review of numerical approach used in the …assisted mooring system [9]. moored system where...
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International Journal of Engineering Technology and Scientific Innovation
ISSN: 2456-1851
Volume:03, Issue:05 "September-October 2018"
www.ijetsi.org Copyright © IJETSI 2018, All rights reserved Page 201
REVIEW OF NUMERICAL APPROACH USED IN THE OPTIMIZATION
OF MOORING SYSTEMS FOR FLOATING STRUCTURES.
Ben Uwihanganyea, Christiaan A. Adenyab, Hiram M. Ndirituc
aDepartment of Mechanical Engineering, Jomo Kenyatta University of Agriculture
and Technology, Main campus Juja, Kenya
bDepartment of Marine Engineering, Jomo Kenyatta University of Agriculture
and Technology, Main campus Juja, Kenya
cDepartment of Mechanical Engineering, Jomo Kenyatta University of Agriculture
and Technology, Main campus Juja, Kenya
ABSTRACT
This paper present a review on the technologies that are used in station-keeping of floating
platforms, the numerical methods used to model the mooring system dynamics with
environmental load of wind, current and wave force interaction. Furthermore the design and
optimization of the mooring system is reviewed. The lumped mass model found to be preferred
in commercial application over finite element and finite difference based on its simplicity and
ability to capture the same physics as of high order model. It was reviewed that Finite difference
would be better if its present nuances and numerical limitation are eliminated. It is notable that
the mooring line damping contribute about eighty percent of the total moored system damping,
hence its accurate prediction is critical during the design. The mooring line damping depends on
the drag force, therefore poor selection of the drag coefficient will lead to wrong prediction of
the amplitude of oscillation of the floater. During optimization of mooring system, it is seen that
the use of genetic algorithms have become popular. They account for environmental load
distribution, anchor holding capacity and mooring line properties such as materiel length and
tension. Some gaps are presented at the end of this review paper including unclear relationship
between mooring line damping and total tension and the surface roughness effect on drag
coefficient of mooring line.
Keywords: Mooring line, damping, drag coefficient and floater.
International Journal of Engineering Technology and Scientific Innovation
ISSN: 2456-1851
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1. INTRODUCTION
The exploration of petroleum and gas in sea
or lake waters is going deeper to more than
2500m of depth [1]. In addition floating
wind turbine and wave energy converters
have shown to be among the potential
sources of renewable energy. This has
compelled many researchers to find an
optimum design, not only in terms of cost
but also safety of station-keeping of any
floating structure within water bodies.
Floating structures within water bodies
experience linear and rotational motions due
to environment loads such as wind, current
and waves. Station-keeping systems have to
respond effectively to these motions. As
shown in Figure 1, linear motions include
heave, sway and surge while rotational
motions include pitch, roll and yaw. Heave
motion is in vertical direction moving
upward or downward while yaw is the
turning rotation of a vessel about the same
vertical axis. The heave response should be
controlled and minimized for effective and
efficient working of floating offshore
platforms because this motion is primarily
responsible for causing damage to the risers
and mooring systems due to excessive
vertical motion of the vessel [2]. Surge is the
linear oscillation along x-axis while roll is
the rotation of a vessel about the same
longitudinal axis caused by maritime
conditions. In 1990, the mooring lines of a
semi-submersible located in North Sea were
damaged due to a severe storm [3]. Deng [4]
studied the wave group characteristics
effects on a semi-submersible in freak waves
and showed that the surge response greatly
increases due to the freak wave and the large
amplitude surge responses due to transient
freak waves. These displacements are
closely related to the maximum tension
forces of mooring lines. Therefore, the surge
motion response of a semi-submersible is a
key issue especially in the extreme sea state.
Sway motion moves laterally and is
generated directly either by the water and
wind currents exerting forces against the
vessel while pitch is the up or down rotation
of a vessel about the same lateral axis. In
numerical study of hydrodynamic response
of mooring lines for large floating structure
in South China Sea by Yipeng Pana in 2015
[5] showed that surge and sway become
larger in moored station keeping system
with longer mooring lines.
The floating vessel motions are also
classified as low frequency (LF) and wave
frequency motions (WF). The WF motions
is the vessel response to first order wave
loads while the LF is slow drift motion due
to second order waves, wind, or driven
motion due to vessel thrusters [6]. The
presence of both WF and LF in the same
direction is called superimposed wave
frequency.
International Journal of Engineering Technology and Scientific Innovation
ISSN: 2456-1851
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Figure 1: Linear & rotational motions of
the vessel
In any marine operations, an important
aspect is to ensure a precise position and
motion control of a floating structure. This is
desirable to maintain integrity of system
elements and to maintain safe distance to
other structures within the waters. The
station-keeping system is one of the major
components of a floating offshore unit. This
technology was invented due to the need of
offshore extraction of oil and gas from the
deep seas or lake waters, and then expanded
to renewable energy sector due to offshore
wind turbine and wave energy converters.
The design of station keeping for any
floating system must reflect the
environmental condition [7].
Different types of station keeping principles
are used in order to withstand the
environmental forces on the floating
structure arising from wind, waves and
current [8]. For a semi-submersible unit, the
station-keeping system can be a mooring
system only, a dynamic positioning (DP)
with thrusters and or a dynamic Positioning
assisted mooring system [9]. Moored system
where positioning uses the mooring lines,
thruster-assisted mooring system where
positioning uses both mooring lines,
thrusters and propellers and thruster assisted
mooring have been used in the design of
station-keeping systems for floating
production storage and offloading (FPSOs).
The thrusters are used for heading control
and for reducing the mooring load. One of
the principal reasons for using thruster
assisted mooring is that it can reduce overall
project costs by reducing the mooring
system in terms of either fewer mooring
lines or a lighter overall system, especially
for deep waters projects [10].
For the dynamic positioning system,
position is achieved by use of thrusters and
propellers. A propulsion system applied for
dynamic positioning of vessels must be able
to generate counter forces against
environmental forces such as wind, current,
and waves, as well as damping forces
resulting from the drag of a deployed array
of pipes and risers during station keeping
operations. Environmental forces are omni-
directional, therefore, propulsion systems or
devices must have the ability to generate
thrust in the full 360 degrees. In order to
move the vessel from location to location,
the propulsion system installed on DP
vessels needs to generate the conventional
propulsion forces in the longitudinal
direction of the vessel [11]. One of the main
disadvantages of dynamic positioning
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ISSN: 2456-1851
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systems when compared to mooring systems
is the fuel costs consumed in operation [12].
These systems are used for different designs
and optimization, depending on cost and
safety requirements. This paper will keep its
focus on moored systems. It will review
numerical model developed to analyze the
dynamics of mooring lines, design and
optimization of mooring systems.
2. MOORING SYSTEM
A mooring system refers to any permanent
mechanism to which a floating object may
be secured by use of mooring lines. Mooring
systems are mainly composed of two
components: mooring line and anchor.
2.1. Mooring Line
Mooring lines may be made from chain,
wire rope, synthetic rope, or a combination
of these. Different combinations of line
material type [13], size, and location are
chosen in order to achieve given
requirements for the mooring performance
[14].
2.1.1. Chain
Chain is the most popular used for mooring
lines and is available in different size and
grades. The chains mooring lines utilize
their own weight to give good restoring
forces. These results to increase the top
tension of the lines and enlarge the vertical
loads on the vessel when the line is lifted
from the sea bottom [15]. Due to the lower
end of chain mooring line that is resting on
the water bed, the anchors only reacting to
the horizontal force. Furthermore chains
have good abrasion characteristics [16].
Figure 2: Studlink and Studless chain [17]
There are primarily two types of designs of
chain: studless and studlink chain as shown
in Figure 2. The studlink chain is commonly
used for floating structures that are moved
numerous times during their lifetime. The
stud provides stability to the link, resulting
in a chain that is strong, reliable and
relatively easy to handle. The studless chain
is commonly used for permanent moored
structures. Removing the stud reduces the
weight per unit of strength and increases the
chain fatigue life. However, this type of
chain is more expensive and less convenient
to handle [18].
2.1.2. Steel Wire Rope
The number of strands and wires in each
stand, core design and layout of strands is
critical for the required strength and bending
fatigue considerations of the wire rope [14].
International Journal of Engineering Technology and Scientific Innovation
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Figure 3 shows different type of wire rope
construction.
Single-strand ropes are commonly used in
permanent mooring systems. The wires are
wound as a helix with each layer rapped in a
different direction, providing torque
balancing which prevent the rope from
twisting as load is applied. This spiral strand
is more fatigue resistant than the multi-
strand wire rope. Sheathing with a
polyurethane coating, adding zinc filler
wires or using galvanized wires is a
common practice meant to enhance the
corrosion resistance. However, sheathing
provides the best performance, provided that
there is no damage to the sheath [18]. The
weight of the wire rope makes it suitable for
use [17].
The multi-strand wire ropes may contain
either a fiber or metallic core. This core
provides support to the outer wires,
especially in a drum, and may in some
applications absorb shock loading. Metallic
core ropes can be divided into two types:
independent wire rope core and wire-strand
core. Independent wire rope core is the most
common core for heavy marine applications.
The fiber core is used in lighter marine
applications [18].
Figure 3: Typical wire rope constructions
[17]
Steel wire rope has a lower weight than
chain, but approximately the same breaking
strength and higher elasticity. As a result it
does not result to increase the top tension of
the lines nor enlarge the vertical loads on the
vessel in case the line is lifted from the sea
bottom [8]. The wire rope constructions
consist of multiple wire strands wound in a
helical pattern around a center core to form a
rope. A six-strand wire rope is easy to
handle and is, along with studlink chain,
commonly used in temporary mooring. The
six-strand ropes are the most common type
of multistrand ropes used in the offshore
industry. To achieve higher strength the
wires have staggered sizes [18].
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2.1.3. Synthetic Fiber Ropes
The difference between a fiber rope system
and wire rope-chain systems is primarily the
non-linear stiffness. This is a nonlinear
minimum tension requirement and that the
location of the fiber rope segment needs to
be away from the fair-lead and the water-
floor. Fair-lead is where the mooring line
attaches the floater. In addition, unlike the
steel components the fiber rope stiffness
increases with mean load and decreases with
cyclic load range and with load relief over
time [14]. Fiber ropes for use in permanent
or temporary mooring systems normally
consist of polyester, aramid, high modulus
polyethylene (HMPE) or nylon. Polyester is
considered as a good candidate for mooring
applications due to its low cost, low stiffness
which induces less dynamic tension, good
fatigue properties, good strength to weight
ratio and good creep resistance [14]. Fiber
materials as HMPE and aramid are
considered suitable for applications where a
small rope diameter is required or for ultra-
deep water mooring applications. In shallow
water, nylon rope is often installed in the
mooring line to absorb energy from the
dynamics of the moored structure, due to its
high elasticity [14].
