THE DANISH CENTER FOR .- APPLIED MATHEMATICS AND …
Transcript of THE DANISH CENTER FOR .- APPLIED MATHEMATICS AND …
THE DANISH CENTER FORAPPLIED MATHEMATICS AND MECHANICS
Søren Christiansen
Frank A. Engelund
Svend Gravesen
Erik Hansen
¡var G. Jonsson
P. Scheel Larsen
Hugo Møltmann
Frithiol L Niordson
Pauli Pedersen
Kristian Refslund
Scientific Council
Laboratory of Applied Mathematical Physics
Institute of Hydrodynamics and Hydraulic Engineering
Structural Research Laboratory
Laboratory of Applied Mathematical Physics
Institute of Hydrodynamics and Hydraulic Engineering
Department of Fluid Mechanics
Structural Research Laboratory
Department of Solid Mechanics
Department of Solid Mechanics
Department of Fluid Mechanics
Secretary
Frithiof I. Niordson, Professor, Ph. D.
Department of Solid Mechanics, Building 404
Technical University of Denmark
2800 Lyngby, Denmark
TC*CHE Uft' '
boratorluSc .- ..'
Archiefe 2, 2628 ' DG!ft
O1 .y35
EQUILIBRIUM OF OFFSHORE CABLES
AND PIPELINES DURING LAYING
by
P. Terndrup Pedersen
DEPART ME NT
OF
OCEAN ENGINEERING
THETECHNICAL UNIVERSITY OFDENP.IARK
A
Cn
Ct
D
EI
F fn' n
f,,g.J)H
Hb.hbH1 ,h.
M
N,n
px r
T
Tb
V
Vb, Vb
V V.i' i
Wb
wt
NOMENCLATURE
Distance between barge deck and water surface
Normal drag coefficient
Tangential drag coefficient
Outer diameter of pipe or cable
Bending stiffness of pipe
Normal drag force per unit length
Tangential drag force per unit length
Auxiliary functions
Water depth
Horizontal force component at the ocean floor
Horizontal force component at upper end ofsuspended length
Suspended length
Bending moment
Axial tension
Components of load per unit length
Arc length
Shear force
Horizontal anchor force
Current velocity
Vertical force component at ocean floor
Vertical force component at upper end ofsuspended length
Buoyancy per unit length
Weight per unit length
X,Y,x,y Rectangular coordinates3 Tangent angle
Mass density of water
EQUILIBRIUM OF OFFSHORE CABLES AND PIPELINES DURING LAYING
P. Terndrup Pedersen
Department of Ocean Engineering
The Technical University of Denmark, Lyngby, Denmark
ABSTRACT - An efficient solutin technique for determination of the staticequilibrium form of a cable or a pipeline suspended between the ocean floorand a laying barge or a stinger is presented. Variations in bending stiff-ness, weight and buoyancy and forces due to ocean current are taken intoaccount. The governing non-linear boundary value problem is transformedinto a non-dimensional form such that the a priori unknown suspended lengthof the pipeline or cable acts as a scaling parameter. The numerical solu-tion is then based on successive integrations. The ajìication of themethod is illustrated by the analysis of equilibrium curves and stressesin pieeiines laid with or without the use of stingers and during abandonand recovery operations. -
1. INTRODUCTION
The object of this paper is to present a technique that
will provide an efficient and direct solution to the static
equilibrium form of a cable or a pipeline suspended between
the ocean floor and a laying barge in a steady ocean current.
With increasing water depth the length of the suspended
pipeline between the pipe laying barge or the lift-off point
from the stinger and the ocean floor becomes greater. This may
cause the stresses in the pipe to become so high that the pipe
buckles or the stresses in the stinger to reach a level where
the stinger breaks. In calm seas these considerations establish
the limits for water depths in which pipes can be layed.
The problem of predicting the suspended geometry and there-
by the stresses of marine pipelines during laying in the ocean
is one of large deflection beam theory, where the length of the
suspended beam is nota priori known. There has been some pre-
vious work dealing with the numerical solution of this problem.
2
Stiffened catenary solutions have been developed [i), [2)
for laying of pipes with relatively small bending stiffness in
extremely deep water. The stiffened catenary solution is ob-
tainod by applying the method of matched asymptotic expansions
irto is based on the assumption that the pipeline takes a shape
which approximates a natural catenary over most of its length
,nd that the influence of the boundary conditions is confined
to small "boundary layers" near the pipe-laying barge and the
ocean floor. Unfortunately, the method is difficult to apply
when the pipe is laid with the use of a stinger, but in those
cases where all the basic assumptions of the theory are satis-
fied the method is attractive because of relatively small
demands onl calculations.
