Three-Dimensional Computations of Water-Air Flow in a Bottom Spillway During Gate Opening
Transcript of Three-Dimensional Computations of Water-Air Flow in a Bottom Spillway During Gate Opening
Engineering Applications of Computational Fluid Mechanics Vol. 8 No. 1, pp. 104–115 (2014)
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THREE-DIMENSIONAL COMPUTATIONS OF WATER–AIR FLOW IN A
BOTTOM SPILLWAY DURING GATE OPENING
Ting Liu *
† and James Yang *
#
*Hydraulic Engineering, Royal Institute of Technology (KTH), SE-100 44, Stockholm, Sweden #Vattenfall Research and Development (R&D), SE-814 26, Ä lvkarleby, Sweden
†E-Mail: [email protected] (Corresponding Author)
ABSTRACT: Undesired entrainment of air in a bottom spillway often leads to problems in both safety and
operational functions. A numerical analysis of a transient process of air entrainment into bottom spillway flows
when a spillway gate is opened was conducted in this study. The Volume of Fluid (VOF) model was used. The 3D
computational domain consisted of a spillway conduit, a moving bulkhead gate, a gate shaft, an upstream reservoir
and a downstream outlet. The large number of cells, together with the dynamic mesh modelling of the moving gate,
required substantial computational resources, which necessitated parallel computing on a mainframe computer. The
simulations captured the changes in the flow patterns and predicted the amount of air entrainment in the gate shaft
and the detrainment downstream, which help in the understanding of the system behaviour during opening of the
spillway gate. The initial conduit water level and the gate opening procedure affect the degree of air entrainment in
the gate shaft. To release the undesired air, a de-aeration chamber with a tube leading to the atmosphere was added
to the conduit. Despite the incomplete air release, the de-aeration chamber was found to be effective in reducing
water surface fluctuations in the downstream outlet.
Keywords: bottom spillway, moving gate, air entrainment, two-phase flow, CFD
1. INTRODUCTION
A bottom spillway can be designed for such
purposes as flood discharge during dam
construction, emptying of a reservoir, or removal
of sediment. Though less frequently used than a
surface-type spillway, a bottom spillway must be
properly maintained to guarantee that it will
function as expected when needed. In a survey of
38 bottom spillways in Sweden, operational
problems were observed in nine. Eight of these
problems were caused by entrained air, which
mainly occurred during gate opening. For reasons
of both structural safety and personnel security,
many of these spillways are no longer in use
(Dath and Mathiesen, 2007).
A typical layout of a bottom spillway consists of a
gate (bulk head or radial), a gate shaft and a
conduit leading downstream. When the water
from the gate plunges into the gate shaft, air
becomes entrained in the water. The air
entrainment starts when a turbulent flow regime
develops and the energy of the surface eddies is
greater than the energy content of the surface
tension (Ferrando and Rico, 2002). Air pockets
and bubbles are entrained at the interface and
trapped at discontinuities between the impinging
jet flow and the receiving water body (Chanson,
2008). At the plunge location, the air entrainment
is caused by surface disturbance due to the jet, the
air boundary layer or the free surface shear layer
(Ervine, 1998).
Some general-purpose empirical formulas are
available to determine the amount of air
entrainment associated with different
mechanisms. Ervine (1998) showed that the
maximum aeration rate per unit jet width was a
function of the jet velocity and could be expressed
as a simple polynomial with factors for
consideration of all of the mechanisms. However,
it is difficult to determine which of the
mechanisms is relevant and to determine some of
the constants in the formulas (Khatsuria, 2005).
Due to the complexity of the problem, which also
depends on site-specific details, numerical
modelling and experiments are often essential in
understanding the air entrainment process and
considering it in design.
For two-phase flows, the geometry of the flow
field or the distribution of the phases commonly
refers to flow patterns or flow regimes, mainly
depending on the flow rates of the fluids. The
Baker chart is one of the flow pattern maps often
used to determine the flow regime and predict the
transitions between the flow patterns. Fig. 1
shows various flow patterns in a horizontal pipe
(Baker, 1954). Among these flow patterns, the
degree of destructivity to the structure increases
from annular and bubbly flow to stratified flow
and further to slug and plug flow (Rahimi, 2010).
