Thermal and structural analysis of RCC double-curvature arch dam.
Abdulrazeg, Aeid Ali ; Noorzaei, Jamaloddin ; Jaafar, Mohamed Saleh 等
Introduction
The RCC technology has being applied in gravity arch dams in the
late of 1980s. The first RCC arch dam was constructed in the world is
Kenllpoort dam, which was completed in S. Africa in 1988 (Qiuhua 2003).
Up to the end of 2003, the number of RCC arch dams completed or under
construction is 14. The construction technology of a RCC arch dam is
very similar to that of a RCC gravity dam. The main differences between
arch RCC dam and gravity RCC dam are that arch dam has a wider surface
and lesser thickness, accordingly different thermal and stress response.
Xie et al. (2005) and Zhang et al. (2009) used a three-dimensional
finite element relocating mesh method to simulate construction process
and compute temperature field. In their work, many factors have also
been considered, such as thermal adiabatic rise of temperature with age,
the process of placement by layer, creep, work suspension in summer and
the change of air temperature. However, the studies were limited for
thermal analysis only. In addition, further studies to select the proper
relocating age of concrete are essential. Penghui et al. (2007)
determined creep values for thermal analysis of Dahuashui RCC arch dam,
applied time and stress dependent coefficient, in a multi-term
expression, whereby certain constants were apparently derived through
experimental study to an accuracy of six decimal places. In the
presented work, the variation of the RCC mechanical properties with time
has not been considered and fixed values were used during the analysis.
Shuping et al. (1999) performed an emulation analysis of two RCC
arch dams using three dimensional finite elements. It has been found
that, the thermal stresses were too high for the construction plan
without contraction joints. However, the authors ignored the effect of
dam foundation interaction. In 2003, a similar study was conducted by
Nilipour (2003). It was concluded that, at the same elevation higher
temperature rise was experienced in the core of the dam in applying
conventional method as compared with RCC method. However, higher tensile
stress occurs in the model using conventional method in the early age of
concrete. Whereas, maximum tensile stress in RCC model occurs later due
to operation loads comparatively with a lower value, hence post-cooling
is not necessary in RCC construction method. However, in these
investigations a simplified relation for stress-strain relationship has
been used which will overestimate the stress of the dam (Crichton et al.
1999).
It is of particular significance to observe that, most of the
studies that address the stress analysis of RCC dams have considered the
time dependent deformation such as creep very approximately or neglected
it all together (Araujo, Awruch 1998; Agullo, Aguado 1995; Saetta et al.
1995; Malkawi et al. 2003; Noorzaei et al. 2006; Zhiqi 2007). However,
creep has a significant influence on the stress values of the concrete
blocks, especially in early ages (Santurjian, Kolarow 1995). Moreover,
there was a concern that RCC acts in the same manner as conventional
concrete and various models developed for the conventional concrete are
applied for RCC without any form of verification. Furthermore, the
material laws for concrete, mainly based on the age of concrete and very
limited study, considered the temperature effect on the mechanical
properties of the concrete (Luna, Wu 2000; Cervera et al. 2000).
Consistent cracking criterion is also necessary for an exact
evaluation of the dam behavior. Most of the previous researchers who
investigated dam concrete mainly focused on the uniaxial compressive
strength and tensile strength, so their studies did not provide
information on the behavior of dam concrete under bi-axial or tri-axial
stress states (Wang, Song 2008).
1. Motivation of the present work
The present investigation is a continuation of the authors'
previous work (Bayagoob et al. 2010) and presenting a numerical
implementation using three-dimensional finite element method to simulate
the construction process of RCC arch dams. The primary objectives of the
present research work:
--This paper presents a new comprehensive numerical procedure to
simulate the construction process of arch RCC dams. It takes into
account the more relevant features of the behavior of concrete such as
hydration, ageing, thermal and creep effect;
--To apply the proposed model to an actual arch RCC dam to
demonstrate the efficiency of the model.
2. Computation of thermal field
The Numerical solution scheme used in this study is based on the
Taylor-Galerkin approach. Upon applying this approach, the following
system of differential equations is obtained (Bayagoob et al. 2010):
[[[K.sub.t]].sup.(e)][{T}.sup.(e)] - [[C].sup.e] [{[partial
derivative]T/[partial derivative]t}.sup.(e)] = [{F}.sup.(e)], (1)
where: [[C].sup.e] is the capacitance matrix; [[K.sub.t]] is the
heat stiffness matrix; {F} is the total load heat vector due to
hydration and convection actions.
