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8/9/2019 Global Buckling Behavior of SuGlobal buckling behavior of submarine unburied pipelinesbmarine Unburied Pipelines
1/12
J. Cent. South Univ. (2013) 20: 2054−2065
DOI: 10.1007/s11771-013-1707-4
Global buckling behavior of submarine unburied pipelines under
thermal stress
GUO Lin-ping(郭林坪), LIU Run(刘润), YAN Shu-wang(闫澍旺)
State Key Laboratory of Hydraulic Engineering Simulation and Safety (Tianjin University), Tianjin 300072, China
© Central South University Press and Springer-Verlag Berlin Heidelberg 2013
Abstract: Buckling of submarine pipelines under thermal stress is one of the most important problems to be considered in pipeline
design. And pipeline with initial imperfections will easily undergo failure due to global buckling under thermal stress and internal
pressure. Therefore, it is vitally important to study the global buckling of the submarine pipeline with initial imperfections. On the
basis of the characteristics of the initial imperfections, the global lateral buckling of submarine pipelines was analyzed. Based on the
deduced analytical solutions for the global lateral buckling, effects of temperature difference and properties of foundation soil on pipeline buckling were analyzed. The results show that the snap buckling is predominantly governed by the amplitude value of initial
imperfection; the triggering temperature difference of Mode I for pipelines with initial imperfections is higher than that of Mode II; a
pipeline with a larger friction coefficient is safer than that with a smaller one; pipelines with larger initial imperfections are safer than
those with smaller ones.
Key words: submarine pipeline; lateral buckling; analytical solution; initial imperfection; subsoil friction resistance
1 Introduction
Since 1970’s, submarine pipelines gradually
become the main way in the offshore engineering totransport gas and oil all over the world. In-service
hydrocarbons must be transported at high temperature
and high pressure to ease the flow and prevent
solidification of the wax fraction. Thermal stress together
with Poisson effect will cause the steel pipe to expand
longitudinally. If such expansion is resisted, for example,
by friction effects of the foundation soil over a kilometer
or so of pipeline, compressive axial stress will be set up
in the pipe-wall. Once the value exceeds the constraint of
foundation soil on the pipeline, sudden deformation will
occur to release internal stress, which is similar to thesudden deformation of strut due to stability problems,
and lateral or vertical global buckling may occur. Studies
show that lateral modes will be dominant in pipelines
unless the line is trenched or buried [1]. Since the pipe
holds a great deal of hydrocarbon, once the pipeline
buckles or even yields, the hydrocarbon will leak out. This
will not only waste resources but also endanger the living
conditions of halobios and human beings. Therefore,
study on global buckling of submarine pipelines under
thermal stress has a great practical significance.
There is an early start on study of global lateral
buckling of unburied or semi-buried submarine pipelines.
LYONS [2] discovered that traditional Coulomb friction
model can be used to represent the force of sand to the
pipeline, while it can’t be applied to soft clay when the pipeline buckles in the lateral plane, which is obtained
from tests and numerical simulations. Based on
achievements of KERR on lateral global buckling of
continuously welded track, HOBBS [1] gave the
analytical solutions to lateral and vertical global buckling
of ideal submarine pipelines; TALOR and GAN [3]
provided analytical solutions to ideal submarine
pipelines based on the lateral soil resistance changes with
its displacement. SCHOTMAN [4] presented the
relationship of soil resistance versus pipeline
displacement by theoretical analysis and numericalsimulations; TAYLOR and GAN [5] studied effects of
initial imperfection on pipeline global buckling, and
pointed out limitations of the relationship between
temperature difference and buckling length proposed by
HOBBS [1]. PRESTON et al [6] presented a method to
control global lateral buckling by FEM, which applied
feed length on pipeline; PEEK and YUN [7] showed the
effects of flotation on lateral global buckling of
submarine pipelines. DUAN et al [8], ZHAO [9], and
LIU [10] did research on pipeline global buckling under
Foundation item: Project(51021004) supported by Innovative Research Groups of the National Natural Science Foundation of China; Project(NCET-11-
0370) supported by Program for New Century Excellent Talents in Universities of China; Project(40776055) supported by the National
Natural Science Foundation of China; Project(1002) supported by State Key Laboratory of Ocean Engineering Foundation, China
Received date: 2012−09−10; Accepted date: 2013−04−10
Corresponding author: LIU Run, Professor, PhD; Tel: +86−22−27404286; E-mail: [email protected]
8/9/2019 Global Buckling Behavior of SuGlobal buckling behavior of submarine unburied pipelinesbmarine Unburied Pipelines
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J. Cent. South Univ. (2013) 20: 2054−2065 2055
thermal stress. LIU et al [11], and GAO et al [12] studied
global buckling modes of submarine pipeline combining
practical engineering.