Received: 10 Jun. 2013; Revised: 24 Sep. 2013; Accepted: 11 Nov. 2013
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When the entrained air in a bottom spillway forms
air pockets, a plug or slug flow pattern often
develops. When moving liquid slugs suddenly
encounter obstructions such as valves and pipe
bends, shock loads are generated (Thorley, 1991).
Enclosed air pockets in a pipe flow can cause pipe
vibrations, blowout, blowback and even a risk of
cavitation.
Fig. 1 Two-phase flow patterns in horizontal pipes
(Baker, 1954).
A de-aeration device is often installed to prevent
air-related problems in bottom spillways. Such a
device is usually located immediately
downstream of the gate shaft to remove undesired
air from the system at an early stage. A typical
de-aeration device, consisting of a de-aeration
chamber and a vertical vent tube leading to the
atmosphere, is typically suggested. According to
Sigg et al. (2004), this type of device offers high
de-aeration efficiency for horizontal or nearly
horizontal conduits. Its function is normally tested
through scaled experiments prior to its installation
in the prototype.
As an option to costly prototype tests and
laboratory experiments that suffer from scale
effects with respect to air entrainment,
computational fluid dynamics (CFD) simulations
lead to both qualitatively and quantitatively
reasonable results. Many mathematical models
have been developed to simulate multiphase flows
in diversified engineering applications. The VOF
model, an Eulerian–Eulerian approach, is suitable
for simulating two or more immiscible fluids and
interface tracking, e.g., water–air flows with free
surface or under pressurised condition (Haun et
al., 2011; De Schepper et al., 2008). In this
approach, the water–air flow is best represented
as a continuous medium, which is the situation in
a bottom spillway.
The finite volume code FLUENT has been
validated for simulations of multiphase and
turbulence flow problems. De Schepper et al.
(2008) successfully used FLUENT to simulate
flow regimes predicted by the Baker chart. Baylar
et al. (2009) employed FLUENT to model the air
injection rate of Venturi flows and achieved good
agreement with experimental results. With
FLUENT, Liu and Yang (2011) modelled air
pocket transport in pipe flows. Politano and
Carrica (2007) and Politano and Arenas (2011)
adopted the software to compute dissolved gas
dynamics downstream of a dam.
Some previous numerical studies of flow in
bottom spillways have focused on only part of the
waterway or steady-state solutions or have been
performed in 2D (Dargahi, 2010; Hong et al.,
2011; Haun et al., 2011; Liu and Yang, 2011). To
examine the overall behaviour of a bottom
spillway when its gate opens, it is essential to
carry out transient simulations in three
dimensions.
In this study, numerical simulations were
conducted to examine a process of air entrainment
and detrainment following the opening of the
spillway gate. The purpose of this study was to
gain insight into the air flow behaviour in the
bottom spillway that would be of use in managing
its operation. The issues discussed include the
characteristics of the two-phase water–air flow
and the influences of contributing factors, such as
the initial water level in the conduit and the gate
opening procedure. This study also included an
examination of the function and efficiency of a
de-aeration chamber.
2. BOTTOM SPILLWAY OF LETAFORS
DAM
The Letafors Dam, located in the municipality of
Torsby in Sweden, is an earth-fill dam with a
maximum structural height of 25m. The full
reservoir water-stage elevation (FRWS) is
+349m. The reservoir has a regulated water depth
of H = 19.1m. There is one surface spillway and
one bottom spillway. The bottom spillway, which
lies below the dam, includes a bulkhead gate, a
gate shaft, a horizontal conduit and a downstream
outlet (Fig. 2).
The discharge of the bottom spillway is controlled
by the bulkhead gate, which has a width of 3.05m
and a maximum opening hmax of 5m. The height
of the gate opening is the gap between the lower
edge of the gate and the reservoir bottom, denoted
by hg. The ordinary gate opening velocity is vg =
1cm/s. The gate shaft, which is open to the
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+349.00
+329.90
+320.95
+328.90
Letten Lake
Gate shaft
Letafors
Dam
Fence
Retaining wallOutlet
Half-filled
Inital water level:
Fully-filled
Empty
Fig. 2 Bottom spillway of Letafors Dam.