2.2. Anchor
Anchor is a device usually of metal or
reinforced concrete attached to a floater by a
marine cable to keep it in a particular
position by means of its weight or a fluke
that digs into water bottom. The choice of an
anchor is mainly dependent on water depth,
the soil behavior and the loads the anchor
needs to withstand, in addition to installation
method and cost. Figure 4 represents anchor
types ranged by water depth and soil type.
Figure 4: Typical anchor types ranged by
water depth and soil type [17]
1. Dead weight anchor: A dead weight
anchor typically consists of steel and
concrete. The horizontal and vertical load
capacity depends on the anchor submerged
weight and the friction between soil and
anchor, respectively. It may be used for
small mooring systems, but is normally not
used for deep water mooring systems [14].
2. Pile anchor: A pile anchor is a hollow
steel cylinder installed by use of a pile
hammer or vibrator. The anchor is able to
withstand both horizontal and vertical loads.
The capacity of this anchor is dependent on
the friction of the soil along the pile and the
lateral soil resistance [15].
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3. Drag embedment anchor: Drag
embedment anchors include both fluke
anchors and plate anchors. Installation is
performed by dragging the anchor into the
seabed. The anchor is well suited to
withstand horizontal loads. The capacity of
the anchor is dependent on size and angle of
the fluke or plate, the ability to penetrate and
the geotechnical conditions of the
installation area [15].
4. Suction anchor: The suction anchor also
consists of a hollow cylinder and is similar
to the pile anchor, although with a much
larger diameter. The anchor withstands both
horizontal and vertical loads, and the
capacity of it depends on the friction of the
soil along the cylinder wall and the lateral
soil resistance. These anchors can be
accurately positioned and are commonly
used for mooring at deep water [19].
5. Dynamically installed anchor: The
dynamically installed anchors include both
deep penetrating anchors and torpedo
anchors, and are designed to penetrate deep
into the seabed. There are no orientation
requirements on the loading for this anchor.
6. Vertical load anchor: Vertical load
anchors are installed in the same way as a
drag embedment anchor, but the penetration
depth is much larger. The anchor can
withstand both horizontal and vertical loads,
and is suited for deep water mooring
applications [15]. For more information on
Special anchors development for offshore
applications were reviewed by J. Atturio,
R.Taylor and P.Valent [20, 21, 22]. The
details on anchors sizing and pricing can
also were discussed by Baldt inc. and
Buttereld respectively [23, 24, 25].
2.3. Categories of mooring systems
2.3.1. Catenary mooring system
As shown on the Figure 5, the mooring line
is hanging freely and the whole cable profile
is suspended or part of its length rests on the
waterbed. A catenary line system usually
consists of chain links that relies on the
weight of links or clamp weight if used to
provide horizontal restoring force. If no
clump weight is attached, a very long
mooring line of chain links must be
considered to obtain adequate flexibility.
Hence, this concept might not be suitable in
shallow waters. Moreover, catenary line
systems will certainly induce vertically
downward loads [27]. Based only on the
motion responses of the floating structure,
the catenary mooring system is the most
suitable system because it exhibits the
smallest motion [28].
Figure 5: Catenary where mooring line
resting on the waterbed
2.3.2. Semi-Taut mooring system
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Figure 6 shows the semi-taut mooring
system where the lines are inclined and is
taut due to the pretension caused by the
platform excess buoyancy. The line does not
contact the waterbed and the anchor
experiences horizontal and vertical loads.
Most of the restoring loads are generated by
line elasticity. The mooring radius of the
semi-taut mooring system is smaller than
that of the centenary mooring system if
designed to support the same platform size
and weight. The semi-taut mooring system
come after the catenary system to have a
better response to the motion of the vessel as
water depth increases [28].
Figure 6: Semi-taut mooring line
2.3.3. Taut mooring system
The Figure 7 shows a taut line connected to
the anchor which is experiencing mainly a
vertical load. A taut-line system is
composed of wire or synthetic ropes and is
normally highly pretensioned. To investigate
the responses of taut mooring line against
hydrodynamic forces and external
excitation: Gottlieb and Yim [29] carried out
a stability analysis of a taut mooring system.
Umar and Siddiqui [30] carried out a
reliability analysis of taut mooring system
against yielding of taut moorings. As a
result, taut-line systems are usually quite
stiff both in horizontal and vertical
directions and can significantly reduce
vertical motions of the floating structure if
connected to the water bottom directly. Z.
Gao and T. Moan [27] found his feature is
certainly not acceptable for motion-
dependent structures like Wave energy
converters. In order to limit the influence of
mooring systems on vertical motions, the
top part of mooring lines, which is directly
attached to the floating, should be kept as
horizontal as possible. In such cases, buoys
can be attached.
Figure 7: Taut line
2.3.4. Taut mooring line with buoy
As Figure 8 shows, in this configuration the
buoy is attached to the sea bottom by a
vertical taut-line and connected to the
floating horizontally.
In 2011, Vicente et al.[32] investigated
different mooring configurations with slack
chain mooring lines of a floating point
absorber with or without additional sinkers
or floaters. It was found that the different
arrangement of the buoys and weights would
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bring significant differences in terms of
average and maximum tensions on the
mooring cables. In 2014, Zhi-Ming Yuan
and Atilla Incecik [31] studied the effects of
buoy position and its Volume with the
mooring system. They found that presence
of the subsurface buoy at half of the length
of the mooring cable in a single-line system
reduces the maximum static tension by
about 14 − 15% and by nearly 13% for
dynamic tension compared to the no buoy
condition. It was observed that the
displacement of the floating structure
increases as the buoy’s volume increases but
no optimal size or position of the buoy to
provide minimum displacement of the vessel
was studied [31]. It is necessary to establish
the relationship between buoy position and
size on one hand and the displacement of the
floater.
Figure 8: Mooring line with buoy [31]
2.4. Effects of water depth
The water depth has to be considered during
the selection and the design of the mooring
system. The water depth has different
impacts on the natural period and damping
ratio of the vessel motions moored by
catenary, semi-taut or taut mooring system.
From the numerical simulation, validated by
the experiment done in the Joint Laboratory
of Wind Tunnel and Wave Flume in Harbin
Institute of Technology, the global responses
of the semi-submersible platform attached
by mooring lines using catenary, semi-taut
and taut mooring systems in 500 m, 1000 m
and 1500 m water depth in the South China
Sea were compared[28]. It was seen that
there is an increase in surge and little
decrease of the pitch natural period with
water depth increase and the natural
damping ratios of the surge and pitch
decreases with increasing water depth. For
the most unloaded mooring line, the taut
mooring system is the most suitable due to
its small amplitude changes. For the most
loaded mooring line, the catenary mooring
system is the most suitable due to its small
peak value, followed by the semi-taut
mooring system. With increasing water
depth, the maximum tensions in lines
increase, indicating that when the length of
mooring lines becomes longer, the dynamic
forces in the mooring lines become more
significant [28].
2.5. Influence of Mooring line Damping
Damping is a characteristic of retaining the
equilibrium after a disturbance of the system
has occurred. The main sources of the total
damping for a moored structure are current
and viscous hull, radiation, wave drift force
and mooring line damping [34, 33]. The
dynamic responses of mooring line serve a
major role in the station keeping of any
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floating structure within water bodies. Thus
the accurate prediction of that response is
essential to have safe moored mechanism. It
is a useful parameter during the estimation
of the Low Frequency vessel motions for
moored offshore structures working in deep
water, whose nature frequency are close to
low frequency. When the LF becomes
similar to the natural frequency of the floater
will cause resonance, then the oscillation
amplitude of the floater will be magnified.
The mooring line induced damping
increases relative to other sources of
damping that are affecting the motion
response of the vessel considerably [33].
The work by Huse [36, 35] indicated that the
mooring line damping in surge for a floating
offshore oil and gas installation can
contribute as much as 80% of the total
damping. The increase of mooring line
damping can decrease the static tension by
reducing the LF motion amplitude, hence
the offset of the floater. It could also reduce
the dynamic tension in mooring line[38].
The problem is to find whether the increase
of the mooring line damping will increase or
decrease the total tension in the line. Thus
deep analysis of mooring line damping is
critical, particularly to satisfy the needs for a
safe station keeping of a floating platform. A
review of mooring line damping is presented
in the next section.
3. MOORING SYSTEM DAMPING
Mooring system damping is an important
parameter to analyze and optimize as much
as possible. This is indeed desirable because
if the mooring system damping increases it
will cause the system vibrations to die out
faster after an external disturbance. This can
be clearly seen in Figure 9.
Figure 9: Damping increases and system
vibrations die out quickly.
A moored floating platform system damping
is contributed by four components which are
the wave drift damping, the wind damping,
the current and viscous flow damping on the
hull, and the mooring line damping [33, 17].
Wave, wind and current damping are the
results of the environment forces on the
vessel here below shown in Figure 10.
Figure 10: Forces on a floating structure
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3.1. Wave drift and viscous damping
Moored vessels in water bodies are exposed
to large linear wave forces and moments,
which are linearly proportional to wave
amplitude and contain the same frequencies
as the waves. This linear component is also
known as first-order wave forces and it is
limited in the frequency scope of wave
spectrum [3].
In addition, floating structures are subjected
to nonlinear wave forces and moments
which are proportional to the square of the
wave amplitude. This is also known as
second-order wave force. The effects of
second-order wave forces are not often
considered since the magnitude of second-
order wave forces might be small relative to
the first-order force. However it may cause
resonance oscillations when its natural
frequency becomes similar to the natural
frequencies in surge, sway and yaw motions
of a semi-submersible positioned by
mooring or dynamic positioning system [39,
34] and [3]. The low frequency wave drift
force may excite the floater and mooring
system at their natural frequency, resulting
in resonant motions in both horizontal and
vertical planes. Therefore, the accurate
prediction of the wave drift forces exerted
on the structure is essential for safe and
optimum design of the mooring systems at
the initial stages.
The mean and slow drift forces on a moored
platform in water bodies could be calculated
by including difference frequency second-
order potential flow excitation [40].