On the basis of the characteristics of the initial
imperfections, the global lateral buckling of submarine
pipelines is analyzed. Based on the deduced analytical
solutions, mode I and mode II, for global lateral buckling,
effects of temperature difference and properties of
foundation soil on pipeline buckling are investigated in
great details.
2 Analytical solutions of global lateralbuckling
2.1 Global lateral buckling modes
The straight pipeline, with uniform cross section
and without initial imperfection, is the ideal pipeline.Probable global lateral buckling modes of ideal pipelines,
according to Ref. [2], are shown in Fig. 1. In practice,
lateral mode I is the most significant symmetrical lateral
mode, lateral mode II is the most significant
skew-symmetrical lateral mode, and lateral mode III and
VI are subordinate forms of lateral modes I and II,
respectively. Approximately, all four modes can be
considered to be a part of lateral mode ∞. Therefore, in
this work, mode I and mode II are mainly analyzed by
employing small deformation theory, and assuming that
the stress strain relationship obeys Hook’s law.
2.2 Analysis of pipeline on lateral mode I
2.2.1 Ideal pipeline
Global lateral buckling of submarine pipelines
under different temperature and pressure conditions is an
analogy with stability problem of strut. Figure 2
describes the topology and axial force distribution of the
global lateral mode I.
The lateral bending moment equilibrium equation
for the idealized pipelines is given by
08
)4(dd
22
L2
2
L xq Pv x
v EI (1)
Fig. 1 Lateral buckling modes: (a) Mode I; (b) Mode II;
(c) Mode III; (d) Mode VI; (e) Mode V
where EI denotes flexural rigidity, m4; v is the lateral
deformation of the buckling region, m; q is the
submerged weight of pipeline per unit length, kN; P is
the axial force in the buckling region, kN; L is the buckling length, m; L is the fully mobilized lateral
friction coefficient of foundation soil to pipeline [13].
EI
P n 2 (2)
Equation (1) has the solution of
2
22L2L
8
8
2sincos
n
Ln
P
q x
P
qnx Bnx Av
(3)
According to boundary conditions: ,00' x xv
,02/ L xv ,02' L x xv we may write
Fig. 2 Deformation and force distribution for first lateral buckling mode
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J. Cent. South Univ. (2013) 20: 2054−20652056
18
2cos
1 22
4
L0m
Ln
nL EI n
qvv x
EI qL
4
L310407.2 (4)
where vm is the buckling amplitude of the buckling
region, m.
Using Eqs. (2) and (4), the relationship of P versus
vm in the buckling region can be obtained by
21
L2
962.376.80
mv
q EI
L
EI P
(5)
The reduction in axial force in the pipeline equals
friction force in axial direction of the buckling region:
sAA
02
qLqL P P (6)
where Ls is the slip length of the buckling region, m, and
the relationship of Ls versus P can be obtained as
72
L602sA 103988.7
2
)(
2 L
EI
q
AE
L P P
AE
qL
(7)
And the relationship of L versus P can be rewritten
as
2/1
52
L
A
5A0 1106390.6
2
L
EI
AEqqL P P
(8)
The axial force P 0, caused by temperature and
internal pressure, is the reason for buckling. To
conveniently analyze this problem, internal pressure is
converted to temperature difference, which is: T =
);2/()]5.0)(2([ t E t D p therefore, the relationship
of P 0 versus temperature difference is
)(0 T T AE P (9)
where D is the outer diameter of the pipeline, m; E is the
elastic modulus, kPa; α is the coefficient of linear
thermal expansion, °C−1; )( T T is the temperaturedifference; p is the positive pressure difference, kPa;
is the Poisson ratio, which is taken as 0.3 generally; t is
the pipe wall thickness, m.