Fig. 3 Blowout at downstream outlet in prototype test.
Air inlet:
Pressure inlet
( P = 0)
Downstream outlet:
Pressure outlet
( P = 0)
Flow
Moving
gate
Wall
Water inlet:
Pressure inlet
( H =19.1 m)
M NCentreline of gate shaft
B C DA
ff
2.55m1.275m
Half-filled9.225m
25m 50m 25m 4m
Initial water level:
Fully filled
Fig. 4 Computational domain and boundary conditions of numerical model.
(a)
(c) (d)
(b)
Fig. 5 3D views of grid showing regions: (a) around gate, (b) at downstream outlet without de-aeration device, (c) at
downstream outlet with de-aeration device and (d) of de-aeration chamber with vertical tube.
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Fig. 6 Mass imbalance in conduit for mesh with
varying sizes for t = 5–15s.
Fig. 7 Dynamic layering method for modelling of gate
opening: (a) initial height of first-layer cell, (b)
cell height increasing with time and (c) cell
splitting into two layers.
Fig. 8 Water flow through gate and flow into river as
function of gate opening.
Table 1 Description of the scenarios modelled.
Air entrainment
scenario Gate opening
VOF
discretisation
scheme
Initial water
level
in conduit
Without de-
aeration device
Continuous
Explicit Half full
Implicit
Empty
Half full
Full
Instantaneous Explicit Full
With de-aeration
device Continuous Implicit Half full
x=40m x=50m
stratified flow
plug flow
bubbly flow
(e)
(f)
(g)
Fig. 9 Contours of air volume fraction in bottom
spillway at gate opening velocity of 1 cm/s.
Water released from the reservoir causes mixing
and air entrainment in the gate shaft, with free
orifice flow at (a) t = 15s and (b) t = 35s and for
submerged conditions at (c) t = 85s and (d) t =
105s, corresponding to gate shaft water levels of
6.29 and 8.27m, respectively, above the
reservoir bottom. The flow pattern in the
conduit undergoes a change from stratified flow
at (e) t = 65s to plug flow at (f) t = 70s to bubbly
flow at (g) t = 75s. In the lower part, air
discharges from the downstream outlet at (h) t =
25s, (i) t = 55s and (j) t = 75s.
(c)
(d)
(h)
(i)
(j)
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atmosphere, is located immediately downstream
from the bulkhead gate. The conduit, which has a
circular cross section, has a diameter of 2.55m
and a length of 104m. Its bottom elevation is
30.6m below the FRWS. The gate shaft connects
to the horizontal conduit through a 90-degree
bend. The bottom of the river is 20.1m below the
FRWS.
During the opening of the gate, a blowout was
observed to occur due to entrained air that was
released downstream (Fig. 3). At the time, no de-
aeration structure existed in the prototype
spillway.
3. NUMERICAL MODELING
A numerical model was set up to simulate the
water–air flow in the bottom spillway of the
Letafors Dam during the gate opening. The VOF
model, combined with the k–ε turbulence model,
was used. It was assumed that mass transfer does
not occur between the air and water, which is
usually a valid assumption as air entrainment
from the gate shaft is mainly caused by turbulent
mixing and pressure reduction. The amount of
entrained air in the flow is dominant, while the
amount of dissolved air is negligible. The
entrained air in the conduit tends to accumulate at
the top of the conduit, forming air pockets.
3.1 VOF model
In the VOF model, all of the phases share a single
momentum equation and velocity field. In each
control volume, the fluid properties are
determined by the presence of the component
phases, i.e., the properties of the mixture in each
control volume. A control volume is filled with
air, water or a mixture of the two; no void volume
is allowed. The momentum equation is written as
Fguupuuut
T
)()(
where αa is air volume fraction in a control
volume, αw is water volume fraction, ρ and µ are
mixture density and viscosity, respectively, ρ =
αaρa + (1 – αa)ρw, μ = (αaρaμa + αwρwμw)/ρ, ρw is
water density, ρa is air density, u
is velocity
vector, t is time, p is static pressure, g is
acceleration of gravity and F is volumetric force
at the interface resulting from the surface tension.
