Time-Variant Reliability Analysis of RC Bridge Girders Subjected To Corrosion - Shear Limit State
Time-Variant Reliability Analysis of RC Bridge Girders Subjected To Corrosion - Shear Limit State
Time-Variant Reliability Analysis of RC Bridge Girders Subjected To Corrosion - Shear Limit State
162 © 2016 Ernst & Sohn Verlag für Architektur und technische Wissenschaften GmbH & Co. KG, Berlin · Structural Concrete 17 (2016), No. 2
A. P. Vatteri/K. B.Rao/A. M. Bharathan · Time-variant reliability analysis of RC bridge girders subjected to corrosion – shear limit state
paper. This paper proposes a stochastic modelling ap- empirical coefficient that relates the reduction in yield
proach for estimating the time-variant shear capacity and strength to corrosion area loss. It was found that the prob-
reliability within the framework of a Monte Carlo simula- ability of failure assuming brittle reinforcement behaviour
tion (MCS). is up to 450 % higher than that obtained assuming ductile
The paper is organized as follows: Section 2 gives a behaviour. As pointed out by Bertolini [32] and others,
brief review of the literature related to the shear capac- micro-environmental effects on the process of corrosion
ity reduction of beams due to corrosion of rebars and at different locations on the same girder could be signifi-
a summary of the corrosion initiation and propagation cant considering the large sizes of girders. Hence, there is
models adopted. Stochastic analysis of reduction of shear a need to consider these effects when estimating the time-
capacity, computation of the capacity of ductile and brittle variant reliabilities of RC beams.
elements and time-variant reliability analysis are elabo- Most of the investigations presented in the above dis-
rated in section 3. An example problem is defined and cussion focused on the structural behaviour of the beams/
the proposed methodology is applied in section 4. Section girders with corroding reinforcement, assuming that cor-
5 discusses the results and conclusions are presented in rosion of reinforcement had already been initiated. Two
section 6. possible practical cases addressed by this assumption are:
a) existing structures that have already started corroding,
2 Literature review and b) structures in which chlorides are introduced dur-
ing mixing itself (due to use of beach sand or seawater for
Many researchers have carried out experimental and ana- mixing). However, for the design of important structures
lytical studies on the shear capacity reduction and flexural such as RC bridges and tall RC buildings, the codes rec-
capacity reduction of RC beams subjected to chloride-in- ommend that care should be taken to ensure an adequate
duced corrosion [6, 7, 9, 17, 18]. Chlorides are introduced service life by avoiding beach sand and using potable
into concrete either by mixing chlorides into the concrete water. For example, bridge codes such as IRS code 1997
mix or by diffusion from the external environment. The [22] restrict the amount of chlorides in the concrete mix to
majority of the experimental work concentrated on the avoid excess chloride concentrations. Thus, in the service
structural behaviour of RC members after the initiation life design of such structures, it is more appropriate to as-
of corrosion, and thus involved the first method, where sume that no added chlorides are present in the concrete
chlorides are already present in the concrete mix. In the mix at the time of concreting. When there are no added
case of environment-assisted corrosion, the diffusion of chlorides in the concrete, the presence of chlorides in the
chlorides into the concrete cover leads to corrosion initia- concrete is attributed to the transportation of chlorides
tion. This is a finite time and in most cases when designing from the surface of a concrete member to the inside by dif-
new structures, the initiation time is considered as the life fusion. It is known that consideration of the corrosion ini-
of the structure. Some of the investigations available in tiation time is important in the service life design of a RC
the literature with respect to shear capacity reduction due structure. In a probabilistic/stochastic service life design
to corrosion of stirrups are presented below. paradigm, the uncertainty associated with the initiation
Many experimental investigations reported in the time has to be estimated and needs to be propagated into
literature (viz. [17]) have reported that shear failure mode a propagation period to estimate realistically the uncer-
dominates in the case of RC beams where stirrups are sub- tainty associated with the service life of an RC member.
jected to corrosion. Corrosion was induced in RC beams Based on the review of the literature, the following
by mixing calcium chloride into the mixing water and by aspects are investigated in this paper:
applying an accelerated corrosion procedure. Coronelli 1) Developing a framework for reliability-based sustain-
and Gambarova [19] and Bhargava et al. [20] attempted to able design against shear failure for RC bridge girders
model the corrosion phenomenon taking into considera- subjected to corrosion of reinforcement in line with
tion the experimental findings of Rodriguez et al. [17]. In Stewart’s [6] formulation, additionally incorporating
developing a time-dependent reliability model, Bhargava randomness in corrosion initiation time and the micro-
et al. [20] considered generalized corrosion, with a reduc- environment effect.