The finite difference approximation was used to solve Eqn (1) in
the time domain numerically. This solution (after assembly of the
stiffness matrices) is given by (Sergerlind 1984):
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII], (2)
where: [{T}.sub.b] and [{[F.sub.t]}.sub.b] are {T} and {[F.sub.t]}
at time (b) and [{T}.sub.a] and [{Ft}.sub.a] are {T} and {[F.sub.t]} at
time (a); [theta] is a scalar (0 [less than or equal to] [theta] [less
than or equal to] 1) which is equal to 2/3 in the Galerkin method. Then
Eqn (2) takes the following general form:
[[A.sub.G]]{[DELTA]T} = [[F.sub.G]], (3)
where:
[[A.sub.G]] = 1/[DELTA]t [C] + 2/3[[K.sub.t]] (a-4)
and
{[F.sub.G]} = 1/2([{[F.sub.t]}.sub.a] + 2[{[F.sub.t]}.sub.b] -
3[[K.sub.t]][{T}.sub.a]), (b-4)
where: {[DELTA]T} represents the temperature changes at the nodal
points with respect to time At which is used for evaluation of
temperatures at the new time stage using the following expression:
[{T}.sub.b] = [{T}.sub.a] + 2/3 {[DELTA]T}. (c-4)
3. Constitutive theories for aging viscoelastic materials
Time dependent behavior of concrete is described by the theory of
viscoelasticity for aging materials. The sum of elastic
{[[epsilon].sub.e]} and creep {[[epsilon].sub.c]} strain is replaced by
the viscoelastic strain {[[epsilon].sub.ve]} as follows:
{[[epsilon].sub.ve]} = {[[epsilon].sub.e]} + {[[epsilon].sub.c]}.
(5)
According to the viscoelastic theory, the strain at time t caused
by constant stress a applied at time [theta] is given by:
[epsilon](t, [theta]) = J(t, [theta])[sigma]. (6)
According to Boltzmann's principal of superposition of
strains, which was modified by Neville (Neville et al. 1983) to include
the effect of aging of concrete, the summation of the strain history due
to all stress increments [DELTA][sigma]([theta]) before time (t) is
expressed as (Atrushi 2003):
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII], (7)
where: t is current time (measured from casting of concrete);
[theta] is concrete age at loading;[deLTA][sigma]([theta]) is stress
increment applied at [theta]; [epsilon](t) is total strain and J(t,
[theta]) is creep compliance.
If the stress varies continuously, Eqn (7) could be expressed as
(Du, Liu 1994):
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII]. (8)
3.1. Creep compliance of RCC material
The exponential model of creep has been attractive from the
computation point of view, because it can avoid storing the whole stress
history and made the implementation feasible comparing with other models
(Abdulrazeg et al. 2010).
The creep functions may be expressed with Dirichlet series (Wu,
Luna 2001) as:
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII], (9)
where: J (t, [theta]) is creep functions;
[[mu].sub.[gamma]]([theta]) is function of one variable, called the
reduced times; [theta] is the loading age in days,
[y.sub.[gamma]]([theta]) is experimental function.
Neglecting temperature effects, a specific form of the compliance
function is often used (Du, Liu 1994):
J(t, [theta]) = C(t, [theta]) + 1/E(t), (10)
where C (t, [theta]) is creep compliance, it can be expressed as,
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII], (11)
where [[alpha].sub.[gamma]], [[beta].sub.[gamma]],
[[delta].sub.[gamma]], D, [S.sub.[gamma]] are constants determined from
the experimental data.
E(t) is elastic modulus, and the model which developed by (Conrad
et al. 2003), has been used in this study. This model expresses the
variation of the elastic modulus of RCC material with time:
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII], (12)
where [E.sub.c] is the final elastic modulus, a and b are model
parameters.
4. Proposed models of creep and elastic with temperature effect
Bazant introduced the concept of the degree of hydration to include
the temperature influence (Bazant et al. 2004). Term of equivalent age
[[theta].sub.e], which represents the hydration period for which the
same degree of hydration is reached at a current temperature as that one
reached during the actual time (t) at a reference temperature. The
concrete age, [theta] will be replaced by equivalent age [[theta].sub.e]
in the exponential model Eqn (9):
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII], (13)
where [beta](i) is a function of current temperature and expressed
as:
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII], (a-13)
where: T (t) is a current temperature, Tr = 20[degrees]C;
[[PI].sub.h] is function of hydration degree = 2700 K. To consider the
temperature effect on the creep compliance, a function
[y.sub.[gamma]](t) is introduced as:
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII], (14)
where [[psi].sub.[tau]](t) is a function of current temperature and
expressed as:
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII], (a-14)
where [[PI].sub.[alpha]] is function of activation energy of creep
= 5000 K.
Using the introduced term of equivalent age [[tau].sub.e], which
represents the hydration period, the concrete age, [tau] will be
replaced with this equivalent age [[tau].sub.e] in the above elastic
modulus Eqn (12). So modified model includes the aging and temperature
effects on the elastic modulus (Abdulrazeg et al. 2010a).
5. Creep at variable temperature
For changing temperature conditions while the concrete is under
load, an additional creep component, the so-called transient thermal
creep, which develops at the time of a temperature increase, should be
considered (Bosnjak 2000). Transient thermal creep is interdependence
between temperature response and mechanical response, and based on that
the thermal strain rate should be made depending on the current stress
state (Thelandersson 1987):
[DELTA][[epsilon].sub.T] = [alpha][DELTA]T (1 + [xi]
[sigma]/[f.sub.c]), (15)
where: [DELTA][[epsilon].sub.T] is thermal strain increment;
[sigma] current stress; [f.sub.c] is uniaxial compressive strength at
reference temperature; [DELTA]T is temperature change; [xi] model
parameter and [alpha] coefficient of thermal expansion.