For the analysis of pipes laid in shallower water or of
pipes with larger bending stiffness much more involved finite
element methods [3), finite difference methods [41 - [51, and
methods involving transformation of the non-linear,two-point
boundary value problem into initial-value problems have been
proposed. Common to these methods is that they are based on
successive iterations and that each main iteration step in-
volves a second set of successive iterations for the calcula-
tion of the suspended length, thereby making these methods
relatively expensive as regards computer size and time.
Furthermore, these methods are usually not flexible enough
to handle all the existing types of pipe-laying procedures
without non-trivial modifications.
In this paper a method is presented which provides a
relatively direct solution to cable and pipe-laying problems.
The governing non-linear, two-point boundary value problem is
derived and transformed into a non-dimensional form such that
the a priori unknown suspended length of the pipeline or cableacts as a scaling parameter. The method of solution is then basedon successive integrations. The requirements to computer storage
and time are thereby limited to the same order of magnitude as forthe stiffened catenary calculations. In order to demonstrate
the flexibility of the method, examples are given on the ana-
lysis of the pipe-laying operations, where the pipe is laid
without the use of a stinger or with an articulated stinger,
and with the use of a rigid stinger. Finally pipe abandon!
recovery operations are treated. In the last section of the
paper we demonstrate how cable-laying problems and one-leg
mooring problems can be analysed by the proposed method.
2. LOADING ON THE SUSPENDED PIPE.
We consider a deformed inextensible pipe as shown in
Fig. 2.1. As independent variable in our formulatiqn we
shall employ the arc length s from the point where the
pipe touches the ocean floor. This point will also serve
as origin for the rectangular coordinate system X-Y shown
in Fig. 2.1. The tangent angle to the pipe is denoted O(s).
and we designate the depth of the ocean by H.
1he load on an element of unit length of the suspended
pipe is composed of: the weight wt(s), the buoyancy w0(s)
and,due to a steady ocean current with velocity V(Y) , also
a normal drag force Fe(s) and a tangential drag force Fe(s)
The mass density of the water is given by'
the
gravity by g, and the cross sectional area of the pipe by A.
Y
Fig. 2.1 Loading on the pipe.
The buoyancy load on the pipe due to the water pressure
is determined as follows. Corlsider the segment of length ds
shown in Fig. 2.2. The total buoyancy of the segment with
7open ends equals JgAds
and acts in the Y-direction.
This load has to be corrected
for the lack of pressure at
the ends of the segment. From
Fig. 2.2 it follows that the
resulting buoyancy load w0ds
acts in the direction normal
to the centreline of the pipe
segment and with a magnitude
given byFig. 2.2 Buoyancy on pipe element.
dOW0 = WiCOSO + (H-YY--j
The loading due to the current takes the form
F = p CV2A2v c
where C is the drag coefficient, V the flow velocity, and
Ac a characteristic area. The axial and tangential load per
Unit length can be obtained from (2.2) as
F = pCVVIDsin2O
Ft = 1TJ C VIVIDcOS2OVt
(2.1)
= FcosO - (wü_Fn)sinO(2.4)
p(s) = FsinO + (w0_Fn)coSO -
respectively.
3. GOVERNING EQUATIONS FOR PIPES
In this section we shall set up the governing equations
for the plane, one-dimensional, finite-strain beam theory
which will be used to model the pipe.
As constitutive law for the pipe we will assume a linear
relation between the bending moment M and the curvature
dO/ds. Thus
where EI is the bending stiffness of the pipe.