Normally, it can be simplified by using
Newmans approximation and only including
quadratic terms from the first-order
potential. Pinkster [4] has made the first
attempt to estimate second-order wave drift
forces, where the wave forces were
calculated by means of quadratic transfer
functions. He calculated the quadratic
transfer functions for the low frequency
longitudinal force in head waves in regular
and irregular waves and compared them
with the experimental data. A reasonable
correlation was achieved considering the
complexity in both the test set-up and the
method of analysis. Stansberg et al. [41]
performed model tests with a moored semi-
submersible in irregular waves to evaluate
slow-drift wave forces and motions. The
experimental data were compared with
numerical predictions, based on traditional
potential flow theory as well as on empirical
drift coefficients. Large differences between
measurements and potential theory were
observed in high sea states, while the
empirical reconstruction compared well.
Hassan et al. [42] carried out a mode test in
scale 1:50 with a horizontally moored, large-
volume production semi-platform to study
slow-drift forces in currents and waves.
Berthelsen et al. [43] presented some main
results from the experiments and compared
them to time-domain numerical simulation
results where the slow-drift forces from both
the potential flow and the viscous drag
contribution were included. Moreover, many
researchers had studied about wave drift
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forces in the hydrodynamic response
analysis a moored semi-submersible
platform [44, 45, 28] and [46]. Schellin [47]
calculated and compared low-frequency
surge response of two moored floating
production platforms in waves using
numerical procedures based on time domain
simulations and frequency domain analysis.
They found that specifying a realistic
amount of wave drift damping is essential to
obtain reliable estimates of low-frequency
surge. Until now, to precisely predict the
drag coefficient for calculating viscous
damping is still a huge challenge to
researchers. The current study by Jian Hua
& Li Zhoub [3], a model test at the scale of
1:70 was used to measure the wave drift
force at low frequency for a semi-
submersible. The measured results were
presented and compared with numerical
diffraction analysis program based on
potential flow theory. In beam sea, wave
drift forces were predicted reasonably by
diffraction analysis within potential flow
theory for structures operating in both the
smaller and higher waves. In head sea, they
agreed well for the small wave, but there
was signicant difference for the higher
wave. One possible reason of that difference
yet to prove was that viscous effect on the
structure was neglected for the higher wave
in head sea. However, viscous drift forces
can be positive or negative. Therefore, cares
should be taken while adding viscous forces.
Study is needed on the viscous model to get
a better prediction.
3.2. Wind damping
The wind drag force is calculated based on
the formula as follow:
𝐹𝑤𝑖𝑛𝑑 =1
2𝜌𝑎𝑖𝑟𝐶𝑠𝐶𝐻𝑉10|𝑉10|𝑆
Where:
𝜌𝑎𝑖𝑟 : The density of air
𝐶𝑠: is the shape coefficient or drag
coefficient = 1 for large flat surface
𝐶𝐻: Height Coefficient, 𝐶𝐻 = 1 for FPSO:
Floating Production Storage and Offloading
𝑉10: Wind velocity at 10m above mean
water level
S: Project area of the exposed surface in the
vertical or the heeled condition
h: Vertical distance between center of wind
force and and center of resistance (by
mooring system).
3.3. Current damping
The current force is calculated using the
formula as follow,
𝐹𝑐𝑢𝑟𝑟𝑒𝑛𝑡 =1
2𝜌𝑤𝑎𝑡𝑒𝑟𝐶𝑑𝑈𝑓|𝑈𝑓|𝑆
Where:
𝜌𝑤𝑎𝑡𝑒𝑟: is the water density
𝐶𝑑: drag coefficient
𝑈𝑓: Current velocity
S: Project area of the exposed surface
3.4. Mooring line damping
The mooring-induced damping is one of the
main contributions to the low-frequency
damping, which further influences the
station keeping of floating structures. A
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reliable prediction of the mooring-induced
damping is essential for the estimation of the
low-frequency motion for floating structures
[48]. As discussed at the end of the previous
section, researchers have indicated that the
mooring line damping for a floating offshore
oil and gas installation can contribute
approximately 80% of the total system
damping. Thus what has been compelling
many researchers to develop different model
of estimating the mooring line damping to
insure safe and optimum design of the
mooring system.
3.4.1. Mooring induced damping
estimation
To estimate mooring induced damping,
Huse and Matsumoto [35, 37] and Huse [36]
applied the dissipated energy model.
Consider a moored floating body, its surge
motion is governed by the following
equation:
(𝑀 + 𝑚𝑎)𝑑2𝑋
𝑑𝑡2+ 𝛽
𝑑𝑋
𝑑𝑡+ 𝐾(𝑥)𝑋 = 𝐹(𝑡)
where: M is the floating barge mass, ma is
the floating barge additional mass by water,
X is the motion response of the floating
barge, β is the system damping
coefficienssst, K is the mooring line
stiffness and F(t) is the environmental load
which is causing motion to the floating
structure. The system damping is in the form
of an equivalent linear surge damping
coefficient β. The dissipated energy E
during one LF oscillation of period τ is
related to the linear coefficient β by the
formula.
𝐸 = ∫ 𝛽 (𝑑𝑋
𝑑𝑡)
𝜏
𝑂
2
𝑑𝑡
The linear damping coefficient β can be
obtained as:
𝛽 =𝐸
𝜋𝑋02𝜔𝑜
Where X0 is the amplitude of oscillation and
𝜔0 is the angular velocity.
3.4.2. Quasi-static method assumptions
The alternative for dissipation energy
method was to adopt a quasi-static method
where the following assumptions had been
made[49]:Firstly, inertia forces in the
mooring line were neglected compared to
drag. Secondly, line profile at any time
during the harmonic surge oscillation was
reasonably well described by the quasi-static
centenary equations. Thirdly, friction effects
of the seabed and internal damping of the
mooring line are not considered here.
Consequently, the mooring line damping is
due to drag forces acting on the mooring line
only. Drag forces acting perpendicular to the
line are considered while drag forces parallel
to the line are neglected. fourthly, The
transverse drag force on an element of the
mooring line is described by the Morison
formulation only.
Liu and Bergdahl [50, 51] then after
Bauduin and Naciri [52] whose model is
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called B&N model proposed improvements
on Huses quasi-static model for mooring
line-induced damping by approximating the
deformation of the line shape and the
transverse velocity of the line in more
accurate ways, respectively. Researchers,
Johanning et al., 2007; Sarkar and Eatock
Taylor, 2000; Webster, 1995 [48] had tried
to obtain the efficient and accurate
estimation of the damping, which can be
represented by the energy dissipation. In
2008, Tang et al. reviewed the studies on
mooring dynamic and concluded that it was
still lack of efficient approaches to predict
mooring-induced damping. Yuan et al. 2010
revealed the energy state of the mooring
lines and further predicted the dissipated
energy due to mooring line damping. In
2014 Dongsheng Qiao and Jinping Ou [53]
in their paper of mooring line damping
estimation for a floating wind turbine(FWT),
had used the energy absorption by a
mooring line resulting from the FWT motion
to derive the numerical estimation method.
They analyzed effects of excitation
amplitude, excitation period and drag
coefficient on the mooring line damping. It
indicated that With increase of drag
coefficient, the non-dimensional damping
almost linearly increases. This means that
the drag coefficient should be prudently
analyzed during the design. In brief, many
scholars prefer dissipated energy model to
estimate the mooring induced damping. The
accurate mooring system damping
prediction may depend also on the floating
structure viscous. So, it should be
considered for better prediction during the
optimum design of moored system.
3.5. Drag Coefficient
In the previous studies the researchers were
omitting the contribution of the mooring line
damping when predicting the motion of the
moored floater. This is due to the small drag
area of the mooring line. However referring
to what we have seen in some literature, the
mooring line damping contributes about
80% of the total mooring system damping.
Considering the result of the Marinteks
experimental study [54], surge amplitude
decrease of by 20 - 25% have been obtained
when mooring lines damping are included.
The amplitude of oscillation of the moored
floater is overestimated if the damping of
mooring line is omitted [55]. Thus, for
obtaining the accurate estimation of the
moored floater motion, the inclusion of the
mooring line damping which is dependent to
the drag force is crucial. Thus the study and
proper selection of drag coefficient(CD) is
important. A sufficiently exact
determination of drag force is required for
accurate prediction of mooring performance
and for selection of appropriate mooring
configuration [78]. Although, errors of
selecting drag coefficients on the mooring
components are less important due to small
drag area(A), they may well lead to
significant errors in predicting the moorings
dynamics[73]. With reasonable choice of
mooring line and buoyancy, it has to be
accepted that drag forces will cause non-
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negligible inclination of mooring line[114].
The drag force can be written as:
𝐹𝑑 =1
2𝐶𝑑𝜌𝐴𝑉2
Where Fd is the drag force, Cd is the drag
coefficient, ρ is the fluid mass density, A is
the cross sectional area and V is flow
relative velocity. The drag coefficient for
mooring components is normally considered
to be those of the corresponding bodies
shape for the appropriate range of Reynolds
numbers. Their data can be found in
engineering handbooks [76] [77] and [72].
3.5.1. Influential factors of drag
coefficient
The drag coefficient depends on Reynolds
(Re) and Keulegan Carpenter (KC) numbers.
The poor analysis of drag coefficient could
cause the large difference between
numerical and experimental studies of the
mooring system damping. In 1989, the study
by Huse and Matsumoto [62] show that
under superimposed WF motion, without
considering CD variations based on Re and
KC numbers, there is a large discrepancy
between numerical estimation of the
moorings damping and experimental results.
The numerical estimation over-predict the
damping of the mooring line by a factor
varying between 1.2 - 2 for different sea-
water conditions. Recently, the Phd
dissertation by Zhengqiang Xu [6]
concluded that the low Re number (lesser
than 106) has less effects on the CD
variation but KC number has meaningful
effects. The same case when the Re number
is high, the KC effects on the drag
coefficient is negligible but Re number has a
meaningful influence.
The challenge is to estimate the influence of
the surface roughness, transverse
oscillations and flow regimes (patterns) on
drag coefficient variation. In reality there is
a wide variety of surface roughness, from
small protrusions existing in the texture of
the surface itself to large roughness in the
form of marine growth. The roughness will
not only increase the projected area, but also
affect various aspects of the flow, such as
the separation angle, the turbulence level
and vortex shedding [6]. Therefore, the
effect of the surface roughness upon the
drag coefficients normally cannot be
neglected. The transverse oscillation can
have an effect of increasing the drag force,
which can be explained by two popular and
pragmatic approaches [38].
3.5.2. Mooring line response with
variation of drag coefficient
Many researchers have been changing the
CD of moorings to examine the effects of
mooring damping on floaters motion. In
2003 Luo and Baudic [63] reported that the
CD variations have negligible effect on the
floaters motion. Contrary, in 2001 Wichers
and Devlin [64] had found that effect of CD
variations on floaters motion is significant.