Jonasson (1994) applied Eqn (15) to young concrete and further
modified the Eqn (13) and expressed as:
[DELTA][[epsilon].sub.T] = [alpha][DELTA]T(1 + [xi]
[sigma]/[f.sub.t] sign[DELTA]T), (16)
where: [f.sub.t] is the tensile strength at reference temperature
and [xi] range between (0.1-0.7) the best value for [xi] fitted to the
test results was 0.27 (Hedlund 1996).
6. The formulation of RCC creep with temperature effects
To predict the response of the concrete in the early period of
construction, a step-by-step method is necessary. At the beginning of
each time step, deformation due to thermal variation (hydration and
environment) and creep during the current time interval are imposed.
This imposed incremental strain on any point at ith time interval is
defined as:
[DELTA][[epsilon].sub.n] = [DELTA][[epsilon].sup.e.sub.n] +
[DELTA][[epsilon].sup.c.sub.n] + [DELTA][[epsilon].sup.T.sub.n] +
[DELTA][[epsilon].sup.Trcr.sub.n], (17)
where [DELTA][[epsilon].sup.e.sub.n],
[DELTA][[epsilon].sup.c.sub.n], [DELTA][[epsilon].sup.T.sub.n],
[DELTA][[epsilon].sup.Trcr.sub.n] refer to elastic, creep, temperature
and transient thermal creep strain increment column vectors,
respectively.
Wu and Luna 2001 introduced the numerical procedure for creep
strain in mass concrete structure with temperature effects by modifying
the exponential algorithm for concrete and the final formula for the
incremental in strain (Eqn (17)) are presented below.
Let the total time interval [[t.sub.0], t] be subdivided into N
steps, for the step [[t.sub.i-1], [t.sub.i]], the creep strain increment
column vector within step [[t.sub.n-1], [t.sub.i]] may be generalized
as:
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII], (18)
where:
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII]; (a-18)
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII]l (b-18)
qn = [3.summation over ([gamma]=1)]
[[phi].sub.[gamma]n][h.sub.[gamma]n]; (c-18)
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII]; (d-18)
[Y.sub.n] = [S.sub.n] [n.summation over (j=1)]
[[psi].sub.Tj][[DELTA].sub.Tj]; (e-18)
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII]; (f-18)
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII]. (g-18)
The corresponding stress increment can be obtained:
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII]; (19)
where: [[D.sub.n]] is the elastic matrix for plane strain problem
at the "th time interval. The full details of the mathematical
derivation are given in the previous work, the authors (Abdulrazeg et
al. 2010).
7. Crack analysis
The crack development in RCC dam due to deferent loads acting on
the dam during the construction or the operation stages such as thermal
load, gravity, hydrostatic load and creep, in a given time interval
depends on the development of mechanical properties, especially elastic
modulus and tensile strength. Making reliable crack prediction
assessment involves advanced modelling of the time and temperature
dependent behaviour of the properties.
7.1. Cracking criteria of RCC gravity dam under triaxial stress
states
In order to check the safety of the dam against cracking under
Triaxial Stress States a new mathematical model has been developed
during the present study to predict the crack development in RCC dam
during the construction and operation stages. The respective failure
criteria for mass concrete in principal stress space and octahedron
stress space which proposed by (Wang, Song 2008) is adopted in the
developed model.
The cracking criterion suggested by Wang and Song (2008) is a
function of octahedral shear stress [[tau].sub.oct] and octahedral
normal stress [[tau].sub.oct]
[[sigma].sub.oct] = ([[sigma].sub.1] + [[sigma].sub.2] +
[[sigma].sub.3]/3); (a-20)
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII]. (20)
Let [[sigma].sub.1], [[sigma].sub.2] and [[sigma].sub.3] denote the
tensile stress, intermediate stress and compressive stress at failure
under triaxial C-C-T, respectively. The values of [[sigma].sub.oct]/fc
and [[tau].sub.oct]/fc will be regressed in a parabolic formula as
follows (Wang, Song 2008):
[[tau].sub.oct]/fc = 0.0655 - 0.9097 [[sigma].sub.oct]/fc
-0.08936[([[sigma].sub.oct]/fc).sup.2]. (21)
This formula to be compatible with RCC construction sequence
further modified as:
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII]. (22)
In triaxial tension [[sigma].sub.1] < [[sigma].sub.2] <
[[sigma].sub.3] < 0.00 the triaxial tensile strength is equal to
uniaxial tensile strength [f.sub.t](t). In
tension-compression--compression (T-C-C), [[sigma].sub.1] > 0.00, and
[[sigma].sub.2] < [[sigma].sub.3] < 0.00, the maximum strength is
given by Eqn (22).
The variation in the compressive strength with time is calculated
according to (ACI 1995), which relates the elastic modulus to the
compressive strength as:
E(t) = 4750[square root of [f.sub.c](t)], (23)
where E(t) is the elastic modulus, which is time and temperature
dependent Eqn (10). The tensile strength of RCC material is evaluated
using the model that developed by (Zdiri et al. 2008):
[f.sub.t] = 0.214 [f.sup.0.69.sub.c]. (24)
Taking into account this criterion, cracking on an element begins
where the relation [[psi].sub.cr] drop below the allowable value. The
following expression is defining the crack index (Abdulrazeg et al.