Using Eq. (8), the relationship of )( T T versus L can be obtained as
2
76.80)( A2
qL L EI T T AE
2/12
L
A
55
1106390.6
EI
AEqL
(10)
With Eq. (7), the relationship of vm versus L can be
obtained:
4/1
L
m7514.4
q
EI v L
(11)
Thus, the relationship of vm versus
)( T T
is
)( T T AE
4/1
L
mA
2/1
m
L 4257.2962.3q
EI vq
v
q EI
2/14/5
L
m
2
L
A
19119.0
q
EI v
EI
AEq
(12)
The bending moment M reaches the maximum at
x=0:
2Lm 37069.0 qL EIv M xx (13)
And the maximum total stress σ m in the buckling
region can be obtained as
I
D M
A
P
2
mm (14)
Comparing this bending plus axial stress with the
yield stress, it can be known whether the pipeline yields.
2.2.2 Pipeline with initial imperfection
Pipeline with imperfection will keep on deforming
from the imperfection position [14]. Topology and axial
load distribution of a buckling pipeline with single-arch
imperfection are shown in Fig. 3.
Fig. 3 Deformation and load analysis for first lateral buckling mode
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The global buckling of pipelines is induced by
external forces. According to the virtual work principle,
the work done by the external forces equals the strain
energy (V ) developing inside the loaded material.
According to the method to calculate the strainenergy, for members with length of l , when pure bend
occurs, the strain energy is
x EI
x M V
l d
2
)(
0
2
(15)
where I is the inertia; E denotes the elastic modulus; M ( x)
is the bending moment of the member.
The strain energy can also be expressed by the
tension force F :
x EA
F V
l d
2
0
2
(16)
where F denotes the axial force of the member; A is its
section area.
Strain in the pipeline is a function of the bending
moment, the axial friction force and the axial force in the
buckling region. Therefore, the strain energy in the
pipeline can be obtained by [4]
xv EI
xvv EI
V L
L xx
/ L
xx xx d)(2
d)(2
2/
2/
2'
2
0
2'0'
0
0
xqv xvvq L
L
Ldd)(
2/
2/A
2/
00A
0
0
xv P xvv P L L x x x
Ld)(
2d)()(
2
/2
2/
2'
2'0
2'
2/
0 0
0
(17)
where L0 is the length of the imperfection; v′ x is the
first-order derivative of the deformation; v0′ x is the
first-order derivative of the imperfection; v′ xx is the
second-order derivative of the deformation; v0′ xx is the
second-order derivative of the imperfection.
To determine the trigger temperature difference of
the global buckling, the minimum strain energy should
be determined first [15]. Solve the equation: dV /dvm=0,
and the relationship between buckling length and theaxial load in the buckling region is
2
012 6.75
176.80 L
L R
L
EI P (18)
where
6301.2)/4493.4sin(1603.4 01 L L R
}1/
)/1(4493.4sin
1/
)/1(4493.4sin
0
0
0
0
L L
L L
L L
L L
Based on the force analysis of the slipping part, the
relation between P and P 0 can be
sAA
02
qLqL
P P
(19)
The relationship between the axial load P and
temperature difference ∆T can be obtained from features
of slipping parts [16]. And the relationship between
temperature difference and the buckling length L is
2
01
2 60.75176.80
L
L R
L
EI T AE
2/12
A70
72
LA5
2)(1066597.1
qL L L
I
Aq (20)
Since L is associated with vm, based on the
relationship of temperature difference and buckling
length, the relationship of temperature difference and
buckling amplitude can be obtained.
2.3 Analysis on lateral mode II
2.3.1 Ideal pipeline
Since the lateral mode II is an antisymmetric mode,
a half of the buckled region is analyzed for simplification.
Figure 4 details the topology and axial force distribution
of lateral mode II [2].