In 2002, the drag coefficient importance to
enlarge the mooring line damping was also
studied by Sarkar and Taylor [65]. The
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moorings damping could be very important
in reducing amplitudes of LF motions.
However, the mean drag of the moorings
due to current/wave force could also
increase the mean offset of floaters.
Depending on the contributions of these two
components, the final impact of the CD
variations could be case-dependent [63].
Indeed, the mooring line damping effects on
LF motion depend on its proportion in the
system damping and magnitude of the
system damping which is challenging to be
precisely determined.
4. DYNAMIC MODELING OF
MOORING LINE
In the moored platform, mooring lines are
important elements to care about. Its good
response to the environment drag forces will
lead to a meaningful stability of the floating
vessel. It is previously seen that the mooring
line contributes up to 80% of the mooring
system damping [36, 35]. Since 1960,
mooring line models were being studied to
predict the behavior of moored surface
vessels to extreme surface wave excitation
[66]. The researchers have been modeling
and analyzing mooring line dynamic using
three techniques which are lumped mass,
finite element and finite difference models
[67, 68]. Before that, it is better to
understand the limitations of static analysis
that was used before.
Quasi-static method is simple useful and
convenient for finding maximum mooring
lines tension due to environment load of
wind, current and waves. It is often used in
the preliminary design stage of mooring
systems [69]. It assumes the identical and
linear motion of the mooring system
between two static positions, during a given
time step for which the loads on the systems
are assumed constant [77]. With Quasi-static
analysis, the top end tension is determined
with respect to the displacement caused the
WF and LF motions.
However, the quasi-static method can result
in large errors when the dynamic response
of the mooring line is dominant, which has
been verified by experimental investigation
[71]. In Quasi-static analysis, the dynamic
effects associated with mass, fluid
acceleration, water bed friction and damping
on the mooring line are ignored [72]. In
quasi-static analysis the drag forces acting
on the mooring line perpendicularly are
considered to be responsible of mooring line
damping only and the forces parallel to the
line are neglected. It is obvious that Quasi-
static method is not considering mass
inertia, internal damping and hydrodynamic
drag loading [73], bending and stiffness
effects though there are some advanced
analytical techniques that try to account such
limitation of vibration[75,74]. Further
review on development and implementation
of quasi static approach can be found in
Bauduin et al.[52], Wang et al.[76], Chai et
al.[77] and Masciola et al. [78]. Because of
the above discussed limitations associated
with quasi-static analysis, a dynamic
mooring analysis is viewed as a rigorous
approach for measuring ultimate and fatigue
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loads in floating offshore structures
moorings. Dynamic mooring models also
feature the ability to easily model
cable/seabed contact with irregularly
contoured seafloors [79] and impact with the
seafloor, as well as the capacity to capture
fluid drag loading and vortex-induced
vibrations[80]. The severity of the sea state
also implies the importance of using a
dynamic mooring model in the simulation as
demonstrated in the DeepCwind
semisubmersible tank test campaign [81]
and [82].
4.1. lumped mass model
A lumped mass model(LM) consider the
continuum mooring line by a series of short
straight line elements. Furthermore, it
assumes that a considered length of the
mooring line can be approximated by a LM
that represents the motion of the line. Then
the hydrodynamic forces lumped on the
concentrated mass are calculated [83]. A
model can be defined as an LM system if the
corresponding mass matrix is strictly
diagonal. There are different variations of
LM model [84, 85, 87, 89, 90, 91]. The first
numerical analyses of the non-linear
dynamics of undersea cables was
represented by Walton and Polacheck [92].
It was based on a heuristic spatial
discretization of the mooring line in two
dimensions.
Figure 11: The lumped model as applied
to the simulation of a single point [66]
The Figure 11 shows the model graphically,
where the mooring line is considered to be a
series of mass less and inextensible finite
segments joined by frictionless pin at
specified positions which made the
representation to be flexible and no bending
or torsional stiffness was considered. Walton
and Polacheck obtained a series of ordinary
differential equations governing the motion
of each node point using Newtons second
law by look at the gravitational,
hydrodynamic and buoyant forces and the
mass of the line at the node points. The
Newton-Raphson approach was then used
solve these equation. This model has
continued to be popular regarding dynamic
analysis of mooring line. Many researchers
have been applying this approach to estimate
waves and gravitational forces on mooring
line in different perspectives. Hicks and
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Clark [93], Nath and Felix [94] and
Merchant and Kelf [95] applied lumped
mass model to analyze the dynamics of
single point moorings. Later Kelf and
Merchant [96] applied it for mooring line
with buoy dynamic analysis. Matsubara et
al. have used the lumped mass model to
simulate the two dimensional motion of a
buoy-cable system for aquaculture
applications [97]. During the assessment of
the importance of composite mooring line
dynamic response in station keeping by
Khan and Ansari [98], the LM had shown
flexibility to simulate the assembly of chain,
cable and synthetic rope that composed each
mooring line. Such flexibility makes the LM
popular in many offshore engineering
practices [99]. Recently, the investigation
done by the national renewable energy
laboratory, lumped mass model was
preferred for implementation in mooring
analysis program over other models based
on its simplicity, low computational cost,
and ability to provide physics similar to
those captured by higher-order models [67].
However for applications where knowledge
of the bending and torsional moments is of
consequence, linear elements are not
adequate since they do not exhibit any
curvature or twist [17]. Bending effects of
cable are important in low-tension towing
maneuvers[85] and for fatigue analysis in
taut mooring systems [86], but bending also
augments the stability of the numerical
model[87, 88]. The use of lumped mass
models requires to provide cable length as
input data and when the mooring line
contact the waterbed it will be hard to find
out the location of the point [100]. The LM
representation traditionally has been derived
heuristically using Newton-Euler methods,
but it can also be obtained based on
Lagrange and Hamiltonian mechanics [101].
Further uncovered description of LM model
on mooring line can be found in [102, 103,
104].
4.2. Finite element analysis
The Finite Element Analysis(FEA) method
is a numerical method by which the
mechanism, structure or continuum is
divided into interconnected small finite
segments. The physical characteristics
within and around a considered segment are
similar to that of its nodes. The marine cable
elements are commonly assumed to be
straight lines. Its accuracy is then dependent
on the number of elements. However,
curved cable elements have been shown to
be more accurate than the straight line
element when continuity of slope across
nodal points is enforced [67] FEA models
have been applicable over many years ago
[105, 106, 107, 108] to capture advanced
features to include improved numerical
integration, hence increases stability [110].
Comparing FEA to LM, FEA model is able
to achieve good results with lower
discretization [92, 108]. Ketchman and Lou
[111] demonstrated that the LM
methodology converges into the same
results with FEA representations when the
discretization size is sufficiently small. Yang
and Teng [112] used FEA approach to
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analyze the static and dynamics of mooring
line. Garett [105, 88] and Ran[113]
developed a specific FEA model that
includes bending stiffness. The derivation
process initiated in[105, 114, 113] is similar
to the comprehensive high order LM
approach in [115]. Besides the method
developed in [105, 88, 113] that is based on
Galerkins method of weighted residuals, a
different basis function can be used to obtain
the equation of motion for the discretized
cable system[116].
Further detailed description of finite element
modeling for mooring lines can be found in
[117, 118, 119, 120].
4.3. Finite difference
The above two models have shown to not
account elasticity and bending stiffness of
the mooring line as the cable is studied as a
series of divided linear elements. The
inclusion of bending stiffness is achievable
with Finite difference approach based on the
demonstration done by Howell and
Triantafyllou for low-tension cable or chain
numerical simulation [121]. The Finite
difference model (FD) differs from FEA by
replacing piecewise gradients with first
order difference functions. In other words,
FEA computes derivatives of the basis
function exactly while FD estimates the
gradients. Thomas and Hearn [122]
developed a time-domain finite-difference
technique that accounts the seabed friction
effects as well as the lifting and grounding
of the seabed-lying portion of the cable.
Huang [123] used finite difference method
to analyze the dynamic behavior of marine
cable in three dimensions. Hover et al.[124]
used finite difference scheme in the
Calculation of dynamic motions and
tensions of towed underwater cables. In
2006 Gobat and Grosenbaugh [125]
investigated the numerical limitations of FD
model, and their effort gave out a clear
understanding of how the method of
integration leads to stability. Even if FD
model has limitations of numerical
implementation, it is easier implemented
into a computer code than LM or FEA. It
will be of advantage if the numerical
challenges of it are addressed. FD models
gives high fidelity modeling capabilities
compare with FEA model. In 2008 Matuela
et al. [126] developed mathematical model
and a matching numerical approach based
on finite differences to predict the static
configuration of mooring or towing
compound cables. Further detailed
descriptions of implementing finite
differences for mooring line, cable and/or
riser models are given in [127, 128, 129,
130]. To summarize, FD model is not
popularly used in commercial applications
because of its numerical limitation, and
more research is needed to improve and
simplify the approach [67].
4.4. Finite Segment
Even if the lumped mass, finite differences
and FEA are the most popular discretisation
schemes for mooring lines. Researchers like
Winget and Huston [131] and Kamman and
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Huston [132] utilised a finite segment
scheme consisting of a series of ball-and-
socket connected rigid rods, to discretize a
mooring line. Nichol et al. [133] developed
a finite segment model for the mooring
system of floating tidal energy devices.
Garrett [114] utilizes a similar scheme
consisting of elastic rods. Filipich and
Rosales [134] model a chain mooring line,
by discretizing the chain into its individual
links.
5. DESIGN & OPTIMIZATION OF
MOORING SYSTEM
The need of offshore exploration of oil and
gas in deep sea waters is increasing and now
can reach beyond 2500m.The use of
mooring system to station-keeping position
of any floating platform in deep water has
proved to be efficient over other means. This
has been compelling researchers to find out
an optimum design of mooring system for
different sea-state.
5.1. Design consideration
The mooring design must be an integral part
of the overall floating structure design,
because the mooring system not only
influence the capital costs, but also the
system performance in both operational and
survival sea-states. The objective is to find
design solutions to mitigate peak mooring
loads, while avoiding the costly overdesign
or compromising the performance of the
floater[135]. The design consideration
associated with a mooring system here
discussed includes design criteria, design
loads, design life, operation and
maintenance considerations. In the
following, the design criteria with respect to
the design limit states and the design loads
with respect to the environmental criteria are
described.
5.1.1. Design Limit States
The design criteria are formulated in terms
of three limit states: Ultimate limit state
(ULS), Accidental limit state (ALS) and
Fatigue limit state (FLS). DNV Offshore
Standard [136] defines the limit states as
following.