The moment equilibrium condition for segments of the pipe
(2.2) gives the shear force T(s) as
dOdM-T(s) = ã ds
The shear force T at any section of the pipe can be found
from Fig. 2.1 by equilibrium considerations. We find
d dO(2.3) T(s) - (EI) = _HbsinO(s) + vbcosO(s)
(3.2)
45
where Wb = PgA for O < Y < H and Wb = O for Y > H.M(s) = EIP (3.1)
where D is the diameter of the pipe, and C, C are drag
- Cos8(S)J(5l)dsi + sine(s)J(si)dsi (3.3)
coefficients.where
11.0,V, are the horizontal and vertical force components,
Thus, the resulting horizontal and vertical load inten- respectively, at the support point at the ocean floor. Simi-
sities for the submerged part of the pipe are larly, we find the axial force N(s) at any section of the
6
form
+ coso(s)J P(S1)dS1 - sinO(s)1 p (s )dslxiO JO
and
N(s) = Hbcose(s) + vbsinO(s)
whe re
= Ftcoso(s) + F sinO(s)
7
- siñO(s)J(si)dsi COSO(5)jx(Si)dS1
p(s) = Fsin0(s) - F cosO(s) - (WL_wb)
11b + HwbcosOb Vb + HwbsinOb
and N = N + {H_Y(s)}wb
Equation (3.5) shows that the effect of the buoyancy on the
equilibrium curve of the pipe can be accounted for by intro-
ducing the submerged weight of the pipe. However, it will beseen from Eq. (3.6) that taking care of the buoyancy simply by
introducing the submerged weight results in an apparent axialfor N which equals the real axial force N plus the hydro-static force wb(H_y) . Here, we may note that for the eva-
luation of the buckling strength of a pipe it is the real axialforce N that is of importance, whereas for the determination
of a reference stress for a solid cable or mooring line we will
(3.6)
-2 d deA -(y-) = hbsinø - VbCOSO +
+A{cosOJPdi - sinOJPdi}
and Eg. (3.6) takes the form
(3.7)
n() = hbcosO + vbsinO - A{sinOfPdi + coser d1} (3.8)
0 '0
Neglecting the axial extension of the pipe, the relation between
the dimensionless natural coordinates (O,E) and the dimension-
less rectangular coordinates (x,y) are
dy = sinOd and dx = cosOd (3.9)
The boundary conditions at the ocean floor are
y(0) = x(0) = O (3.10)
O(0) = (3.11)
(de\(3. 12)
The boundary conditions at the upper end of the suspended pipe
depend on the method of operation (for example the type of
stinger used) . But we note, for future use, that the dimen-
= s/L {x, y) = {X, Y)/L A = L/B
The equations (3.3) and (3.4) can also be written in theEIY = ---- x' Pyf =
d dO - wtH= HbsinO(s) - VbcosO(s) and
(s Ishb Vb, n,t} = (Hb, Vb, j:, T}/(wH)
(3.5)
0.where w is a characteristic value of the weight per unit
length w of the pipe. Then Eg. (3.5) takes the form
be concerned with the adjusted axial force which here issuspended pipe as
denoted N
N(s) = HbcosO(s) + VbsinO(s) In order to isolate the unknown suspended length L of
the pipe let us then introduce the following dimensionless
_sinOsJys1dsl - cOsOsJxsidsi (3.4)quantities:
o
and that the vertical component of the tension is given by
i
vi v - A
The non-linear boundary value problem will be solved nu-
meri.cally by successive iterations. The physical background of
of the numerical method is as follows: first the loading on
the pipe (p,p) associated with an arbitrary deflection curve
and is determined; based on this loading a new
deflection curve is found (8. ,x. ,y , and À. } which is3+1 j+1 j+l j+1
then used In the next iteration step for the calculation of
the loading on the pipe. This continues until a certain re-
quired degree of equilibrium is obtained. Mathematically,
the method Is based on a series of formal integrations of
the thfferential equations, together with a determination
of the dimensionless suspended length A , which acts as ascaling parameter.
In all the examples presented in the following the
iteration procedure is stopped when the following inequa-
lity is fulfilled
(1
{(x -x)2
+ (Y31-Y)21d12
jj+i i
O
(3.14) where t is a small number (lOs).
(4.1)
o
Consequently,tiere the non-dimensional forces h.,v. are related to theto the equilibriumapp)ied forces H.,V. bygration we can
h1 = (H1 + (H-Yj)wbcosOj}/(wH) whereand
f1(.1) =
y. = (V. + (H-Yjw sinO.}/(wH) ini i i b i
The differential equations (3.7) and (3.9) and the bound- f3R)
let us assume that
curve (8..x..Y}.
determine the functions
Ir,
; f.(F,) = I
I y 1 I
- pd1 i fU) =
we have an approximation
Then by numerical inte-
f.(); i = i .....6,
X
Y 1
8
9
sionless applied horizontal tension can be found from the
following equilibrium equation
h. = hb - pxl (3.13)
ary conditions of the problem constitute the non-linear bound- O O
(4.2)ary value problem to be solved.
f5() = (f3sinø. + f4cosO.}d1
4. METHOD OF SOLUTION FOR PIPE-LAYING PROBLEMS, and
f6;) =
f5
O
Following the outlined method of solution we get from
Eq. (3.7) ,wlth the notation (4.2)
dO-2 dA.1 -(ï
d) - hbslnO. - vbcosO.