2010b):
[[psi].sub.cr] = [[tau].sub.oct][(t).sup.ult]/[[tau].sub.oct](t),
(25)
it can be verified that when [[psi].sub.cr] > 1.0 the element is
not cracked, and cracking occurs when [[psi].sub.cr] < 1.0.
Finally, the allowable octahedral shear stress will be determined
using Eqn (22) and based on that the crack safety factor is generated by
Eqn (25). If safety coefficient of crack is greater than one, the
element will be considered safe against crack. But if the coefficient is
less than one, crack will develop in the dam body.
7.2. Gradient cracking criteria
Design specification for concrete arch dam (Abdulrazeg 2012)
demands that the tensile stress should be controlled by the following
equation:
[epsilon]T [less than or equal to] [[epsilon].sub.p]/[K.sub.f];
(26)
[[epsilon].sub.T] = [DELTA]T x [alpha], (27)
where: [[epsilon].sub.T] is tensile strain of concrete which caused
by temperature difference [DELTA]T; [alpha] is thermal expansion
coefficient; [[epsilon].sub.p] is ultimate tensile strain of concrete;
and [K.sub.f] is safety coefficient and range from 1.3-1.8 (SL282-2003).
The laboratory test reported by Dunstan (1981) showed that a typical
value of the tensile strain capacity is 80 [micro]mm.
8. Development of finite element code
In previous discussion, the formulation in Sections 2
(temperature), Sections 6 (creep) and Sections 7 (crack analysis) are
implemented in the present research program (Abdulrazeg 2012). Based on
that, a three-dimensional finite element program was developed and the
following are the features of the finite element code.
1) Simulation of sequence of construction for both gravity and arch
RCC dam;
2) Thermal analysis;
3) Structural analysis with or without creep effect;
4) Combined thermal and structural analysis with or without creep
effect;
5) Crack safety evaluation.
The desired outcome of the modified code with respect to both two
and three-dimensional finite element method are:
--Spatial distribution of temperature and its evolution with time;
--The stress distribution during and following the dam
construction;
--Assessment of the crack occurrence either at short or long term.
The developed finite element program is written in FORTRAN language
and can work under power station environment. The flowchart shown in
Figure 1 represents the architecture of the program. The main program
calls 36 main subroutines, each main subroutine calls another
sub-subroutines and the code is about 7198 lines (Abdulrazeg 2012):
1) Divided the structure into stages according to construction
schedule;
2) Divided each stage into several times;
3) Perform the thermal analysis, if only the temperature field
analysis is desired, then the program moves to the next time step;
4) Perform stress analysis, and in case the creep is taken into
consideration, the computational procedures in Section 6 will be
preformed;
5) Performing crack prediction using the procedures in Section 7.
9. Analysis of actual RCC arch dam
The Karun III has been taken as a case study for the purpose of
verification of the developed code. The Karun III dam is a hydroelectric
dam on the Karun River in the province of Khuzestan, Iran. The dam is
unsymmetrical double curvature type, 205 m high from the foundation. Its
foundation width is 29.5 m. The arch dam design is an ideal one for a
dam built in a narrow, rocky gorge to hold back water in a reservoir.
Table 1 shows the main characteristics of the dam. Figure 2 shows
original view and plan view of Karun III arch dam. The construction of
the dam was started on 1995 and was put in operation 2005 (Karun III
technical report 1995). The dam was originally designed as conventional
concrete arch dam. In this study, RCC technology has been ascertained as
an alternative method to reduce the cost of the project.
[FIGURE 1 OMITTED]
[FIGURE 2 OMITTED]
The dam site is generally hot and occasionally humid. Summertime
temperatures routinely exceed 50[degrees]C. Khuzestan province is known
as one of the hottest state in the world.
9.1. Material properties and site conditions
The material properties for the RCC and the rock foundation are
tabulated in Table 2. These values were chosen based on values reported
in the literature for RCC materials which are used in arch RCC dam (Xie,
Chen 2005). The creep experimental data which were reported in the
literature by (Zhang 1995) for RCC material have been adopted in the
present study; these data are tabulated in the Table 3. In addition, the
average monthly air temperatures at the project site are plotted in
Figure 3 according to NASA organization (www.Eosweb.larc.nasa.gov/sse/
RETScreen). The average annual wind speed which is 4.0 m/s recorded at
the site.
[FIGURE 3 OMITTED]
9.2. Construction schedule
In this study, the construction schedule of 205.0 m height RCC arch
dam is proposed. The construction of the dam is planned according to a
similar project was reported in the literature (Xie, Chen 2005), to be
realistic, the construction schedule is adjusted based on the
corresponding geometry of the adopted project. However, during the high
temperature of the summer time, the construction will be stopped during
July, August and September. Table 4 shows the proposed construction
schedule of the dam.
9.3. Finite element modeling of RCC arch dam
The three-dimensional finite element model of the block foundation
and dam body is shown in Figure 4. The finite element of the dam body is
generated according to the construction Schedule which was given in
Table 4. Twenty node isoparametric element is used for propose of
discretization of the dam body and foundation block. 2880 isoparametric
elements are used to model the foundation block and 560 elements to
model the dam body, over all 17627 nodes have been used to define the
coordinate of the finite element mesh of the entire system.