tion in steel area as well as concrete area due to spalling 2) Illustrating the need for considering the transition from
as corrosion progressed. In order to develop modelling ductile to brittle behaviour of stirrups with the progress
guidelines for the structural assessment of corroded RC of corrosion when estimating the residual shear capaci-
beams, Coronelli and Gambarova [19] considered pitting- ties of a girder at different times.
type corrosion by considering a factor defined by the ratio 3) Quantifying the improvement in performance of RC
of area of pit to nominal bar area in the model. These girders when using PFA concrete instead of OPC con-
studies focus on the structural behaviour of the beams/ crete, with respect to reliability against shear failure.
girders with corroding reinforcement without giving con-
sideration to corrosion initiation time. The importance of One of the aspects of sustainable design is the choice of
modelling the spatial variation in degradation phenomena more durable materials for construction. The framework
in the service life assessment of RC structures was studied developed in this paper works well in this aspect, as it
by Ying and Vrouwenvelder [21]. Stewart [6] developed a gives the designer an option to compare the durability
spatial time-dependent reliability model for pitting-type performance of the RC girder, by using different material
corrosion which takes into account the transition of the compositions, at the design stage itself, thus enabling a
mechanical behaviour of reinforcement in RC beams. The sustainable design.
effects of pitting are considered by a pitting factor and an
A brief overview of the corrosion initiation and Vu(t) = Vc(t) + Vs(t) (4)
propagation processes is carried out in the next section.
That is followed by the estimation of the shear capacity of The shear capacity of the concrete (without shear stirrups)
girders according to code provisions. depends on the grade of concrete and longitudinal steel
area, and is given by
2.1 Corrosion initiation and propagation
Vc(t) = τ c(t) ⋅ bw ⋅ d (5)
The ingress of chlorides into concrete is assumed to be
due to the diffusion of chlorides from the environment where:
through the concrete cover. Most of the models for initia- τc(t) permissible shear stress in concrete in girder with-
tion of chloride-induced corrosion are based on Fick’s sec- out shear reinforcement
ond law of diffusion (e.g. [9], [23]). Corrosion in stirrups bw width of web
is assumed to initiate when chloride concentration at the d effective depth of girder
location of stirrups reaches a critical value ccr. The time of
initiation is evaluated as follows: The value of τc(t) is obtained from the Eurocode 2 [26]
formula. The Eurocode is used instead of the IS code
−2 because the latter does not include any explicit formula
c 2 −1 c0 − ccr
Ti = erf (1) showing the relation between concrete grade and longitu-
4D c0 dinal steel area. As the area of longitudinal steel reduces
with time due to corrosion, τc(t) is estimated with the
where: available area of longitudinal steel at any time t by using
Ti corrosion initiation time in years the Eurocode2 formula for τc [25, 26]:
c̃ concrete cover to stirrups in cm
D chloride diffusion coefficient of concrete in cm2/year 0.18 1
τ c(t) = ⋅ K ⋅ (100 pt(t)fcl ) 3 + 0.15 ⋅ σ cp
c0 chloride concentration at concrete surface as percent- γc (6)
age weight of concrete 3 1
ccr critical chloride concentration to initiate corrosion ≥ (0.035 ⋅ K2 ⋅ fcl 2
as percentage weight of concrete
where:
The first phase of corrosion, i.e. the corrosion initiation, is
200
mainly affected by the aforementioned factors, which are K = 1 + ≤2
random variables. Hence, the time to initiation of corro- d
sion is also a random variable.
After initiation, corrosion propagates in the stirrups,
Ast(t)
causing a reduction in the cross-sectional area of the stir- pt(t) longitudinal steel ratio =
bw d
rups. This corresponds to the second phase. The reduced
diameter after corrosion is given by σcp axial stress in the case of prestressed girders
fcl characteristic cylinder compressive strength of con-
∅(t) = ∅(0) − rcorr(t − Ti ) (2) crete
where: The girder is analysed for its ultimate capacity and so the
∅(t) remaining diameter at time t partial safety factor for concrete γc is set to 1.