(4.3)+ A
. (f sinO f cosO3 j 4 j
and from Eq. (3.8) we get
n1(E) = hbcosO. + vbsin8.
(4.4)+ À 1{f3cosß. - f4sin81)
10
Fin1ly,the equations (3.13) and (3.14) result in
h1 = hb + À.1f3(l)
y. = y - A. f (1)i b j+l 4
respectively.
A first step in the determination of the new approximation
to the equilibrium curve is a formal integration of Eq. (4.3),
which yields
do,A21(y lf1) - h y - y x + A f + C
b j b j+1 S
The static boundary condition (3.12) expressing the fact
that the bending moment is zero for = O imposes the value
zero for the integration constant C. Now the tangent angle
can be obtained from (4.7) by a second formal integra-
tien resulting in
+ A2 0bA2 0. (1) hbfl - vbf2 + A.1 f6 j+l1+1 3+1
when the kinematic boundary condition (3.11) is introduced.
In order to proceed we have to introduce the boun-
dary conditions at the upper end of the suspended pipe. We
shall here consider three important cases.
a. Pipe-laying without stinger or with an articulated stinger.
Fig. 4.1 Pipe-laying without stinger.
First we shall consider a case where the pipe is layed
without the use of a stinger. We shall assume that at the
upper end of the suspended pipe we have the kinematic bound-(4.5) ary conditions
(4.6)
(4.7)
where(4.8)
f2)g () = O + (0.-0i b i b f2(l)
f(ì)= hi(f1() - f2(1) f2()}
jo
The as yet unk'own suspended length A1 of the pipe
can now be determine. by solving the transcendental equation
obtained from the bourìary condition (4.10) and Eq. (4.15)
0(L) = 0.1
Y(L) = H + A
where A is the distance between the pipe support ori the
barge and the ocean surface. We shall also assume that the
applied horizontal tension H. at the support is known.
Introducing the kinematic boundary condition (4.9) in
(4.8) gives
= 1(0 -0.)AT2 + hbfl(l) + f6(1)A1)/f2(1)b i. j+1
Introducing (4.11) and (4.5) In (4.8) yields
2 3= g1() + A.1 g2() + A1 g3()
g3(E) =f6(F) +(f3(l)f1(1) f6(1)}f(1) f3(i)f1U)
li
(4.11)
(4.12)
(4. 13)
From (3.9) and (3.10) we get
X.j+1 = jo cosO d1i+1
(4.14)
= sinO (4.15)
(4.9)
(4.10)
12
1
sin(g + A2 g + A3 g3dE1 = 1 + ai j+l 2 j+i,o
where a = A/H.
Thus, starting with an arbitrary integrable approximation
to the equilibrium curve the functions g1, g2, and g3 can
be determined from (4.13) and a new approximation to the sus-pended length of the pipe can be found from (4.16). The
improved approximation to the equilibrium functions are here-
after found from (4.12), (4.14), and (4.15).
The sequence of successive iterations may be started with
an arbitrary regular function satisfying the kinematic boundaryconditions. We can, for example, use the deflection curve
corresponding to a natural catenary or a solution of the
linearized Bernoulli-Euler beam equation that satisfies all
the boundary conditions at the ocean floor and the kinematic
boundary conditions at the upper end of the suspended pipe.
These methods of obtaining the first approximation also supplyus with a first estimate of the suspended length.
The effect of having part of the equilibrium curve abovethe surface of the ocean (A > O), or support buoys along thepipe, or, an articulated stinger, is easily taken care ofin the present formulation by introducing a variation in the
distributed buoyancy and/or weight of the pipe.
As an application of the foregoing, Fig. 4.2 shows the
results of the numerical analysis of a pipe-laying procedurewhere the pipe is laid without the use of a stinger. The waterdepth H is 50 m, the pipe leaves the pipe-laying barge 2 m
above the water surface at an angle equal to 200. The hori-zontal tension H. applied at the barge is 2.200l05N.The uniform bending stiffness EI of the pipe is 2.256'109Nm2,
the buoyancy per unit length in water Wb is l.6l4l04N/m and
the weight per unit length w is l.843l04N/m.
