of changing point on the estimation precision with 2000 replications

5. Conclusion and further work

SSADT is one of the most commonly used methods for reducing the required sample size. When we have multiple failure modes in SSADT, it is important to take into account the dependency between them. This article has proposed a modeling approach for simultaneously analyzing dependent failure modes and degradation data under the SSADT. According to this method, we can estimate the reliability function in a dependent case and compare the differences between the dependent and independent cases. This difference is significant in dependent failure modes. Sensitivity analysis also shows that changing the copula function and change-point of the stress affects on a small number of parameters.

In this article, we have assumed that the degradation is linear; failure rates depend on degradation and do not make any assumption about the failure-time distribution. For further analysis, we can change these assumptions. For example, we can consider nonlinear degradation or other forms of failure rates, such as: λk(z(t)) = γk + (θkz(t))νk.


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Cite this article

AU  - Somayeh Mireh
AU  - Ahmad Khodadadi
AU  - Firoozeh Haghighi
PY  - 2018
DA  - 2018/06/30
TI  - Joint Modeling of Linear Degradation and Multiple Dependent Competing Risks Data under a Step-Stress Accelerated Degradation Test
JO  - Journal of Statistical Theory and Applications
SP  - 340
EP  - 358
VL  - 17
IS  - 2
SN  - 2214-1766
UR  -
DO  -
ID  - Mireh2018
ER  -