∅(0) initial diameter of stirrup The resistance offered by shear reinforcement Vs at
Ti corrosion initiation time any time t should be calculated as follows [24]:
rcorr rate of corrosion penetration, given by
σ sv(t)Asv(t)d (7)
Vs(t) =
rcorr = 0.0115 Icorrα (3) s
4. The mechanical behaviour of stirrups is assumed to where Vs(i)(t) = Rns(i)(t), as obtained by either Eq. (10) or
change from ductile to brittle when the loss of stirrup (11) and Vc(i)(t) is the shear capacity of concrete without
area exceeds 20 % of the initial nominal area [6]. Ad- stirrups at time t, as obtained with Eqs. (5) and (6), which
ditionally, an element is considered to be brittle when reduces with the reduction in longitudinal steel area with
> 20 % of its stirrups has become brittle. time; V is the time-invariant shear demand. The uncertain-
ties associated with the resistance model are taken care of
Details of the computation of shear capacity reduction, by modelling errors associated with the computation of
considering the elements as either ductile or brittle and reduced diameter f(t), reduced yield strength fy(i)j(t) and
the time-variant reliability estimation are discussed in the permissible shear stress in concrete without shear rein-
following sections. forcement τc(t) (Table 3).
3.1 Capacities of perfectly ductile and perfectly brittle 3.2 Estimation of probability of failure
elements
The probability of failure is the probability that Vus(t) ≤ 0 at
The shear capacity of one element when it is ductile (ac- time t. The probability is evaluated by the relative frequency
cording to the criteria mentioned before) is obtained by approach, i.e. probability of failure at time t is
adding the individual shear capacities of each stirrup at
every instant of time. Let i denote the element number pf(t) = (number of realizations in which Vus(t)
and j the stirrup number. The individual shear capacity ≤ 0)/1000) (14)
r(i)j(t) of the jth stirrup in the ith element at time t is given
by The methodology for estimating the time-variant probabil-
ity of failure against shear capacity of a girder subjected
r(i) j(t) = Asv
(i) (t) ⋅ f (i) (t)
j y j (8) to reinforcement corrosion is summarized in a flowchart
(Fig.2). Some of the codes of practice (viz. IS 456) specify
(i)
where A sv j(t) is the available reduced area of the same deemed-to-satisfy clauses for the durability-based service
stirrup, given by life design of RC structures. However, fib Model Code
2010 gives an explicit procedure for such design. This
(t − T )
2
(i) (t) = 2 ⋅ π (i) (i)
Asv ∅ (0) − rcorr(i) (9) methodology, incorporating aspects related to sustaina-
j
4 j i
bility-based design, is presented in Fig. 3. Accordingly, the
structure should be redesigned if the failure probability
(i)
and f y j(t) is the yield strength of the same stirrup at time obtained is greater than an allowable failure probability at
t, given by the given time (say, expected service life).
Fig. 2. Flowchart for estimating the time-variant probability of failure against shear capacity due to corrosion
local environment (viz. local temperature, relative humid- 5 Results and discussion
ity) will change the vulnerability of the beam with regard 5.1 Corrosion initiation time for stirrups
to corrosion propagation. This micro-environment effect
can be significant for tropical countries and for bridges It is assumed that the quality of workmanship would be
located in coastal areas. For example, the portion of the nominally the same and there should not be any compel-
intermediate girder located on an abutment is more prone ling need to consider it as a sequence of random variables
to corrosion than the portion remote from it. Thus, the within an element. The consequence of this assumption
corrosion propagation life changes. For this reason, rcorr is is – for a given element – that Ti is only one random vari-
expected to be higher for the elements closer to the con- able. However, from element to element, Ti variables are
Table 1. Random variables associated with girder properties [9], [25]
considered to be i.i.d. variables. Thus, Ti is the same for tribution is found to be the best fit with the distribution
all stirrups in one element. A comparative study is car- above as verified by a K-S test.
ried out with a 30 % PFA concrete girder having the same
cross-sectional and strength properties, using the random 5.1.2 30 % PFA concrete
variables listed in Table 2.
The mean corrosion initiation time for stirrups is about 38
5.1.1 OPC concrete years for a T-girder made from30 % PFA concrete, which
is more than six times that of the OPC concrete girder;
The mean value of Ti for stirrups in the OPC concrete standard deviation varies from 13.8 to 14.7 years from
girder is about 6 years; standard deviation varies from element to element for the five elements in the shear span
6.99 to 7.36 years for the five elements of the shear span. considered, as shown in Fig. 7. The average value of COV
The average value of COV in the five elements is 1.156. for Ti in the five elements is 0.3639. The distribution is
The range space of Ti is from zero to 80 years consider- skewed to the right. The range space of the distribution is
ing all the elements. From the histograms of Ti of five from 10 to 120 years in most of the elements and can be
elements in Fig. 6, the distribution is found to be heavily considered general. In the case of 30 % PFA concrete, Ti is
skewed towards the right. A two-parameter Weibull dis- found to follow a lognormal distribution.