Starting with a deflection curve corresponding to the
solution of the linearized beam equation, where the effectof the applied horizontal tension h1 is neglected, the so-
lution presented in Fig. 4.2 is obtained in 3 iteratIon steps.
(4.16)
A.2so
Lt 2 fl$ t0 'b.'-, 'to' 41.
a t &t4 to' t41.
4, L200 tO'No
Fig. 4.2 Results of numerical analysis of pipe-laying procedurewithout the use of a stinger.
b. Pipe-laying using a rigid stinger.
We will now consider pipelaying with the use of a rigid
stinger with a fixed curvature i/R as shown in Fig. 4.3. Let us
Fig. 4.3 pipe-laying using a rigid stinger
13
assume that the applied horizontal tension is H. at the upper
end of the suspended pipe (the lift-off point from the stinger)
The tangent angle of the stinger at the point where the stinger
is hinged to the barge is denoted O. The angle e will nor-
mally be a non-linear func-
tion of the position of
the lift-off point given
by Y and and the
magnitude of the concen-
trated force T1 per-
pendicular to the stinger
axis at the lift-off point.
Due to the constant curva-
ture of the stinger the
force T1 equals the shear
force in the pipe Just be-
low the lift-off point.The function = 0(Y.,T.) can be determined when the geometry
and the weight distribution of the stinger are known. See Fig.4.4
Besides the static boundary condition expressing the fact
that the horizontal force is H at the lift-off point the bending
moment M1 is also given
= -EI/R (4.18)
Finally, kinematic considerations give us the relationship
I-1-Y1 +A
cosO. = cose -i u R
Let us now construct the iteration algorithm using these
boundary conditions. Applying the boundary condition (4.18) to
the equation (4.7) results in
Fig. 4.4 The stinger supported partof the pipe.
X- (1)
_____ - Ihb Vb y(l) r (l)A141
(l)
f5(l)
(4.19)
(4.20)
where r R/H. The equations (4.20) and (4.5) yield
y.(l) f5(l)f (1)) + )Vb x1(l) 1h1 + A11{(1)3 1+1 r y(l) (4.21)
substituting (4.21) and (4.5) into (4.8) gives
8. () = O + A. g () + 1g2() +b j+l iJ+i
whereY
=r x.(1)
-g () = h.(f () f2 i 1 x.(1)
and1f5(1) y.(l)
g3() =f6() -f3(l)f1() 2jx.(l) _f3(l)3(1)}J i
The unknown dimensionsless suspended length A141 is determined
from the following transcendental equation obtained from the
boundary condition (4.19) together with (4.15)
cose. (1) = cosO - À(l + a - À1y1(l)}3+1 u r
Thus, starting with an arbitrary integrable approximation
to the equilibrium curve one step in the iteration procedure
is to determine the functions g1, g2, and g3 from (4.23) and
from (4.24). The improved approximation to the equi-
librium functions are hereafter given by (4.22), (4.14) and
(4.15). The iteration scheme is stopped when the convergence
criterion (4.1) is fulfilled.
The method outlined is,of course,only valid when the
stinger is so long that the calculated lift-off point is on the
stinger. If this is not the case,a slightly different itera-
tion scheme is called for.
An example of the numerical analysis of a pipe-laying
procedure using a stinger with fixed curvature Is shown In
Fig. 4.5. The stinger radius is assumed to be 300 m and,
in this example, the stinger is assumed to be rigidly connected
to the pipe-laying barge. The water depth and the pipe data
are assumed to be the sanie as in the previous example.
(4.24)
[415
(4.22)
(4.23)
16
El 226 i0 N,..2
i soi io'
8 101o 10' 1W...
ii, 2.200 lO N
-I
Fig. 4.5 Results of numerical analysis of pipe-laying procedurewith the use of a rigid stinger.
c. Pipe abandon/recovery operations.
Pipe abandon and recovery operations may be modelled as
Fig- 4.6 pipe abandon/recoverY operation
shown in Fig. 4.6. These operations can be performed in a
number of different ways. As an example we will assume
that the wire passes over the stinger rollers and that the
horizontal anchor force transmitted to the pipe Tb andthe V-coordinate of the pipe end Vi are known, whereas
the wire tension T is considered as a dependent vari-able.