• An ultimate limit state to ensure that the
individual mooring lines have adequate
strength to withstand the load effects
imposed by extreme environmental actions.
The ULS requires that the mooring lines
shall resist all known loads with a sufficient
margin, and states that a design against
overload of an intact mooring system in
extreme weather shall be conducted.
• An accidental limit state to ensure that the
mooring system has adequate capacity to
withstand the failure of one mooring line,
failure of one thruster or one failure in the
thrusters control or power systems for
unknown reasons. A single failure in the
control or power systems may cause that
several thrusters are not working. The ALS
requires that an accidental event shall not
develop into progressive collapse, hence a
design against overload for a damaged
system in extreme weather conditions shall
be performed. A damaged system is
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considered as a system where one or two
line failures have occurred.
• A fatigue limits state has to be analyzed to
ensure that the individual mooring lines
have adequate capacity to withstand cyclic
loading. Analysis of the mooring system
shall be performed in accordance with these
three limit states.
The mooring line design for permanent
mooring must satisfy all three limit states.
The FLS requires that the safety margin
against fatigue failure shall be acceptable.
The mooring system shall thus be designed
against fatigue failure, taking all possible
sea states into account [136]. In order to
consider the FLS, a wide range of
environmental conditions is needed. The
following description of the properties,
analysis and fatigue safety factor is based on
offshore standard [136]. The fatigue
damage, D, in mooring line components are
accumulated by cyclic loading, and summed
up from the fatigue damage arising from
Environmental states combined to simulate
the long term environment that the mooring
system is exposed to
𝐷 = ∑ 𝑑𝑖
𝑛
𝑖=1
Where di is the fatigue damage to the
component arising in sea state i and defined
as
𝑑𝑖 = 𝑛𝑖 ∫𝑓𝑠𝑖(𝑠)
𝑛𝑐(𝑠)
∞
0
𝑑𝑠
Where ni is the number of stress cycles
encountered in sea state i, f S i(s) is the
probability density of stress cycles in sea
state I and nc(s) is the number of stress
cycles leading to failure. The number of
stress cycles in sea state i is defined as:
𝑛𝑖 = 𝑁𝑃𝑖
Where N is the total number of stress cycles
during the entire lifetime and Pi is the
probability of occurrence of sea state i. The
capacity of a component is described by the
S-N curve
𝑛𝑐 = 𝑎𝐷𝑆−𝑚
Where aD and m are parameters of the S-N
curve dependent on the mooring line
composition.
Figure 12 presents S-N curves for different
mooring line compositions
Figure 12: Design S-N curves [136]
Fatigue analysis is generally performed by
frequency domain method, where both wave
frequency tension cycles and low frequency
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tension cycles are taken into account. The
fatigue damage in the environmental state i
is determined by:
𝑑𝑖 =𝑛𝑖
𝑎𝐷𝐸[𝑆𝑖
𝑚]
Where 𝐸[𝑆𝑖𝑚] is the expected value of the
nominal stress ranges raised to the power m
in environmental state i. If the low
frequency content of the stress process is
neglectable, a narrow-banded assumption
can be applied. Fatigue damage in
environmental state i then becomes:
𝑑𝑖 =𝑉𝑜𝑖 𝑇𝑖
𝑎𝐷
(2√2𝜎𝑠𝑖)𝑚
𝛤 (𝑚
2+ 1)
Where 𝜎𝑠𝑖 is the standard deviation of the
stress process, Γ() is the gamma function,
V0i is the mean up crossing rate of the
tension process and 𝑇𝑖 is the duration of the
environmental condition. The intent of the
fatigue limit state is to ensure sustainable
resistance to fatigue failure of each type of
Component in an individual mooring line.
The design equation for FLS is given as:
1 − 𝑑𝑐 𝛾𝐹 ≥ 0
Where 𝑑𝑐 the characteristic fatigue damage
is accumulated as a result of cyclic loading
during the design life time, and 𝛾𝐹 is the
single safety factor for the fatigue limit state.
In the fatigue analysis, the fatigue safety
factor shall cover a range of uncertainties.
For mooring lines that are not regularly
inspected, the safety factor is thus given as:
𝛾𝐹 = 5 𝑖𝑓 𝑑𝑓 ≤ 0.8
𝛾𝐹 = 5 + 3 (𝑑𝐹 − 0.8
0.2) 𝑖𝑓 𝑑𝑓 > 0.8
Where 𝑑𝑓 is the adjacent fatigue damage
ratio. The ratio between the characteristic
fatigue damage dc in two adjacent lines
taken as the lesser damage divided by the
greater damage. Further description of
different techniques useful to analyze the
fatigue of moorings and risers in floating
production systems for offshore oil and gas
exploration can be found in [137, 138, 139,
140, 141]. Also Snap loads on moorings
were found to significantly influence
damage in several experiments [139, 142,
143]. Thus considering the effect of snap
loads is crucial for assessing the fatigue of
mooring lines. Palm et al.[144] developed a
model that captures the real amplitude and
duration of snap loads in mooring lines.
5.1.2. Environmental Criteria
There are mainly two classifications of
environmental conditions when evaluating a
mooring system; maxi-mum design
condition and maximum operation
condition.
1. Maximum Design Condition: The
maximum design condition is described by
the combination of waves, wind and current
for which the mooring system is designed.
This condition is defined as extreme
combinations of wind, waves and current
causing an extreme load in the design
environment [14]. The environmental effects
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applied for the calculations of design limit
states above discussed in section, should
include the most severe combinations of
waves, wind and current with a return period
of no less than 100 years for the
combination. The most severe conditions are
those leading to the most extreme mooring
loads. In order to determine the most
unfavorable conditions, both intensity and
directions of the environmental effect are of
importance [136]. The environmental loads
are specified in terms of:
Significant wave height (Hs )
Peak wave period (Tp )
Wave spectrum
Wave energy distribution
Main wave direction
Mean wind speed, over a 1 hour
averaging period 10m above sea
level (U 1hour, 10m)
Wind spectrum function
Wind direction
Surface current speed (Vc )
Current profile over depth
Current direction
2. Maximum Operation Condition: The
maximum operating condition is defined as
the combination of waves, wind and current
in which the unit is capable of continue to
work, including for instance to drill,
produce, offload or maintain gangway
connection. This condition shall not exceed
the maximum design condition [14]. In
order to obtain a 100-year design
environment, different sets of conditions are
investigated. In accordance with [145],
waves of a sea state with return period of
100 years should normally be used. These
wave conditions shall include different
combinations of significant wave heights
and peak periods. In addition, the mean
wind speed 10 m above the water surface
with a 100-year return period and a surface
current speed with a 10-year return period
should be applied. Both wind and current
should be based on the marginal distribution
of the wind and current speeds at the
specific location respectively [136].
5.2. Optimization
In engineering many optimization problems
are naturally very complex and hard to find
their solution by conventional optimization
techniques [146,147]. To address such
challenge, in 1960s researchers started an
new techniques named evolutionary
algorithms where they had imitated living
beings by simulating the process of natural
evolution of human beings [148, 150, 149].
Today the use of genetic algorithms (GAs)
has become popular among evolutionary
International Journal of Engineering Technology and Scientific Innovation
ISSN: 2456-1851
Volume:03, Issue:05 "September-October 2018"
www.ijetsi.org Copyright © IJETSI 2018, All rights reserved Page 224
algorithm types. In 2014 Tianhui Fan [151,
152] used it to optimize his design of
truncated mooring system based on static
and damping equivalent. In 2006, M.
Shafieefar and A. Rezvani [1] used the same
techniques of GAs to optimize the design of
moorings for floating structures. They
mentioned the aspect to be considered
during the mooring system optimization.
Firstly the platform heading, this accounts
the environmental forces directional
distribution function. Secondly the mooring
pattern which consider the mooring system
holding capacity factor like anchor position,
Thirdly, the mooring line tension or length,.
Fourthly the mooring line materials and
sizes and finally automation to minimize
time taken during design. They have
presented a codes to optimize the design of
moored floating structures which determine
floating structures offset and handles design
constraint like safety factor of the lines. The
code implementation has shown good results
to mooring design optimization cases.
However, it was noticed that, they had
considered safety factor constraint of
mooring lines only. It means that they were
able to control the tension limit of lines but
there was no information of anchor tension.
The anchor tension could be considered as
constraint of mooring system design as its
weight practically matter and that is why it
is needed to take it into consideration as a
design constraint by further researchers.
6. CONCLUSION
Mooring system is mechanism used to
control the position of floating structures in
water by means of marine cables.
Researchers have been studying mooring
line statically and were unable to analyze the
effects of friction and bending strength. In
summary, this review found that the
mooring line motion can cause resonance
when its natural frequency becomes similar
to that of the floater. The mooring line
motion is due to the drag force and depends
on drag coefficient. In the analysis of the
floater motion with respect moored system
and to drag forces. The selection of drag
coefficient should involve the Re and KC
numbers otherwise it will results a large
discrepancy between numerical and
experimental results.
Among the gaps found during this review
are the unclear relationship between
mooring line damping and mooring line total
tension. It is seen that the increase of the
mooring line damping will decrease the
amplitude of low frequency motion, hence
static tension. It could also increase the
dynamic tension, however it was not seen
whether it will increase or decrease the total
line tension. It has been seen that the finite
difference approach of mooring line
dynamics would lead to stability, give high
fidelity modeling capabilities. However it
has limitation of numerical implementation.
There is a need to investigate and simplify
the implementation of finite difference
model by overcoming its numerical
limitations. It was reviewed that the mooring
line damping plays major part to the total
International Journal of Engineering Technology and Scientific Innovation
ISSN: 2456-1851
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mooring system damping. This depend to
the hydrodynamic forces on the line which
is relative to the drag coefficient. The
surface roughness effect on CD values
variation of mooring line is not considered
in any analysis reviewed. Actually, the
impact of surface roughness could
considerably influence the variation of CD.
So it might be important to carry out the
investigation of this effect.
It has been seen that both the position and
volume increase of the buoy affect the
mooring line tension hence the floater offset.
However there is no code has been
generated to automatically predict the
optimum position and volume of the buoy
with maximum allowable floater offset
desired.
REFERENCES
[1] Mehdi S. Aidin R., Mooring
optimization of floating platforms using
agenetic algorithm
www.researchgate.net/publication/23590819
6; 2006.
[2] Philip, Nallayarasu, & Bhattacharyya.,
Experimental investigation and CFD
simulation of heave damping effects due to
circular plates attached to spar hull Nimmy,
Ships and Offshore Structures,
http://dx.doi.org/10.1080/17445302.2013.83
5146, 2013.