Fig. 6. Corrosion initiation time of stirrups in different elements for OPC concrete girder
Fig. 7. Corrosion initiation time of stirrups in different elements for 30 % PFA concrete girder
Initially, all the stirrups in the shear span are uncorroded, As discussed earlier, out of the series system of elements,
and the mechanical behaviour of the stirrup steel is duc- the shear capacity of the weakest element governs the
tile. As the stirrups start to corrode, the shear capacity shear capacity of the girder (Eq.(12)). Shear capacity
reduces from the original capacity, but the stirrups could distribution at different ages is studied to establish the
still exhibit ductile behaviour if the area loss is less than decrease in capacity over time as shown in Fig. 8. Mean
the critical limit of 20 % at which the mechanical behav- values of capacity at ages of 5, 10, 20, 30, 40 and 50 years
iour of the stirrup is assumed to become brittle. Only are 1130, 1020, 780, 619, 523 and 459 kN respectively.
when > 20 % of the stirrups within an element become The drastic fall in shear capacity of the girder beyond 20
brittle is the element itself considered to be brittle, as years (1020 to 780 kN) can be attributed to the transition
explained in section 3. After initiation of corrosion, the in the mechanical behaviour, as it can be shown from the
time-variant shear capacities of the girder are estimated deterministic calculation of the time required for a 20%
using the variables listed in Tables 1 and 3. The resulting reduction in stirrup area at which this transition occurs
distributions at various ages are presented in Figs. 8 and 9 is 21 years. If the transition in the mechanical behaviour
for OPC and 30 % PFA concrete respectively. from ductile to brittle is not taken into account, and the
Fig. 8. Distribution of shear capacity at different ages for OPC concrete girder
stirrups are assumed to be ductile irrespective of the ex- The influence could be more predominant in structures
tent of corrosion, the mean values at the aforementioned with a longer service life than the 50-year life considered.
ages are approx. 1130, 1030, 823, 658, 544 and 467 kN Mean values of capacity at ages of 5, 10, 20, 30, 40 and
respectively. It can be seen that avoiding the brittle behav- 50 years are 1130, 1130, 1130, 1080, 944 and 789 kN
iour with the propagation of corrosion in stirrups can lead respectively (Fig. 9). The elements start becoming brittle
to overestimating the shear capacity, which is not desir- at an average age of 50 years, hence the sudden drop in
able due to the nature of the failure of the system. shear capacity between 40 and 50 years. If the transition
in the mechanical behaviour is not considered, mean
5.2.2 30 % PFA concrete values of capacities at the given ages are approximately
1130, 1130, 1130, 1085, 962 and 817kN respectively,
Similar observations to those for the OPC concrete which are overestimates, as mentioned in the case of the
girder are made in the case of 30 % PFA concrete. Since OPC concrete girder.
the corrosion initiation time is about six times higher for
the 30 % PFA concrete girder compared with the OPC 5.3 Time-variant probabilities of failure
concrete girder, the shear capacity reduction is com-
paratively lower for the 30 %PFA girder. Hence, the time The observations made above regarding reduction in
taken for the stirrups to become brittle will also be large. shear capacities over time are reflected in the correspond-
Fig. 9. Distribution of shear capacity at different ages for 30 % PFA concrete girder
ing probabilities of failure for OPC and 30 % PFA con- 30 % PFA concrete was carried out within the scope of
crete girders. The latter gives a more durable performance a Monte Carlo simulation (Fig. 2). The 30 % PFA con-
compared with the former, as is to be expected from its crete was found to give a more durable performance
low chloride diffusion coefficient and high corrosion over OPC concrete, and can be used as a sustainable
initiation time. Fig. 10 compares the time-variant prob- alternative to OPC. The reliability analysis took into
abilities of failure of the girder when the transition in the account the spatial variability of the corrosion process
mechanical behaviour is avoided and when it is taken into along the length of the girder, the micro-environment
account. Clearly, the first case, which is often followed, near the supports and the transition in the mechanical
gives lower probabilities of failure, which can lead to non- behaviour of stirrups from ductile to brittle, as explained
conservative design decisions. The difference in probabili- in section 3.
ties of failure of both approaches is more pronounced in More detailed studies have to be carried out to iden-
the case of 30 % PFA concrete. tify perfectly the transition in the mechanical behaviour
from ductile to brittle, as it is conservatively assumed to
6 Conclusions occur at an area loss of 20 % in the present study. Further,
the spatial variation in corrosion along the length of a
A stochastic analysis of the reduction in shear capac- stirrup and randomness in the loads, not addressed in this
ity of RC bridge girders made from OPC concrete and study, are identified as scope for future work.
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