Taking into account tohe water pressure on the
lid which is normally welded onto the pipe end during
these operations,the boundary conditions for the upper end
of the pipe take the form
Y(L) = Y.i
M(L) = O
FI. = T - w (H-Y.)cosh(L)i b b i
Let us again construct one step in the iteration algo-
rithm using these boundary conditions. From F.gs. (4.5) and
(4.7) and the boundary conditions (4.25) - (4.26) we get
y,(l) f5(l)
i j+13)J +Vb {hk. f (1)x.(l) 3+1 X (1)
J j
Substituting into Eg. (4.8) results in
e. () ej+l = b 1g2() + À1g3()
where g2() and g3(r,) are given by (4.23). The dimen-
sionless suspended length is determined from theboundary conditions (4.25).
Fig. 4.7 shows the results of a numerical analysis of
a pipe abandon or recovery operation. The same pipe data as
in the two previous numerical examples have beell assumed.
The position of the upper end of the suspended length is
specified as 25 m above the ocean floor and the horizontal
anchor force as 105N. The necessary wire tension is found
(4.25)
(4.26)
(4.27)
17
100 200 i,. 300 X
(4 .28)
(4.29)
18
to be 2.148105N.
dN= wsinO - Ft
Fig. 4.7 ResultS of numerical analysis of abandon/recovery operation
Cables are characterized by a negligible bending stiff-
ness (EI O) . The iteration method presented in section 4
for determination of equilibrium curves for pipes fails if
we let the bending stiffness approach zero. Therefore, in
this section we shall present a similar iteration method for
the analysis of equilibrium curves and elastic restoring forces
of cables as that used, for example, for mooring systems, taking
into account drag forces on the cable and variations in cable
weight per unit length.
and that equilibrium in the direction normal to the neutral
axis of the cable is obtained when
F + (w_wb)cosO - wb(H_Y)ds n
Introducing the adjusted normal force
= N + wb(H'SY)
the governing equations (5.j), (5.2) take the simpler form
AdN
(wt_wb) sinO * Ft
=j"ds
ç
(wt_wb)cosø + F)
The boundary conditions for these equations express the
fact that, at the upper end of the Suspended cable,
Y(L) H+A5. STATIC EQUILIBRIUM OF CABLES.
and = H./cosO(L)
where H. is the applied tension, while at the ocean floorwe have
X(0) O and Y(0) = O (5.6a-b)
If we consider a problem where part of the cable is lying
on the ocean floor we have the additional boundary condition
e(o) - (5.7)
In non-dimensional forni,the governing equations (5.3) -
(5.4) take the form
(5.1) pt() = {(wt_wb)sino -AO
and n(F;) = N/wtH
(5.2)
(5.3)
(5.4)
(5. Sa-b)
19
Governing equations.dn Ap() dO A
(5 .8a-b)
It follows from Fig. 2.1 that force equilibrium in the wheretangential direction for an element of the cable is expressed
= f (w-w)cos8 +by
V
El 223S *0PI.I I3 Io' *4 Witt I.V.n
05I SII. IO' *V4.. o u. I0'N
*4 . I0N05..
.o-
- 20
Numerical solution.
An iteration procedure similar to that outlined in
section 4 will now be applied for the numerical solution of
the non-linear boundary value problem given by (5.5) - (5.8).
Assume that an initial approximation to equilibrium curve
is given so that the iteration algorithm can be
started by a formal integration of Eq. (5.8e)
nU) = 1j+l ptdl + C1Jo
It follows from the boundary condition (5.5b) that the inte-
gration constant is determined by
ih.
J- -ÀC1= cosO j+l' ti
i JO
Formal integration of Eg. (5.8b) results in
= À11[ d+n 1
o
Long Cables. If we are dealing with a mooring cable problem
where the length of the cable is so large that part of the
cable lies on the ocean floor,then the integration constant
in (5.10) is given by the inclination of the ocean floor. Fig.5.l.
Fig. 5.1 Mooring-cable geometry, long cable.
(5.9)
(5. 10)
Using the boundary conditions (5.5a) and (5.6b) it is seen that
in this case the unknown,unsupported length of the cable can be
determined from the transcendental equation
IlA sinO d1 = i + aj+l j+l
Thus, the static equilibrium of the cable can be determined
by successive iterations, where each iteration step involves the
calculation of n and A41 using Eqs. (5.9) - (5.11).
The sequence of iterations can be stopped when the convergencecriterion (4.1) is fulfilled.
Shorter Cables. When dealing with a mooring system where thecable is of shorter length so that the point of initial contactis the anchor point, the inclination of the cable at the anchorpoint
0b is usually unknown. However, in this case we will as-sume that the length L of the cable is known. This leaves us
with sufficient information to construct one step in theiteration procedure. See Fig. 5.2.