[FIGURE 4 OMITTED]
9.4. Simulation of the initial conditions
The temperature distribution in the rock foundation and the RCC
placing temperature are the two initial conditions considered in the
analysis. In this case of study, the main annual temperature recorded
near the project site is 25.6[degrees]C it was assigned first to the all
nodes of the block foundation as an initial condition. Then heat
transfer between the atmospheric temperature and the block foundation
was performed for a period of two years using the average monthly
temperature (Ishakawa 1991). The RCC placing temperature is taken as the
environmental temperature at the casting time but not permitted to
exceed 30[degrees]C.
10. Results and discussion
10.1. Temperature distribution of Karun III RCC arch dam
According to the proposed schedule which given in Table 4, the
thermal analysis is performed. The construction was started on March
1995 and completed in October 2000. However, the construction process
was stopped every year for three months to avoid the work in very hot
weather at the construction site during the summer period (July, August
and September).
Temperature distribution in the body of the arch dam at the end of
construction for the crown cantilever of the central section and
different levels of the dam (20 m, 75 m, and 95 m) are shown in Figures
5 and 6 respectively. Higher temperatures zones are observed at the
lower elevation levels near the abutments as shown in Figure 6. This can
be anticipated to the higher thickness at these locations which provide
high insulating property compared to the upper levels where the dam
thickness decreased progressively.
In addition, high temperature concentration was observed at the
upper elevation levels (150 m and 195 m) of the dam that because, the
hydration process is still high in this part. However, the temperature
at the lower part of the dam is 42[degrees]C and it reduced to the air
temperature at the boundary condition.
[FIGURE 5 OMITTED]
[FIGURE 6 OMITTED]
10.1.1. Gradient cracking control standard
According to the methodology described in Section 7.2, allowable
gradient strain is determined and compared with a computed strain based
on the predicted temperature obtained from finite element analysis. The
maximum internal temperature is 42.0[degrees]C (determined from the
plots). The minimum temperature is 12.0[degrees]C (based on the annual
temperature cycle) taken from Figure 3. The coefficient of thermal
expansion is given in Table 2. The calculated induced strain based on
Eqn (27) is 166.8 umm, which exceeded the allowable strain (Eqn (26)).
This could be controlled by determining the proper spacing of the RCC
blocks.
10.2. Stress analysis of Karun III RCC arch dam
A viscoelastic mathematical model which involves ageing and
temperature effects (presented in Section 6) is adopted for the stress
analysis. First, the thermal analysis is performed for each time step.
Then the degree of equivalent hydration period is determined. Based on
this degree the mechanical properties such as elastic modulus (Eqn (12))
and creep compliance (Eqn (11)) are calculated. Finally, the crack
safety factor will be determined for each time step (Fig. 1).
Figure 7 shows the principal stress contours or (MPa) in the dam
body, the result indicates that, the tensile stresses developed mainly
at the dam bottom and the abutment boundaries, because of the contact
between two dissimilar materials. In addition, the tensile stress has
been observed at the upstream side (1.6 MPa) due to arch action combined
with the restraint against environmental thermal variation, which
doesn't exceed the limit according to U. S. crops of engineering
(ACI. EM 1110-2, 2006).
On the other hand, compressive stress contours are developed at the
downstream side due to the arch action and gradually decreased in the
direction of boundaries.
[FIGURE 7 OMITTED]
Figure 8 shows contour plots for the evolution of the intermediate
principal stress [[sigma].sub.2] (MPa). It can notice that, tensile
stresses developed at the same locations of the principal stress
[[sigma].sub.1] with smaller values. In addition, high compressive
stresses zones are observed at some level at the downstream side (75.0
and 150.0 m).
[FIGURE 8 OMITTED]
Figure 9 shows the distribution of the minimum principal stress 03.
High compressive stress zones concentrated at the upper part of the
upstream dam side which gradually decreased in the direction of abutment
sides. Generally, the compressive stresses developed in the dam body
during the construction are not exceeding the allowable compressive
strength specified by ACI 207 (1999).
[FIGURE 9 OMITTED]
10.3. Crack analysis and safety evaluation
Simultaneously during the stress analysis the crack safety factor
will be calculated using the procedure described in Section 7.1 at each
Gaussian point. The safety factor against cracking in any point of a
generic finite element is determined using Eqn (25).
An attempt is made to draw the crack safety factor at level of
105.0 m along the dam width for different construction levels as shown
in Figure 10. Observing Figure 10, it is verified that the crack safety
factor along the section for different construction height at that
particular lift is greater than the allowable limit. Thus, it is
considered to be safe against the crack development. However, near the
abutments of the dam, the crack safety factor is dropped below the limit
which coincides with higher tensile stress zone (Fig. 7f). Hence,
special attention must be given to locations during the design of the
dam.
[FIGURE 10 OMITTED]
Conclusion and remarks
The capability of the developed system for thermal and structural
analysis of RCC arch dam has been demonstrated through analyzing 205.0
height Karun III arch dam located in Iran. In this study, RCC technology
has been as ascertained as an alternative method. The analysis was
carried out during the construction stages only.