The bending moment equation is the same as the
lateral mode I, therefore, the solution can be written as
432
2L
21
2
sincos A x A x
EI n
qnx Anx Av
(21)
Taking boundary conditions:
Fig. 4 Deformation and force distribution for second lateral buckling mode
8/9/2019 Global Buckling Behavior of SuGlobal buckling behavior of submarine unburied pipelinesbmarine Unburied Pipelines
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J. Cent. South Univ. (2013) 20: 2054−20652058
00 xv , 00' x xxv , 0 L xv , 0' L x xv
into Eq. (21), the constants A1 to A4 can be obtained:
EI n
q A
nLnLnL
nLnLnLnL
nL
EI n
q A
nLnLnLnL
nLnLnLnL
EI n
q A
EI n
q A
4
L4
3
L3
2
4
L2
4
L1
sincos
)cos1(sincos2
cossin
2
)()cos1(sin
(22)
Introduce Eq. (22) into Eq. (21), employ the
antisymmetric condition [17−18]: 0'
L x xx
v into
Eq. (21), and it can be obtained that,
2πnL (23)
Use Eqs. (21), (22) and (23), and the buckling
deformation v can be obtained as
22
4
4L
π2π2
sinππ2
cos1π16 L
x
L
x
L
x
L
x
EI
qLv
,
0≤ x≤ L (24)
x=0.346 4 L, where the buckling amplitude occurs,
can be obtained from boundary condition 0' xv ( x (0,
L)). Take the value of x into Eq. (24):
EI
qLv
4L3
m 105531.5 (25)
Introduce Eq. (23) into P =n2 EI , and the axial force
in the buckling region is
2478.39
L
EI P (26)
Use Eqs. (25) and (26), and the relationship of P
versus vm can be obtained:
2/1
m
L2936.2
v
qEI P
(27)
The axial deformation at x= L is
72L602sL 10715.8)(
2 L
EI
q
AE
L P P
AE
qL
(28)
The equilibrium of axial force is
sAA0 qLqL P P (29)
With Eqs. (28) and (29), the relationship of P 0
versus P can be obtained:
5
2
L4
A0
110743.1 L
EI qAE qL P P
L
A2/1
L
A
2L
2A 12
(30)
The relationship of )( T T versus L can be
obtained:
qL L
EI T T AE A2478.39)(
2/12
L
A52
L4 11
110743.1
L
EI qAE
L
A1
(31)
The maximum bending moment M m can be obtained
with the boundary condition 0' xxxv :
2L'm 8108.0 qL EIv M xx (32)
2.3.2 Pipeline with initial imperfection
Topology and axial load distribution of a buckling
pipeline, with a double-arch imperfection, are shown in
Fig. 5 [19].
Fig. 5 Deformation and force analysis for second lateral buckling mode
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The strain energy in the pipeline can be obtained:
xv EI
xvv EI
V L
L xx
L
xx xx d)(2
d)(2
2'
0
2'0'
0
0
xqv xvvq L
L
Ldd)(
A
0
0A0
0
xv P xvv P L L x x x
Ld)(
2d)()(
2
2'
2'0
2'
0 0
0
(33)
To determine the trigger temperature difference of
pipeline global buckling, the minimum strain energy
should be determined first [20−21]. Solve the equation,
dV /dvm=0, and the relationship between buckling length
and the axial load in the buckling region can be deduced:
2
0
32
2
2
ππ35
31
π4
L
L R
L
EI P (34)
where
L L
L L
L L L L L L R /π2
)/(1
)/π)(/()/π2sin( 02
0
02
002
)/()/π2cos(1π 00 L L L L L
Based on the force analysis of the slipping part, the
relation between P and P 0 can be obtained:
sAA0 qLqL P P (35)
The relationship between the axial load P and
temperature difference ∆T can be obtained from the force
analysis of slipping parts [22−25]. And the relationship
between temperature difference and the buckling length
L can be obtained:
2
0
3
2
2
4
ππ35
31
π4
L
L R
L
EI T AE
2/1
2A
70
732
LA4 )()(10743.1
qL L Lq
I E
A
(36)
3 Case study
3.1 Case introduction
The outer diameter of the concerned pipeline is
355.6 mm, and the thickness of the pipe wall is 12.7 mm.
The designed internal pressure and temperature
difference are 7.6 MPa and 48 °C, respectively. With
equation ],2/)5.0([ t E pDT the equivalenttemperature difference can be determined as 57 °C. The
length of the analyzed part is 500 m, and the initial
imperfection amplitude is 300 mm. Design parameters of
pipeline and properties of foundation soil are presented
in Table 1 and Table 2.
3.2 Analysis results
The analytic method mentioned above is employedto predict the global lateral buckling of pipelines in this
case. The friction factor between the pipeline and subsoil
is 0.3 according to the geology condition. Figure 6 shows
the shape and values of the pipeline deformation. The
x-coordinate denotes the horizontal distance from
midpoint of pipeline. The analysis results show that with
the bending plus axial stress reaching the material yield
strength, the corresponding temperature differences are
57.8 °C and 65.4 °C for Mode I and Mode II,
respectively.