[3] Jian Hua and Li Zhoub., Experimental
and numerical study on wave drift forces on
a semi- submersible platform in waves
College of Shipbuilding Engineering, Harbin
Engineering University, Harbin, P.R. China
& Aker Solutions, Fornebu, Norway, 2015
[4] Pinkster JA. Low frequency second order
wave exciting forces on oating structures.
Delft (the Netherlands): Delft University of
Technology, 1980
[5] Yipeng Pana, Prasanta Kumar Sahooa &
Lin Lub Numerical study of hydrodynamic
response of mooring lines for large floating
structure in South China Sea, Taylor &
Francis, 2015.
[6] Zhengqiang Xu Phd thesis: Drag
Coefficient and Damping of Moorings and
their Effect on FPSOs Response University
of Strathclyde, Glasgow Department of
Naval Architecture, Ocean and Marine,
2014.
[7] Ioannis K. Chatjigeorgiou, Ioannis
Thanos, Paraskevi Bourma, Thomas
Mazarakos and Spyros A. Mavrakos;
Mooring system & motion response analysis
of a gas import terminal in operating and
survival conditions, National Technical
University of Athens, School of Naval
Architecture and Marine Engineering
Laboratory of Floating Structures and
Mooring Systems 9 Heroon Polytechniou
Ave, GR157-73, Greece, 2005
[8] O.M. Faltinsen, Book: Sea loads on ships
and offshore structures, Cambridge
university press, 1990.
[9] Sue Wang, On the Assessment of
Thruster Assisted Mooring, American
International Journal of Engineering Technology and Scientific Innovation
ISSN: 2456-1851
Volume:03, Issue:05 "September-October 2018"
www.ijetsi.org Copyright © IJETSI 2018, All rights reserved Page 226
Bureau of Shipping Houston, Texas, USA,
2012.
[10] S. Ryu, Hull/Mooring/Riser Coupled
Motion Simulations of Thruster-Assisted
Mooring Platforms, Texas A&M University,
2003.
[11] Dietmer Deter, Conference of Dynamic
Positioning, Marine Technology Society,
1997.
[12] Aalbers, B. Albert, de Vries, Leo; van
Vugt, Hans, Dynamic Positioning,.
Conference, Fuel consumption and emission
predictions: application to a DPFPSO
concept. Houston, October 2006.
[13] Ramberg, S. E. and Gri n, O. M., Free
Vibrations of Taut and Slack Marine Cables
Journal. of Struct. Div., ASCE, Nov. 1977.
Also, see discussion in the June 1978 issue.
[14] API Recommended Practice, Design and
Analysis of Station keeping Systems for
Floating Structures., 2005.
[15] Vryhof, Anchor Manual, 2015.
[16] DR. IR. Gerad Van OORTMERSSEN,
The motions of a moored ship in waves,
Publication no. 510 Netherlands ship model
basin Wageningen, the netherlands, 2008.
[17] K. E. Klingan, Automated optimization
and design of mooring systems for deep
water, M.thesis, Norwegian University of
Science and Technology, 2016.
[18] SUBRATA K. Chakrabarti, Handbook of
offshore Engineering Offshore Structure
Analysis, Inc, Elsevier Ltd,2005
[19] G.T. Houlsby and B.W. Byrne, Design
Procedures for Installation of Suction
Caissons in Clay and Other Soils. OUEL
2268/04,2004 [20] Atturio, J. M., Valent, P. J.,
and Taylor, R J.,”Preliminary Selection of
Anchor Systems for OTEC,’” Ocean
Engineering, Vol. 6, Nos. 1/2, 1979
[21] Taylor, R. J., Jones, D. and Beard, R. M.,
Uplift-Resisting Anchors, Ocean Engineering,
Vol. 6, Nos. 1/2, 1979
[22] Valent, P. J., Taylor, R. J., Atturio, J.
M., and Beard, R. M., Single Anchor Holding
Capacities for OTEC in Typical Deep Sea
Sediments Ocean Engineering, Vol. 6, Nos. 1/2,
1979.
[23] Baldt Inc. Baldt Anchor Catalogue.
Chester (PA): Baldt.1990a
[24] Baldt Inc. Baldt chain catalogue. Chester
(PA): Baldt. 1990b.
[25] Musial W, Buttered S. Future for
offshore wind energy in the United States,
Energy Ocean 2004 Conference; June 2829;
Palm Beach, Florida.
[26] Mohammed Khair Al-Solihat and Meyer
Nahon; Stiffness of slack and taut moorings,
Francis and Taylors, 2015.
[27] Z. Gao and T. Moan; Mooring system
analysis of multiple wave energy converters in
a farm configuration, Proceedings of the 8th
International Journal of Engineering Technology and Scientific Innovation
ISSN: 2456-1851
Volume:03, Issue:05 "September-October 2018"
www.ijetsi.org Copyright © IJETSI 2018, All rights reserved Page 227
European Wave and Tidal Energy Conference,
Uppsala, Sweden, Centre for Ships and Ocean
Structures, Norwegian University of Science
and Technology, Otto Nielsens vei 10, NO-
7491, Trondheim, Norway, 2009
[28] Dongsheng Qiao and Jinping Ou,
Global responses analysis of a semi-
submersible platform with different
mooring models in South China Sea, Deep-
water Engineering Research Center, Dalian
University of Technology, Dalian, China /
Taylor & Francis, 2012.
[29] Gottlieb, O. and Yim, S. C. S., Nonlinear
oscillations, bifurcations and chaos in a multi-
point mooring system with a geometric
nonlinearity, Appl. Ocean Res; 1992
[30] Umar, A. and Siddiqui, N. A., Reliability
analysis of a moored vessel, Journal of
Structural Engineering, SERC, India, 2002
[31] Zhi-Ming Yuan & Atilla Incecik
Numerical study on an hybrid mooring
system with clump weights and buoys;
Ocean Engineering, 2014
[32] Vicente P.C., Falc£o A.F., Justino P. J
Slack-chain mooring configuration analysis of a
floating wave energy converter. 26th
International Workshop on Water Waves and
Floating Bodies, Athens, Greece.2011
[33] Yang, W.S., Phd thesis: Hydrodynamic
Analysis of Mooring Lines Based on Optical
Tracking Experiments. Texas A & M
University, December 2007.
[34] Lars Johanning, George H. Smith,
Julian Wolfram; Measurements of static and
dynamic mooring line damping and their
importance for floating and underwater
WEC devices, Elsevier ltd, 2007
[35] E. Huse, Influence of mooring line
damping upon rig motions, In: Proceedings
of the 18th Offshore Technology Conference;
1986 May 58 Houston, TX. p.433438.
[36] Huse E. New developments in prediction
of mooring system damping in; Proceedings of
the 23rd Offshore Technology Conference;
1991 May 69; Houston, TX. p. 291298.
[37] E. Huse, Matsumoto K. Practical
estimation of mooring line damping,
Proceedings of the 20th Offshore
Technology, 1988.
[38] JOURNE, J. M. J. & MASSIE, W. W.
Offshore Hydromechanics, Delft University
of Technology, 2001.
[39] Bayati, Jonkman J, Robertson A. The
effects of second-order hydrodynamics on a
semi-submersible floating offshore wind turbine.
Journal of Physics, 2014.
[40] Faltinsen OM., Sea loads on ships and
ocean structures. Cambridge: Cambridge
University Press, 1990
[41] Stansberg C, Yttervik R, Nilsen F. Wave
drift forces and response in storm waves.
Proceedings of the Seventh International
Symposium on Practical Design of Ships and
Mobile Units;1998.
International Journal of Engineering Technology and Scientific Innovation
ISSN: 2456-1851
Volume:03, Issue:05 "September-October 2018"
www.ijetsi.org Copyright © IJETSI 2018, All rights reserved Page 228
[42] Hassan A, Downie M, Incecik A,
Baarholm R, Berthelsen P, Pakozdi C,
Stansberg C. Contribution of the mooring
system to the low-frequency motions of a
semisubmersible in combined wave and current.
Proceedings of the ASME 2009 28th
International Conference on Ocean, O shore and
Arctic Engineering; 2009 May 31Jun 5;
Honolulu (HI): ASME, 2009.
[43] Berthelsen P, Baarholm R, Pakozdi
C, Stansberg C, Hassan A Downie M,
Incecik A. Viscous drift forces and
responses on a semisubmersible platform in
high wave, Proceedings of the ASME 2009;
28th International Conference on ocean Off
shore and Arctic Engineering; 2009 May
31Jun 5; Honolulu (HI): ASME, 2009
[44] Nallayarasu S, Siva Prasad P.
Hydrodynamic response of spar and semi-
submersible interlinked by a rigid yole part I:
regular waves. Ships Offshore Struct.
7(2):133141,2012.
[45] Nallayarasu S, Siva Prasad P.
Hydrodynamic response of spar and semi-
submersible interlinked by a rigid yole part II:
random waves, Ships Offshore Struct.
7(2):133141,2012.
[46] Ye Q, Jin W, He Y, Bai Y. System
reliability of a semi-submersible drilling rig.
Ships Offshore Structures. 2013
[47] Schellin, T. E., Jiang, T.and Sharma S.
Numerical prediction of low-frequency
surge of two moored floating production
platforms; Proceedings of Tenth
International Symposium and Exhibit on
Offshore; Mechanics and Arctic Eng., Vol.
1-A, Offshore Technology, Houston,
pp.165174
[48] Lingzhi Xiong, Wenhua Zhao, Study on
global performances and mooring- induced
damping of a semi-submersible, Article in
China, Ocean Engineering October 2016.
[49] Tianhui Fan, Dongsheng Qiao &
Jinping Ou, Innovative approach to design
truncated mooring system based on static
and damping equivalent, Taylor & Francis,
Ships and Offshore Structures, 9:6, 557-568,
DOI: 10.1080/17445302.2013.867631,2014.
[50] Liu, Y. Dynamics and Extreme Value
Problems for Moored Floating Platforms.
Ph.D. Thesis, Chalmers University of
Technology, Gothenburg, Sweden, 1998.
[51] Liu, Y.; Bergdahl, L. Frequency-
domain dynamic analysis of cables. Eng.
Struct. 1997, 19, 499506
[52] Christian Bauduin & Mamoun Naciri,
A Contribution on Quasi-Static Mooring
Line Damping, Journal of Offshore
Mechanics and Arctic Engineering, 2000.