(5.11)
21
X7,
FIg. 5.2 Mooring-cable geometry, Short cable.
22
Dropping the subscripts on the known dimensionless length A
Eq. (5.10) can be written as
e. () = n. () + Oj+1 +i b
where
n () = A'j+1J0
n
From (5.13) the unknown angle 8b can be determined as
8 = Arcsin( l+a
)Arctan
A/C+C ()h
Thus, in order to determine the static equilibrium positionof a short mooring cable,each iteration step must consist of acalculation of n (5.9) and 8.4k (5.10), where the angle
is determined from (5.14).
(5.12)
(5.14)
6. CONCLUSION
The method of successive integrations presented for the
determination of equilibrium forms and stresses for submarine
pipelines during laying possesses several advantages over
other available methods. The principal advantage is the ex-
tremely modest requirements to computer storage and computer
time. Since, in principle, the method only involves integration
of known functions,the me'thod is well suited for programming
on shipboard computers for control of the actual pipe-laying
procedure. The numerical calculations for the three pipe-
laying examples presented in this paper were done as one job
on an IHM 370/165 computer. The total computer time is 0.88
sec. and the storage requirement,including object code and
array area for this general program,is 32 K8. Another ad-
vantage of the method is its flexibility. For example the
effect of variations of pipeline bending stiffness due to
variations in the coating, current variations with depth,
and auxiliary support buoys can easily be accounted for.
The primary limitation of the present method for the
analysis of equilibrium forms of pipes is failure to converge
for some extreme input values such as very deep water or small
bending stiffness. However, since the present method and the
stiffened catenary method has a common convergence region it
is possible to shift to stiffened catenary solutions if the
pipe data are such that the method of successive integrations
fails to converge. If it is necessary to take ocean current
and variations in pipe data into account the stiffened cate-
nary solution can be based on the numerical method presented
for the analysis of cables.
23
Introducing
in
where
C1 =
(5.12) into the boundary condition
CicosOb + C2slflOb =
Ilsinn. dF1 and C2
I 3+1
(5.4a)
Ilcosri
i j+1û
results
(5. 13)
24
REF ERENC ES
il) PLUNKETT, R.: Static bending stresses in catenaries
and drill strings, Trans. ASME, Journal of Engineering
for Industry, Vol. 89, No. 1, pp 31-36, 1967
(2) DIXON, D.A. and RUTLEDGE, D.R.: Stiffened catenary cal-
culations In pipeline laying problems, Trans. ASME,
Journal of Engineering for Industry, Vol. 90, No. 1,
pp 153-160, 1968
[3] POWERS, J.T. and FINN. L.D.: Stress analysis of off-
shore pipelines during installation, Offshore Technology
Conference, Houston, Texas, Paper No. OTC 1071, May, 1969
[4) PALMER, A.C., HUTCHINSON, G. and ELL.S, J.W.: Configuration
of submarine pipelines during laying operations, ASME,
Paper No. 73-WA/OCT-4, 1973
[5] DAREING, D.W., NEATHERY, R.F.: Marine pipeline analysis
based on Newtons's method with an arctic application,
Trans. ASME, Journal of Engineering for Industry, Vol. 92,
No. 4, pp 827-833, 1970
LATEST DCAÌ4 REPORTS
HINWOOD, J.B. & RASMUSSEN, H.: On the Derivation of Models forFlow in Estuaries (February 1973)
NEMAT-NASSER, S. & FU, F.C.L.: Improvable Lower and Upper Boundsfor Frequencies of Harmonic Waves in Elastic Composites(April 1973)
ENGELUND, F.: The Dynamics of Warm Surface Currents (April 1973)
1414. CHRISTOFFERSEN, JEE: On Zubov's Principle of StationaryComplementary Ener and a Related Principle (April 1973)
GERMAIN, P.: The Method of Virtual Power in Continuum Mechanics(E403 1973)
CHRISTOFFERSEN, JEG: A Simple Flow Theory of Elastic-PlasticDeformation Applicable to Materials with a Singular Yield Surface(May 1973)
MØRCH, K.A.: On the Impingement of a Composite Jet (May 1973)
DE4UTR, LARS: Free Temporal and Spatial Longitudinal Modes inRadiating Elastic Cylindrical Rods (May 1973)