It can be known from Fig. 6 that, with the increase
of temperature difference, when temperature difference
is less than 20 °C, the buckling amplitude increases
slowly. Once the temperature difference is larger than 20
°C, the buckling amplitude will increase obviously. The
triggering temperature differences of Mode I and Mode
II are 20.89 °C and 20.75 °C, respectively. And it’s
obvious in Fig. 6 that, the increase of amplitude is not
uniform with the same increase interval of temperature
difference.
Table 1 Properties of pipeline
Elastic
modulus,
E /kPa
Poisson
ratio,
External
radius,
r /m
Wall
thickness,
t /m
Thermal
expansion coefficient,
α/(m·°C−1)
Bulk
density/
(kN·m−3)
Yield stress of
steel/MPa
Seawater
density/
(kg·m−3)
2.07×1011 0.3 0.177 8 0.012 7 1.17×10−5 7 850 448 1 025
Table 2 Physic-mechanical properties of soils
Consolidated
quick shear testCompression test
C v/
(10−4cm2·s−1) Number
of soilSoil e I p I L
c/kPa /(°) a1−2/MPa−1 E s/MPa 100 kPa 200 kPa
Coefficient
of permeability,
k /(10−7cm·s−1)
Thickness
of soil/m
1 Clay 1.747 25.91 1.55 11.10 9.90 1.52 1.86 2.90 2.71 2.760 3.0−9.5
1 Muckyclay 1.149 17.10 1.25 15.82 13.8 0.83 2.99 10.33 14.47 29.540 1.0−4.0
2Mucky
clay1.225 20.43 1.15 16.92 12.2 0.94 2.45 12.9 11.62 0.390 4.3−6.2
8/9/2019 Global Buckling Behavior of SuGlobal buckling behavior of submarine unburied pipelinesbmarine Unburied Pipelines
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Figure 7 presents the characteristics of the pipeline
global buckling with the friction coefficient of 0.3 and
the initial imperfection amplitude of 300 mm in the case.
The temperature difference corresponding to the
point, as marked in Fig. 7(a), is defined as the safe
temperature difference or triggering temperature
difference. Once the temperature difference is higher
than this value, the global buckling will happen
continuously until the stress in the pipe wall reaches the
yield stress. And the pipeline would not suffer the global
buckling failure if the design temperature difference is
lower than the triggering temperature difference.
It can be known from Fig. 7(a) that the triggering
temperature difference of Mode I is higher than that of
Mode II, which means that, Mode II is easier to occur
than Mode I. The two ending points in Fig. 7(b) imply
that the maximum bending plus axial stresses under thedesigned temperature difference and pressure are
444 MPa and 334 MPa for Mode I and Mode II,
respectively. This also verifies that Mode II is easier to
occur than Mode I and Mode II is much safer than Mode
I while the global buckling occurs.
In order to investigate more detailed regularity of
pipeline global buckling, the influencing factors, such as
the soil friction resistance and the initial imperfection,
are analyzed in following section.
4 Influencing factors on pipeline globalbuckling
4.1 Influence of subsoil friction resistance
4.1.1 Impact on triggering temperature difference
In order to analyze the effect of the subsoil friction
resistance on pipeline global buckling, temperature
difference of pipelines with imperfection amplitude of
300 mm, which is common in practice and different
pipe-subsoil friction coefficient of 0.1, 0.2, 0.3 and 0.5
are applied in pipeline global buckling analysis. Figure 8
shows the main results. It can be seen that, as to pipeline
with the same initial imperfection amplitude and
different friction coefficients, the larger the frictioncoefficient, the larger the triggering temperature
difference. This indicates that with large subsoil
resistance, the pipeline will not be easy to occur global
buckling.
4.1.2 Impact on buckling shape
In order to investigate the effect of the subsoil
friction resistance on the shape of the pipeline global
Fig. 6 Horizontal distance from midpoint of pipeline: (a) Mode I; (b) Mode II
Fig. 7 Buckling characteristics of pipeline: (a) vm vs ∆T ; (b) vm vs σ m
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buckling, the same imperfection amplitude and different
temperature differences are used in the analysis. A half of
analyzed model of the pipeline with the global buckling
is drawn in Fig. 9 with the temperature difference of
30 °C.
It can be seen that, as to pipeline with the same
initial imperfection amplitude under the same
temperature difference conditions, the larger the
pipe-subsoil friction resistance is, the smaller the
buckling amplitude and buckling length of the pipeline
are. This suggests that if the pipe-subsoil friction
resistance is large enough, the length of the pipeline
global buckling segment will be very small. On the
contrary, with the small friction resistance, the pipeline
global buckling segment will be quite long under the
same temperature difference conditions.