Based on the limitations and assumptions used in the present study,
the following points can be drawn:
--The finite element code developed in this study is capable of
simulating the structural response of arch RCC dams efficiently. This is
clearly shown from the reasonable stresses distributions obtained;
--Higher temperature zones are formed at the center part of the
dam, especially at the thicker places near the abutments which gradually
decreased in values to reach the air temperature at the boundaries. The
requirements of strength and crack resistance are greater in high Zone,
because of the adiabatic temperature is high in this zone;
--High Tensile stresses have been observed at the dam bottom and
the abutment boundaries in the upstream side section due to the
restriction from the abutment and foundation rock. This is because of
low temperature, ranging from dam foundation to abutment and there is no
transverse joint in RCC arch dam. Engineers should pay special attention
to this zone. Moreover, the tensile stress has been observed at the
upstream side due to arch action combined with the restraint against
environmental thermal variation;
--High compressive stress zones concentrated at the upper part of
the upstream dam side which gradually decreased in the direction of
abutment sides.
doi: 10.3846/13923730.2013.801897
References
Abdulrazeg, A. A.; Noorzaei, J.; Khanehzaei, P.; Jaafar, M. S.;
Mohammed, T. A. 2010. Effect of temperature and creep on roller
compacted concrete dam during the construction stages, CMES: Computer
Modeling in Engineering & Sciences 68(3): 239-268.
Abdulrazeg, A. A. 2012. Modeling of Combined Thermal and Mechanical
Actions in Roller Compacted Concrete Dam By Finite Element Method: PhD
Thesis. Civil Engineering Department, Universiti Putra Malaysia
Malaysiy.
Abdulrazeg, A. A.; Noorzaei, J.; Khanehzaei, P.; Jaafar, M. S.;
Mohammed, T. A., Thanoon, W. A. 2011. Cracking safety evaluation of
massive concrete structures, Journal of Key Engineering Materials
462-463: 1403-1408. http://dx.doi.org/10.4028/www.scientific.net/KEM.462463.1403
ACI318. 1995. Building code requirements for structural concrete.
USA: ACI 318M-95.
Agullo, L.; Aguado, A. 1995. Thermal behavior of concrete dams due
to environmental actions, Journal of Dam Eng. VI: 3-21.
American Concrete Institute. 1999. Roller-Compacted Mass Concrete,
ACI 207.5R-99, Farmington Hills.
Araujo, J. M.; Awruch, A. M. 1998. Cracking safety evaluation on
gravity concrete dams during the construction phase, Computers &
Structures 66(1): 93-104.
http://dx.doi.org/10.1016/S0045-7949(97)00048-5
Atrushi, D. S. 2003. Tensile and compressive creep of early age
concrete: testing and modelling: PhD. The Norwegian University of
Science and Technology.
Bayagoob, K. H.; Noorzaei, J.; Abdularzeg, A. A.; Al-Karni, A. A.;
Jaafar, M. S. 2010. Coupled thermal and structural analyses of roller
compacted concrete dams by three dimensional finite element method, J.
Structural Engineering and Mechanics 36.
Bayagoob, K. H.; Noorzaei, J.; Jaafar, M. S.; Thanoon, W. A.;
Abdularzeg, A. A. 2010. Modelling heat exchange between RCC dam and
reservoir, J. Engineering and Computational Mechanics, Ice 163.
Bazant, Z. P.; Cusatis, G.; Cedolin, L. 2004. Temperature effect on
concrete creep modeled by microprestress solidification theory, Journal
of Engineering Mechanics Proceedings of the ASCE 130(Special issue:
Constitutive modeling of geomaterials): 691-699. http://dx.doi.org/10.
1061/(ASCE)0733-9399(2004)130:6(691)
Bosnjak, D. 2000. Self-induced cracking problems in hardening
concrete structures: PhD. Norwegian University of Science and
Technology, ISBN 82-7984-151-2.
Cervera, M.; Oliver, J.; Prato, T. 2000. Simulation of construction
of RCC dams. I: temperature and aging, Journal of Structural Engineering
126(9): 1062-1069. http://dx.doi.org/10.1061/(ASCE)0733
9445(2000)126:9(1062)
Conrad, M.; Aufleger, M.; Malkawi, A. 2003. Investigations on the
modulus of elasticity of young RCC, in Berga, L. (Ed.). Proceedings of
the Fourth International Symposium on Roller Compacted Concrete (RCC)
Dams, Madrid, Spain, 729-733.
Crichton, A.; Benzenati, I.; Qiu, T.; Williams, J. 1999. Kinta RCC
dam--are over-simplified thermal structural analyses valid, ANCOLD
Issue. 10 p.
Du, C.; Liu, G. 1994. Numerical procedure for thermal creep stress
in mass concrete structures, Communications in Numerical Methods in
Engineering 10(7): 545-554. http://dx.doi.org/10.1002/cnm.1640100706
Dunstan, M. R. H. 1981. Rolled concrete for dam--laboratory trial
of high fly ash content concrete, CIRIA Technical Note 105, London.
Hedlund, H. 1996. Stresses in high performance concrete due to
temperature and moisture variations at early ages: Licentiate Thesis.
Lulea University of Technology.