[53] Qiao, D. & Ou, J., Mooring line
damping estimation for a floating wind
turbine., The American Naturalist Scientific
World Journal, 2014, 840283.
https://doi.org/10.1155/2014/840283, 2014
[54] HUSE,E. Influence of mooring line
damping upon rig motions, Offshore
International Journal of Engineering Technology and Scientific Innovation
ISSN: 2456-1851
Volume:03, Issue:05 "September-October 2018"
www.ijetsi.org Copyright © IJETSI 2018, All rights reserved Page 229
Technology Conference. Houston, Texas,
1986.
[55] NAKAMURA, M., KOTERAYAMA,
W. & KYOZUKA, Y. Slow drift damping
due to drag forces acting on mooring lines,
Ocean Engineering, 18, 283296. 1991.
[56] Casarella M.J. and M. Parsons Cable
systems under hydrodynamic loading, J.Mar
Technol Soc. 1970
[57] M. Finker and G. Siedler, Drag
coefficients of oceanographic mooring
components, Kiel University, 1985.
[58] Fofonoff N.P. Buoy-system motions,
Hand book of ocean and underwater
engineering, McGraw Hill, 9-109 to 9-115,
1969.
[59] Sass F. & Ch. Bouche, Handbook of
ocean engineering, Dubbel Taschenbuch fur
Maschinenbau, Springer-Verlag,884 pp;
1956.
[60] Hoerner, S.F. Fluid Dynamics Drag
Publ. by the Author New Jersey, 1965.
[61] Myers, D.A., Holm C. H. & R.F.
McAllister, Handbook of ocean and
underwater engineering, McGraw Hill 1-2
to 12-112pp, 1969.
[62] HUSE, E. & MATSUMOTO, K.
Mooring line damping due to first and
second order vessel motion, Offshore
Technology Conference. Houston, Texas,
1989.
[63] LUO, Y. & BAUDIC, S. Predicting
FPSO responses using model tests and
numerical analysis, 13th International
Offshore and Polar Engineering. Conference
(ISOPE-2003), Honolulu, Hi. 167-174,
2003.
[64] WICHERS, J. E. W. & DEVLIN, P. V.
Effect of coupling of mooring lines and
risers on the design values for a turret
moored FPSO in deep water of the Gulf of
Mexico, 11th International Offshore and
Polar Engineering Conference
(ISOPE2001), Stavanger, Norway. 480-487,
2001.
[65] Sarkar, A., Taylor, R.E., Dynamics of
mooring cables in random seas, J. Fluids
Struct. 16 (2), 193212, 2002.
[66] Bradley J. Buckham, Dynamics
Modelling of Low-Tension Tethers for
Submerged Remotely Operated Vehicles.
University of victoria, 1997.
[67] J. J. Marco Masciola and A. Robertson,
Extending the capabilities of the mooring
analysis program: A survey of dynamic
mooring line theories for integration into
fast, National Renewable Energy
Laboratory, 2014
[68] Chatjigeorgiou, I. K. and Mavrakos, S.
A. Comparative evaluation of numerical
schemes for 2D mooring dynamics, Int. J.
OffshorePolar Eng;2000.
[69] Y.Inoue, H.Miyabe, X.Weiyi and
M.Nakamura, Comparative Study on the
Quasi-Static Analysisand Dynamic
International Journal of Engineering Technology and Scientific Innovation
ISSN: 2456-1851
Volume:03, Issue:05 "September-October 2018"
www.ijetsi.org Copyright © IJETSI 2018, All rights reserved Page 230
Simulations for Estimating the Maximum
Tensions of Mooring Lines, International
Offshore and Polar Engineering
Conference, 1991.
[70] Vickers, A. Improve the Understanding
of Uncertainties in Numerical Analysis of
Moored Floating Wave Energy Converters.
Ph.D. Thesis, University of Exeter, Exeter,
UK, 2012.
[71] PAPAZOGLOU, V. J., MAVRAKOS,
S. A. & TRIANTAFYLLOU, M. S.
Nonlinear cable response and model testing
in water. Journal of Sound and Vibration,
140, 103-115,1990
[72] Johanning, L.; Smith, G.H.; Wolfram,
J. Towards design standards for WEC
moorings. In Proceedings of the 6th
European,Wave and Tidal Energy
Conference, Glasgow, UK, 29 August 2
September 2005.
[73] Hall, M.; Goupee, A. Validation of a
lumped-mass mooring line model with
DeepCwind semi-submersible model test
data. Ocean Eng. 2015, 104, 590603
[74] Griffin, O. M. and Rosenthal, F., The
Dynamic Of Slack Marine Cables, J.
Offshore Mech. Arct. Eng., 11(4), pp.
298302, 1989.
[75] Starossek, U. Cable Dynamics a
Review, J. Structural Eng. Int., 4, pp.
171176, 1994.
[76] Wang, L.Z.; Guo, Z.; Yuan, F. Quasi-
static three-dimensional analysis of suction
anchor mooring system. Ocean Eng. 2010,
37, 11271138.
[77] Chai, Y.; Varyani, K.; Barltrop, N.
Semi-analytical quasi-static Formulation for
three-dimensional partially grounded
mooring system problems. Ocean Eng. 2002,
29, 627649
[78] Masciola, M.; Jonkman, J.; Robertson,
A. Implementation of a Multi segmented,
Quasi-Static Cable Model. In Proceedings of
the 23rd International Offshore and Polar
Engineering Conference, Anchorage, AK,
USA, 30 June5 July 2013.
[79] Gatti-Bono, C., and Perkins, N. C;
Numerical Simulations of Cable/Seabed
Interactions, J. Int. Soc. Offshore and Polar
Eng., 14(2);2004
[80] Nicoll, R. A; Dynamic Simulation of
Marine Risers with Vortex Induced
Vibrations, Masters Thesis, University of
Victoria, British Columbia, Canada; 2004.
[81] Masciola, M., Nahon, M., and Driscoll,
F., Preliminary Assessment of the
Importance of Platform Tendon Coupling in
a Tension Leg Platform, J. Offshore Mech.
Arct. Eng., 135(3), 2012.
[82] Masciola, M., Jonkman, J., Robertson,
A., Coulling, A., and Goupee, A.
Assessment of the Importance of Mooring
Dynamics on the Global Response of the
DeepCwind Floating Semisubmersible
Offshore Wind Turbine, 23rd International
Offshore and Polar Engineering (ISOPE)
International Journal of Engineering Technology and Scientific Innovation
ISSN: 2456-1851
Volume:03, Issue:05 "September-October 2018"
www.ijetsi.org Copyright © IJETSI 2018, All rights reserved Page 231
Conference, Anchorage, AK, June 30 July
2013.
[83] R. Chiou, PhD thesis: Nonlinear
Hydrodynamic Response of Curved Singly
Connected cable., Oregon State University,
2004
[84] Chai Y. Varyani K. and Barltrop N.
Semi-analytical Quasi-Static Formulation
for three Dimensional Partially Grounded
Mooring System Problems, Ocean Eng., 29,
pp. 627649, 2002.
[85] Buckham B. Driscoll F. R. and Nahon
M. Development of a Finite Element Cable
Model for Use in Low-Tension Dynamics
Simulation J. Applied Mech., 71(4), pp.
476485. 2004.
[86] Dalane, J. I., Fatigue Reliability
Measured Response of the Heidrun TLP
Tethers, Marine Structures pp. 611628;
1997.
[87] Buckham B. Nahon M. Seto M. Zhao
X. and Lambert C. Dynamic of a Towed
Underwater Vehicle System: Part 1: Model
Development Ocean Eng., 30(4), pp.
453470. 2003
[88] Powell, G., and Simons, J., Improved
Iteration Strategy for Nonlinear Structures
Journal of. Numerical Methods 1981.
[89] Lambert C. Nahon M. and Chalmers D.
2007 Implementation of an Aerial
Positioning System with Cable Control
IEEE/ASME Transactions on Mechatronics,
12(1), pp. 3240.
[90] Nahon M. 1999 Dynamics and Control
of a Novel Radio Telescope Antenna AIAA
Modeling and Simulation Technologies
Conference and Exhibit, pp. 214222.
[91] Williams P. Trivaila P. 2007 Dynamics
of Circularly Towered Cable Systems, Part
1: Optimal Configurations and their
Stability J. Guidance, Control and
Dynamics, 30(2), pp. 753765
[92] Walton, T. S. and Polacheck, H.,
Calculation of Transient Motion of
Submerged Cables, Mathematics of
Computation, Vol. 14, No. 69, 1960, pp. 27-
46.
[93] Hicks, J. B. and Clark, L. G., On the
Dynamic Response of Buoy-Supported
Cables and Pipes to Currents and Waves,
Offshore Technology Conference, Vol.
OTC-1556, 1972, pp. 453-462
[94] Nath, J. H. and Felix, M. P., Dynamics
of a Single Point Mooring in Deep Water,
ASCE Journal of Water Ways, Harbour and
Coastal Engineering Division, Vol. 96,
1970, pp. 815-833.
[95] Merchant, H. C. and Kelf, M. A. Non-
Linear Analysis of Submerged Ocean Buoy
Systems, Proceedings of MTS/IEEE
OCEANS 73, Vol. 1, 1973, pp. 390-395.
[96] Kelf, M. A. and Merchant, H. C.
Analysis of a Multiple Buoy Instrument
Platform; A Non-Linear Model Proceedings
of MTS/IEEE OCEANS 74, Vol.1, 1974,
(pp.44-48)
International Journal of Engineering Technology and Scientific Innovation
ISSN: 2456-1851
Volume:03, Issue:05 "September-October 2018"
www.ijetsi.org Copyright © IJETSI 2018, All rights reserved Page 232
[97] Matsubara, Y., Hideaki, N., and Hirao,
A.Dynamic Behaviour of the Submerged
Buoy-Cable System by Ocean Waves
Coastal Engineering in Japan, Vol. 28,
1985, (pp. 235-241.)
[98] Khan, N. U. and Ansari, K. A. On the
Dynamics of a Multicomponent Mooring
Line, Computers and Structures, Vol. 22,
No. 3, 1986, pp. 311-334.
[99] Herbich, J. B. and Ansari, K. A.
Developments in Offshore Engineering.
Wave Phenomena and Offshore Topics, Gulf
Publishing Co.: Houston, TX, 1999, pp.
195- 233.
[100] B. V. . C. Barbu, A novel numerical
approach to the dynamics analysis of marine
cables, International Journal of Applied
Science and Technology, 2014
[101] Rupe R. C. and Thresher R. W. 1975,
The Anchor-Last Deployment Problem for
Inextensible Mooring Lines; Transactions of
the ASME, (74-WA), pp. 10461052.