4.1.3 Impact on maximum compressive stressIn order to investigate the effect of the subsoil
friction resistance on the maximum compressive stress in
the pipe wall, the same imperfection amplitude and
different temperature differences are used in the analysis.
The analyzed results with temperature difference of
50 °C are shown in Fig. 10.
It can be seen from Fig. 10 that, as to pipeline with
the same initial imperfection and different pipe-subsoil
friction coefficients under the same temperature
difference condition, the larger the friction coefficient is,
the lower the maximum compressive stress is. This
indicates that pipeline with larger pipe-subsoil friction
resistance is safer than the pipeline with the smaller one.
All the above analysis results are tabulated in Table
3. Table 3 shows that with the increase of pipe-subsoil
friction resistance, the triggering temperature difference
increases, and the buckling length, amplitude and
bending plus axial stress all decrease, which indicates
that the large subsoil friction resistance will make the
pipeline safer.
4.2 Influence of initial imperfection
4.2.1 Impact on temperature difference
To analyze the impact of initial imperfection ontemperature difference, temperature difference of
pipelines with different initial imperfections amplitudes,
100 mm, 200 mm, 300 mm, 500 mm, are introduced in
the analysis. Figure 11 shows the analyzing results. In
the analysis, the friction coefficient between the pipeline
and subsoil is 0.3, which is commonly used in practice.
It can be seen from Fig. 11 that the snap buckling
Fig. 8 Comparison of temperature difference: (a) Mode I; (b) Mode II
Fig. 9 Horizontal distance from midpoint of pipeline: (a) Mode I; (b) Mode II
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Fig. 10 Comparison of bending plus axial stress
phenomenon is predominantly governed by vom. Only theideal pipeline or pipelines with relatively small
imperfections, such as 100 mm of Mode I, display the
maximum temperature difference together with the
associated snap buckling phenomenon [1]. When the
curve coincides with the left branch, the buckling shape
of the pipeline is equivalent to the first kind of stability
problem. This kind of global buckling can occur only if
the foundation soil can provide enough restraint to the
pipeline.
For the unburied pipeline, the restraint of
foundation soil comes from friction force only, therefore,
the global buckling shape of pipeline corresponding to
the left branch cannot occur or it’s an unstable buckling
stage. When the curve coincides with the right branch of
the curve, the global buckling regulation of the pipeline
is equivalent to the second kind of stability problem of
Euler buckling for a slender column. This means that
with the increase of temperature difference, theamplitude increases or is even damaged. This kind of
buckling also indicates that the increase of global
buckling segment length is the only way to increase the
friction resistance between the subsoil and pipeline for
unburied condition. However, once the imperfection
exceeds some value, such as 200 mm in Mode I and 100
mm in Mode II, the snap buckling phenomenon will
disappear, and the stable post-buckling only takes place.
Figure 11 indicates that the triggering temperature
difference of ideal pipeline is larger than that of pipeline
with imperfection. There is also an interesting
phenomenon that once the temperature difference
exceeds some value, such as 30 °C in this analysis,
buckling amplitudes of pipeline with different initial
imperfections are nearly the same under the same
temperature difference.
4.2.2 Impact on buckling shape
To analyze the regularity of impact of initial
imperfection on buckling shape, half of buckling shape
of pipelines with pipe-subsoil friction factor of 0.3 and
different initial imperfections of 100 mm, 200 mm,
300 mm, 500 mm under temperature difference of 25 °C
are analyzed. Figure 12 shows the analyzing results.
As to the impact of initial imperfection on buckling
Table 3 Buckling characteristics of pipeline under same temperature difference
Triggering temperature difference/°C Length/m Amplitude/m Bending plus axial stress/MPaFriction
coefficient Mode I Mode II Mode I Mode II Mode I Mode II Mode I Mode II
0.1 12.56 11.59 192 137 11.69 6.90 263.07 198.46
0.2 17.63 16.73 140 99 11.09 3.79 265.00 195.33
0.3 20.89 20.75 114 81 4.32 2.54 254.75 185.67
0.5 27.84 27.22 85 60 2.25 1.26 220.60 152.14
Fig. 11 Comparison of temperature difference: (a) Mode I; (b) Mode II
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Fig. 12 Horizontal distance from midpoint of pipeline:
(a) Mode I; (b) Mode II
shape, with the increase of initial imperfection amplitude
under the same temperature difference, there are
increases in buckling amplitudes, however, it is not large
at all. And the higher the temperature difference is, the
smaller the difference of global buckling amplitude will
be.