Ishikawa, M. 1991. Thermal stress analysis of a concrete dam,
Computers & Structures 40(2): 347-352.
http://dx.doi.org/10.1016/0045-7949(91)90360-X
Jonasson, J. E. 1994. Modelling of temperature, moisture and
stresses in young concrete: PhD Doctoral Thesis. Lulea University of
Technology.
Luna, R.; Wu, Y. 2000. Simulation of temperature and stress fields
during RCC dam construction, Journal of Construction Engineering and
Management 126(5): 381-388.
http://dx.doi.org/10.1061/(ASCE)0733-9364(2000) 126:5(381)
Malkawi, A. I. H.; Mutasher, S. A.; Qiu, T. J. 2003.
Thermal-structural modeling and temperature control of roller compacted
concrete gravity dam, Journal of performance of constructed facilities
17(4): 177-187. http://dx.doi.org/
10.1061/(ASCE)0887-3828(2003)17:4(177)
Neville, A. M.; Dilger, W. H.; Brooks, J. J. 1983. Creep of plain
and structural concrete. New York Construction Press London. 361 p.
Noorzaei, J.; Bayagoob, K. H.; Thanoon, W. A.; Jaafar, M. S. 2006.
Thermal and stress analysis of Kinta RCC dam, Engineering Structures
28(13): 1795-1802. http://dx.doi.org/10.1016/j.engstruct.2006.03.027
Nilipour, N. 2003. Study of arch concrete dams constructed by RCC
method, Switzerland (in Press).
Penghui, L.; Hong, C. 2007. 3-D Simulating analysis for thermal
control during constructionperiod on Dahuashui RCC arch dam, in 5th
International Symposium on Roller Compacted Concrete Dam, Guiyang,
China, 577-581.
Qiuhua, C. 2003. New design method of RCC high arch dam, in Berga,
L. (Ed.). The Proceedings of the Fourth International Symposium on
Roller Compacted Concrete Dams, Madrid, Spain. Taylor & Francis:
427-430.
Santurjian, O.; Kolarow, L. 1996. A spatial FEM model of thermal
stress state of concrete blocks with creep consideration, Computers
& Structures 58(3): 563-574.
http://dx.doi.org/10.1016/0045-7949(95)00156-B
Saetta, A.; Scotta, R.; Vitaliani, R. 1995. Stress analysis of
concrete structures subjected to variable thermal loads, Journal of
Structural Engineering 121(3): 446-457.
http://dx.doi.org/10.1061/(ASCE)0733-9445(1995)121: 3(446)
Sergerlind, L. J. 1984. Applied finite element analysis. 2nd
edition. New York: John Wiley and Sons.
Shuping, H.; Ping, H.; Yaozhen, Y.; Baoying, D.; Ping, Y. 1999. The
emulation analysis of thermal stresses on RCC arch dams, in
International Symposium on Roller Compacted Concrete, China, 482-491.
The consalting Eng. Mahab Ghods- Akerz. 1995. Transmitals of the
Karun III Dam Report Design of Dam.
Thelandersson, S. 1987. Modeling of combined thermal and mechanical
action in concrete, Journal of Engineering Mechanics 113(6): 813-906.
http://dx.doi.org/10.1061/ (ASCE)0733-9399(1987)113:6(893)
Wang, H.; Song, Y. 2008. Behavior of dam concrete under biaxial
compression-tension and triaxial compression-compression-tension
stresses, Frontiers of Architecture and Civil Engineering in China 2(4):
323-328. http://dx.doi.org/10.1007/s11709-008-0043-5
Wu, Y.; Luna, R. 2001. Numerical implementation of temperature and
creep in mass concrete, Finite elements in analysis and design 37(2):
97-106. http://dx.doi.org/10.1016/S0168-874X(00)00022-6
Xie, H.; Chen, Y. 2005. Influence of the different pipe cooling
scheme on temperature distribution in RCC arch dams, Communications in
Numerical Methods in Engineering 21(12): 769-778.
http://dx.doi.org/10.1002/cnm.793
US Army Corps of Engineers. 2006. Roller-Compacted Concrete. EM
1110-2-2006. Washington, DC.
Zdiri, M.; Ouezdou, M. B.; Neji, J. 2008. Theoretical and
experimental study of roller-compacted concrete strength, Magazine of
Concrete Research 60(7): 469-174.
http://dx.doi.org/10.1680/macr.2007.00002
Zhang, M. L. 1995. Study on structural treatment, stress and
stability of roller compacted concrete gravity dam: Master's
Thesis. Tsinghua University, Beijing, China.
Zhang, X.; Li, S.; Chen, Y.; Chai, J. 2009. The development and
verification of relocating mesh method for the computation of
temperature field of RCC dam, Advances in Engineering Software 40(11):
1119-1123. http://dx.doi.org/10.1016/j.advengsoft.2009.05.006
Zhiqi, H.; Huifen, Z.; Jianping, H.; Yirui, Z. 2007. Simulation
analysis on thermal stress of Longtan RCC gravity dam, in Jinsheng, J.;
Berga, L.; Guoxin, Z.; Gaixin, C.; Cuiying, Z. (Eds.). New Progress on
Roller Compacted Concrete Dams, Guiyang, China, 551-556.