[102] Low, Y.; Langley, R. Time and
frequency domain coupled analysis of deep-
water floating production systems. Appl.
Ocean Res. 2006, 28, 371385
[103] Van den Boom, H. Dynamic behavior
of mooring lines. In Proceedings of the
BOSS Conference, Delft, The Netherlands,
15 July 1985.
[104] Chai, Y.; Varyani, K.; Barltrop, N.
Three-dimensional Lump-Mass formulation
of a catenary riser with bending, torsion and
irregular seabed interaction effect. Ocean
Eng. 2002, 29, 15031525.
[105] Garret, D. L. Dynamic Analysis of
Slender Rods, J. Energy Resource
Technology, 104, pp. 302306, 1982.
[106] Kennedy, R. M., Crosstrack Dynamics
of a Long Cable Towed in the Ocean, IEEE
OCEANS81, Boston, MA, September 1618,
pp. 966970, 1981.
[107] Lo, A., and Leonard, J. W., Dynamic
Analysis of Underwater Cables, J.Eng.
Mechanics Division, 108(4), pp.
605621,1982.
[108] Leonard, J. W., and Nath, J. H.,
Comparison of Finite Element and Lumped
Parameter Method for Oceanic Cables, Eng.
Structures, 3(3), pp.153167, 1981.
[109] Bathe, K. J., Finite element procedure,
Englewood Cliffs, N. J. Prentice-hall, 1996.
[110] Chung, J., and Hulbert, G. M., A Time
Integration Algorithm for Structural
Dynamic with Improved Numerical
Dissipation: the Generalize Method, J. App.
Mech. (pp. 371375); 1993.
[111] Ketchman J. J. and Lou Y. K;
Application of the Finite Element Method to
Towed Cable Dynamics, Proc. MTS/IEEE
Oceans, 1975.
[112] Yang Min-Dong and Teng Bin; Static
and dynamic analysis of nonlinear finite
element, Chinese, Ocean Engineering
Society, 2010.
International Journal of Engineering Technology and Scientific Innovation
ISSN: 2456-1851
Volume:03, Issue:05 "September-October 2018"
www.ijetsi.org Copyright © IJETSI 2018, All rights reserved Page 233
[113] Ran, Z. Coupled Dynamic Analysis of
Floating Structures in Waves and Currents
Ph.D. Thesis, Texas A & M University,
College Station, TX, 2000.
[114] D. L. Garrett, Coupled Analysis of
Floating Production Systems; Ocean Eng.,
32, pp. 802816, 2005
[115] Buckham, B. J. Dynamics Modeling of
Low Tension Tethers for Submerged
Remotely Operated Vehicles Ph.D. Thesis,
University of Victoria, British Columbia,
2003.
[116] Kaczmarczyk, S., and Ostachowicz,
W. Transient Vibration Phenomena in Deep
Mine Hoisting Cables: Part 1:
Mathematical Model, Journal of Sound and
Vibration, 2003.
[117] Aamo, O.M.; Fossen, T.I. Finite
element modelling of mooring lines. Math.
Comput. Simul. 2000 , 53, 415422.
[118] Aamo, O.; Fossen, T. Finite element
modelling of moored vessels. Math. Comput.
Model. Dyn. Syst. 2001 , 7, 4775
[119] Palm, J.; Paredes, G.M.; Eskilsson, C.;
Pinto, F.T.; Bergdahl, L. Simulation of
mooring cable dynamics using a
discontinuous Galerkin method. In
Proceedings of the 5th International
Conference on Computational Methods in
Marine Engineering, Hamburg, Germany,
2931 May 2013
[120] Montano, A. Restelli, M. Sacco, R.
Numerical simulation of tethered buoy
dynamics using mixed finite elements.
Comput. Methods Appl. Mech. Eng. 2007,
196, 41174129
[121] Howell, C. T. and Triantafyllou, M.
S., Investigation of Large Amplitude
Nonlinear Dynamics of Hanging Chains,
International Journal of Offshore and Polar
Engineering, Vol. 3, No. 3, 1993, pp. 162-
167
[122] Thomas D. O. and Hearn G. E. Deep
water mooring line dynamics with emphasis
on sea-bed interference effects, Offshore
Technology Conference, OTC 7488, Vol. 3,
203 241; 1994.
[123] Huang, S., Dynamic analysis of three -
dimensional marine cables, Ocean Eng;
1994.
[124] Hover, F. S., Grosenbaugh, M. A. and
Triantafyllou, M. S., Calculation of dynamic
motions and tensions in towed underwater
cables, IEEE J. Ocean. Eng; 1994.
[125] Gobat, J., and Grosenbaugh, M., Time-
Domain Numerical Simulation of Ocean
Cable Structures, Ocean Eng., 33(10), pp.
13731400, 2006.
[126] Matulea, I. C., N stase, A., T lmaciu,
N., Sl mnoiu, G. and Goncalves Coelho, A.
M., On the equilibrium configuration of
mooring and towing cables, Appl. Ocean
Res; 2008.
[127] Chatjigeorgiou, I.; Mavrakos, S.
Assessment of bottom-cable interaction
effects on mooring line dynamics. In
International Journal of Engineering Technology and Scientific Innovation
ISSN: 2456-1851
Volume:03, Issue:05 "September-October 2018"
www.ijetsi.org Copyright © IJETSI 2018, All rights reserved Page 234
Proceedings of the 17th International
Conference on Offshore Mechanics and
Arctic Engineering, Lisbon, Portugal, 56
July 1998.
[128] Ablow, C.; Schechter, S. Numerical
simulation of undersea cable dynamics.
Ocean Eng. 1983, 10, 443457.
[129] Howell, C.T. Investigation of the
Dynamics of Low-Tension Cables.
Ph.D.Thesis, Woods Hole Oceanographic
Institution, Massachusetts Institute of
Technology, Cambridge, MA, USA, 1992.
[130] Chatjigeorgiou, I.K. A finite
differences formulation for the linear and
nonlinear dynamics of 2D catenary risers.
Ocean Eng. 2008, 35, 616636.
[131] Winget, J.; Huston, R. Cable
dynamics, A finite segment approach.
Comput. Struct. 1976, 6, 475480.
[132] Kamman, J.W.; Huston, R.L.
Modelling of submerged cable dynamics.
Comput. Struct. 1985, 20, 623629.
[133] Nichol, T.; DuBuque, G.; Fabien, B.;
Dynamic Modelling of Compliant-Moored
Submerged Systems with Applications to
Marine Energy Converters. In Proceedings
of the 2nd Marine Energy Technology
Symposium, Seattle, WA, USA, 1517 April
2014.
[134] Filipich, C.; Rosales, M. Dynamic
Analysis of plane mooring chains of
inextensible links. Mec. Comput. 2007 , 26,
24792495.
[135] Josh Davidson and John V. Ringwood
Mathematical Modelling of Mooring
Systems for Wave Energy Converters. A
Review, Centre for Ocean Energy Research,
Maynooth University, 2017.
[136] DNV-OS-E301 Offshore Standard,
DNV GL, 2013.
[137] Saidee, M.H. Fatigue Analysis and
Design of Mooring Systems. Assessment and
Comparison of Different Methods. Masters
Thesis, NTNU, Trondheim, Norway, 2015.
[138] Low, Y.M.; Cheung, S.H. On the
long-term fatigue assessment of mooring
and riser systems. Ocean Eng.2012, 53,
6071
[139] Thies, P.R.; Johanning, L.; Smith,
G.H. Lifecycle fatigue load spectrum
estimation for mooring lines of a floating
marine energy converter. In Proceedings of
the ASME 2012 31st International
Conference on Ocean, Offshore and Arctic
Engineering, Rio de Janeiro, Brazil, 16 July
2012; pp.667676.
[140] Thies, P.R.; Johanning, L.; Harnois,
V.; Smith, H.C.; Parish, D.N. Mooring line
fatigue damage evaluation for floating
marine energy converters: Field
measurements and prediction. Renew.
Energy 2014, 63, 133144.
[141] Christiansen, N.H.; Voie, P.E.T.;
Hgsberg, J.; Sdahl, N. Efficient mooring line
fatigue analysis using a hybrid method time
domain simulation scheme. In Proceedings
of the ASME 2013 32nd International
International Journal of Engineering Technology and Scientific Innovation
ISSN: 2456-1851
Volume:03, Issue:05 "September-October 2018"
www.ijetsi.org Copyright © IJETSI 2018, All rights reserved Page 235
Conference on Ocean, Offshore and Arctic
Engineering, Nantes, France, 914 June 2013;
p.V001T01A035.
[142] Harnois, V. Analysis of Highly
Dynamic Mooring Systems: Peak Mooring
Loads in Realistic Sea Conditions. Ph.D.
Thesis, University of Exeter, Exeter, UK,
2014
[143] Savin, A.; Svensson, O.; Leijon, M.
Azimuth-inclination angles and snatch load
on a tight mooring system. Ocean Eng.
2012, 40, 4049
[144] Palm, J.; Eskilsson, C.; Bergdahl, L.
Mooring cable simulations with snap load
capturing for wave energy applications. In
Proceedings of the 2nd International
Conference on Renewable Energies
Offshore, Lisbon, Portugal, 2428 October
2016
[145] ISO 19901-7: Specific Requirements
for Offshore Structures, Petroleum and
Natural Gas Industries, 2013.
[146] Singh, N. Systems Approach to
Computer-Integrated Design and
Manufacturing. Wiley, New York, 1996.
[147] Su YH, Yang JM, Xiao LF, Li X.
Multi-objective optimization design of
truncated mooring system based on
equivalent static characteristics. China
Offshore Platform. 23(1):14 19, 2008.
[148] Michalewicz Z. Genetic algorithms +
data structures = evolution programs. New
York (NY): Springer-Verlag, 1994.
[149] Michalewicz, Z., Schoenauer, M.,
Evolutionary computation for constrained
parameter optimization problems.
Evolutionary Computation 4 (1), 132. 1996.
[150] Lagaros N.D., Papadrakakis M.,
Kokossalakis G. Structural optimization
using evolutionary algorithms. Computers
and Structures 80, 539571, 2002.
[151] Tianhui Fan, Dongsheng Qiao &
Jinping Ou; Innovative approach to design
truncated mooring system based on static
and damping equivalent; Ships and Offshore
Structures/ Francis taylor, 2014.
[152] Tianhui Fan, Dongsheng Qiao, Jun
Yan, Chaohe Chen & Jinping Ou
Experimental verification of a semi-
submersible platform with truncated
mooring system based on static and
damping equivalence ,Ships and Offshore
Structures , 2017.