4.2.3 Impact on maximum compressive stress
To analyze the regularity of impact of initial
imperfection on the maximum compressive stress in the
pipe wall, the maximum compressive stresses with the pipe-subsoil friction factor of 0.3, the different initial
imperfections of 100 mm, 200 mm, 300 mm and 500 mm
and the temperature difference of 30 °C are shown in
Fig. 13.
Fig. 13 Comparison of maximum compressive stress
It can be seen from Fig. 13 that, the larger the initial
imperfection amplitude is, the lower the maximum
compressive stress is. This means that the pipeline with
larger initial imperfection amplitude is safer than the
pipeline with smaller one.
All the above analysis results are tabulated in Table
4.
4.3 Comprehension influence analysis
The combined effects of vom and the pipe-subsoil
friction coefficient on thermal buckling for an unburied
pipeline are shown in Fig. 14. It presents comparison
results among the pipelines with different imperfection
amplitudes and different pipe-subsoil friction coefficients
for Mode I and Mode II.
Figure 14 shows that the curves of pipeline with the
same pipe-subsoil friction coefficient will reach a same
certain point, that is to say, pipelines with the same
friction coefficient and different initial imperfections will
have the same buckling amplitude while the temperature
difference exceeds a certain value. It can also be seen
that the larger the friction coefficient is, the higher the
merging point is, which means that the larger the friction
Table 4 Buckling characteristics of pipeline corresponding to different initial imperfections
Buckling characteristics under temperature difference of 30 °CTriggering temperature
difference/°C Length/m Amplitude/m Bending plus axial stress/MPaCondition of pipeline
Mode I Mode II Mode I Mode II Mode I Mode II Mode I Mode II
Ideal pipeline 22.55 21.71 113 81 4.20 2.49 389.84 325.08
100 mm 21.25 20.66 113 81 4.22 2.52 287.70 224.50
200 mm 20.01 19.12 114 81 4.26 2.56 268.52 201.99
300 mm 20.89 20.75 114 82 4.32 2.61 254.75 187.77
Pipelinewith initial
imperfection
500 mm 19.10 18.26 115 82 4.43 2.72 233.29 166.41
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Fig. 14 Comparison of buckling curves: (a) Mode I; (b) ModeII
coefficient is, the higher the triggering temperature
difference is.
5 Conclusions
1) For two global buckling modes, with the increase
of the temperature difference, both the buckling
amplitude and length increase. However, this kind of
increase is not uniform: buckling amplitude and length
increase slowly when the temperature difference is less
than a certain value. Once the temperature difference
exceeds this value, there will be a series of intense
increase in the buckling amplitude and length. This
value of temperature difference is defined as the
triggering temperature difference. The triggering
temperature difference of Mode I is higher than that of
Mode II, which indicates the lateral buckling is easier to
occur for Mode II than Mode I. The bending plus axial
stress will increase with the increase of temperature
difference, and bending plus axial stress of Mode I is
much higher than that of Mode II under the designtemperature difference, which indicates that Mode I is
more dangerous compared with Mode II once it occurs.
2) As to the impact of the pipe-subsoil friction
coefficient on pipeline global buckling, the larger the
friction coefficient is, the smaller the buckling amplitude
and buckling length of the pipeline for both global
buckling modes are. The triggering temperature
difference increases and the bending plus axial stress in
the pipe wall decreases with the friction between the
pipeline and subsoil increasing. This means that a
pipeline with larger pipe-subsoil friction coefficient is
safer than that with small one.
3) As to analysis on impact of initial imperfection
on pipeline global buckling, the snap buckling is
predominantly governed by the amplitude value of initial
imperfection. The snap buckling phenomenon only exists
on pipeline with small initial imperfection. For the same
temperature difference, the global buckling amplitude
increases with the initial imperfection amplitude of the
pipeline. However, this kind of increase will beeliminated with the temperature difference rising.
Meanwhile, the larger the initial imperfection amplitude
is, the smaller the bending plus axial stress is, which
indicates that actively creating larger initial
imperfections can effectively prevent submarine
pipelines from global buckling failure.
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(Edited by YANG Bing)