Aeid Ali ABDULRAZEG completed his PhD study at the Universiti of
Putra Malaysia. He is currently lecturer at the civil engineering
department of Omar Al Mukhtar University. His main area of interest is
the finite element analysis of complex structures.
Jamaloddin NOORZAEI completed his PhD study at the University of
Roorkee, India. His research interests include computational techniques
in civil engineering applications especially those related to structural
engineering, soil- structure interaction and earthquake engineering. He
was Professor and Head of the Structural Engineering Research group at
the Universiti Putra Malaysia (UPM).
Mohamed Saleh JAAFAR obtained his PhD from the University of
Sheffield. Currently Professor and Deputy Vice Chancellor of Universiti
of Putra Malaysia. His research interests include concrete and
prestressed concrete structures, high performance concrete and
structural conditions assessment.
Parvin KHANEHZAEI obtained her MSc degree from the Universiti of
Putra Malaysia. She is currently a PhD candidate at the same University.
Her main area of interest is soil-structure interaction and structural
engineering.
Thamer Ahmed MOHAMED completed his PhD study at the Universiti
Putra Malaysia, Malaysia. Currently Professor of the Faculty of
Engineering UPM, Malaysia. His research interests include hydraulic and
hydrologic modeling, sediment transport, urban drainage, groundwater
modeling.
Aeid Ali ABDULRAZEG (a), Jamaloddin NOORZAEI (b,c), Mohamed Saleh
JAAFAR (b), Parvin KHANEHZAEI (b), Thamer Ahmed MOHAMED (b)
(a) Civil Engineering Department, Omar Al Mukhtar University,
El-Beida, Libya
(b) Civil Engineering Department Universiti Putra Malaysia, 43400
UPM- Serdang, Malaysia
(c) Institute of advance Technology, Universiti Putra Malaysia,
43400 UPM- Serdang, Malaysia
Received 08 Dec 2011; accepted 20 Feb 2012
Corresponding author: Aeid Ali Abdulrazeg
E-mail: aied@omu.edu.ly
Table 1. Main characteristics of Karun III concrete arch dam
Characteristic Quantity
Maximum height above foundation 205.0 m
Crest width 5.5 m
Base width 29.5 m
Crest length 462.0 m
Placed concrete 1300000.0 [m.sup.3]
Reservoir normal capacity 2,970,000,000 [m.sup.3]
Table 2. Thermal and mechanical properties for
Karun III concrete arch dam
Characteristic RCC Rock
Cement (Kg/[m.sup.3]) 90
Fly ash (Kg/[m.sup.3]) 110
Coefficient of thermal expansion 3.04E-6 4.2E-6
Thermal conductivity(KJ/m h [degrees]C) 8.314 10.0
Specific heat (J/(kg. K)) 1080 1500
Elastic Modulus (MPa) 18200 24000
Table 3. Creep data for RCC and CMC materials (Zhang 1995)
Material [[alpha]. [[beta].sub.i] [[delta].sub.i] D
sub.i]
CVC 1 0.35494 0.4836 0.35361 0.835
2 3.7335 -0.186 0.01248
3 2.5644 0.1378 0.03264
RCC 1 0.05886 0.38362 1.356 4.2808
2 7.4729 -11.115 0.08919
3 5.2079 7.9619 0.078675
Table 4. Construction schedule of
Karun III RCC Arch Dam
Time of pouring Height of
(D-M-Y) casting (m)
3/1/1995 1.2
3/30/1995 3.0
4/20/1995 6.0
5/14/1995 9.0
9/7/1995 12.0
10/1/1995 15.0
10/25/1995 18.0
11/18/1995 21.0
12/11/1995 24.0
1/5/1996 27.0
1/29/1996 30.0
2/22/1996 33.0
3/16/1996 36.0
4/2/1996 39.0
4/21/1996 42.0
5/26/1996 45.0
9/21/1996 48.0
10/14/1996 51.0
11/8/1996 54.0
12/1/1996 57.0
12/25/1996 60.0
1/19/1997 63.0
2/12/1997 66.0
3/5/1997 69.0
3/29/1997 72.0
4/23/1997 75.0
9/16/1997 78.0
10/10/1997 81.0
11/3/1997 84.0
12/27/1997 87.0
1/20/1998 90.0
2/16/1998 93.0
3/9/1998 96.0
4/3/1998 99.0
5/27/1998 102.0
6/10/1998 105.0
7/1/1998 108.0
10/1/1998 111.0
10/21/1998 114.0
11/10/1998 117.0
11/30/1998 120.0
12/20/1998 123.0
1/10/1999 126.0
1/30/1999 129.0
2/20/1999 132.0
3/10/1999 135.0
3/30/1999 138.0
4/21/1999 141.0
5/11/1999 144.0
5/29/1999 147.0
6/20/1999 150.0
7/10/1999 153.0
10/1/1999 156.0
10/20/1999 159.0
11/10/1999 162.0
11/29/1999 165.0
12/20/1999 168.0
1/11/2000 171.0
1/29/2000 174.0
2/21/2000 177.0
3/11/2000 180.0
3/30/2000 183.0
4/19/2000 186.0
5/11/2000 189.0
5/30/2000 192.0
6/19/2000 195.0
7/10/2000 198.0
10/1/2000 201.0
10/21/2000 205.0