JENSEN, FINN BRUUN: Response of an Air Bubble in Water to aShock Wave (June 1973)
NF34AT-NASSER, S.: On Nonlinear Thermoelasticity and NonequilibriumThermodynamics (June 1973)
COLLATZ, L.: Chained Approximation with Application to Differential-and Integral Equations (August 1973)
BORGNAKJCE, C. & SCHEEL LARSEN, P. : Statistical Collision Model forMonte Carlo Simulation of Polyatomic Gas (August 1973)
RASMUSSEN, H. & CHRISTIANSEN, S.: Numerical Solutions for Tvo-Dimensionai Annular Electrochernical Machining Problems (August 1973)
514. KARIHALOO, BL. & NIORDSON, F.I.: Optimum Design of a Circular Shaftin Forward Precession (August 1973)
TVERGAARD, VIGGO: On the Optimum Shape of a Fillet in a Flat Barwith Restrictions (September 1973)
OLHOFF, NIELE: On Singularities, Local Optima and Formation ofStiffeners in Optimal Design of Plates (September 1973)
GROSS-PEGENSEN, .JBGEN: A Compenbation Method in Scattered LightPhotQelasticity (September 1973)
CHRISTOFFEPSEN, JES: A Note on Necking of Cylindrical Bars(Oktober 1973)
JENSEN, JØRGEÍJ JUNCHIIR: Zero-Moment Ellipsoidal Domes (November 1973)
TALHEJA, RMSH: Cycle-Dependent Creep under Random Loading(November 1973)
Li. CHRISTOFFERSEN, JES: Elastic and Elastic-Plastic Composites. A newApproach (November 1973)SKOVGAARD, OVE: Selected Numerical Approximation Methods(December 1973)
NEEDLEMAN, A. : Postbifurcation Behavior and Imperfection Sensitivityof Elastic-Plastic Circular Plates (February 19714)
6l. NEEDLEMAN, A. A.xisynuiietric Buckling of Elastic-Plastic Annular Plates(February 19714)
.. EBENE, STEEN: On the Integration of Singular Integral Equations(two papers) (March 19714)FEDERSEN, PAULI & MAGAHF.D, M.M.: A.xisyiiimetric Element Analysis UsingAnalytical Computing (March 19714)EBENE, STEEN: The Stress Distribution in an Infinite AnisotropicPlate with Co-Linear Cracks (May 19714)PEDEFISEN, P. TEFINDRUP: On the Collapse Load of Cylindrical Shells(June 19714)TVEFGAARD, V. & NEEDLEMAN, A.: Mode Interaction in an EccentricallyStiffened Elastic-Plastic Panel under Compression (June l971i)
BRSTBUP, MW.: Plastic Analysis of Shear in Reinforced Concrete(July 19714)
il. TVERGAARD, V. & NEEDLEMAN, A. : Buckling of Eccentrically StiffenedElastic-plastic Panels on two Simple Supports or Multiply Supported(August 19714)CIIRISTIAI1SEN, S.: On Kupradze's Punctional Equations for Plane HarmonicProblems (September 19714)CHBISTOFFEHSEN, JES: Small Scale Plastic Flow Associated With Rolling(September 19714)
7i. PEDERSEN, FLENMING BO: Interfacial Mixing in Two Layer Stratified Flow(October 19714)
TVEBGAARD, V. & NEEDLEÌ4AN, A.: On the Buckling of Elastic-PlasticColumns with Asymmetric Cross-Sections (November 19714)
HANSEN, JOHN: Influence of General Imperfections in Mcially LoadedCylindrical Shells (November 19714)KARIHALOO, B.L.: Dislocation Mobility and a Concept of Flow Stress(November 19714)
7h. KABIHALOO, B.L.: Range of Applicability of Barenblatt-Dugdale- BCS Model(January 1975)EPJIIHALOO, B.L.: Mobility of Super-lattice and Partial Dislocations inan Internally Stressed Solid (February 1975)PEDERSEN, P. TEIINDRUP: Equilibrium of Offshare Calles and PipelinesDuring Laying (February 1975).
The DCAMM reports are issued for early dissemination of research results fromthe Laboratory of Applied Mathematical Physics, Department of Fluid Mechanics,Institute 0f Hydrodynamics and Hydisulic Engineering, Department of SolidMechanics and Structural Research Laboratory at the Technical University ofDenmark.
These technical reports are as a rule submitted to international scientific journalsand should not be widely distributed until after the date of publication. When-ever possible reference should be given to the final publications and not to theDCAMM reports.
This report or any part thereof may not be reproduced without written permissionof The Danish Center for Applied Mathematics and Mechanics.