The VOF model is a direct solution for the motion
of the two phases that does not track the moving
boundary of the interface (ANSYS Inc., 2011).
The volume fraction of air is obtained by solving
its continuity equation, written as
0)()(
u
ta
(2)
The volume fraction of water is calculated as
αw = 1 – αa (3) The VOF equations are time-discretised using
either an implicit or an explicit scheme. The explicit scheme is only used to compute a time-
dependent solution, whereas the implicit scheme is used for both time-dependent and steady-state
solutions. To improve convergence and allow large time
steps, the implicit scheme is used, rather than the
explicit scheme, to discretise the VOF equations (Chau and Jiang, 2001 and 2004). Simulations are
performed to examine the difference between the two schemes and also to confirm that the implicit
VOF yields sufficiently high accuracy. With the volume fraction of each phase calculated
in each computational cell, the geometry of the interface is configured through the interface
reconstruction method (ANSYS, 2011). In the explicit VOF, the water–air interface is calculated
using a piecewise linear interface calculation (PLIC) procedure, the so-called Geo-reconstruct
routine in FLUENT (De Schepper et al., 2008). This procedure has the highest accuracy of the
interface reconstruction techniques available in the code. A second-order reconstruction scheme
(the Compressive routine) is used for the implicit
VOF. The interface is almost as sharp as the solution from the PLIC method.
3.2 Numerical solver
The equations are solved using an unsteady solver. The code uses a second-order upwind
scheme and the PISO pressure–velocity coupling routine. For the interface computations, Geo-
Reconstruct is used for the explicit VOF and Compressive is used for the implicit VOF.
3.3 Simulations
3.3.1 Geometry and grid
The reservoir in the model is limited to an area of
50m×50m. The gate is centrally located at the downstream boundary of the reservoir. Fig. 4
displays the cross-sectional profile of the 3D computational domain (here without the de-
aeration device). Due to its irregular geometry, the downstream outlet in the river is somewhat
simplified and treated as a rectangular pool. When
pressurised, air pockets attach to the top of the conduit and are discharged close to the upper
(1)
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vertical boundary of the pool. The simplification
of the lower boundary might have some slight effect on the air flow. Our intention is that, with
the data from the Letafors Dam and the generalisation of the outlet geometry, the blowout
behaviour can be used as a reference to illustrate other similar outlets. A de-aeration chamber was added to the conduit in the model to demonstrate its effectiveness in mitigating the blowout in the prototype. The de-aeration chamber is situated 92m downstream of the gate shaft, at an existing hole in the prototype. Based on Wickenhäuser and Minor’s (2008) recommendations for the minimum dimensions of a de-aeration chamber, the height, length and width were set to 28%, 27% and 50% of the conduit diameter, respectively. The chamber length must be optimised because an excessively long chamber could exert an unfavourable influence on the flow. The vertical tube connecting the chamber to the atmosphere has a diameter of 0.3m. Fig. 5 shows a 3D view of a typical grid for
simulations with and without a de-aeration
device. The domain is discretised using a multi-block grid with hexahedral cells. The typical
mesh sizes are between 6×106 and 8×10
6 cells for
the cases of air entrainment and de-aeration. The
grids are refined near the solid boundaries, near the gate opening and near the de-aeration
chamber, where large velocity gradients are expected. In the conduit, the height of the first
layer mesh is 1.3cm, i.e., 0.5% of the conduit diameter. The maximum skewness of the mesh is
0.65. The ordinary mesh, with n = 6×10
6 cells, is
denoted by G. To show grid independence, a fine mesh G1 and a coarse mesh G2 were generated,
with n = 9×106 and 3×10
6 cells, respectively. The
mass imbalance ηm in the conduit refers to the net
flux through the conduit, i.e., the difference
between the flow rates at cross sections M and N,
ηm = (QM – QN)/QM·100% (4)
Fig. 6 shows the change in ŋm with time. The
value of ŋm falls below 0.2% when the solutions
for meshes G0 and G1 converge to 15s. The mass
conservation is best achieved with mesh G1. The
change in the net mass flux with time is almost
the same for G0 as for G1, implying that the
overall mass balance in the conduit is achieved
and that the solution for the ordinary mesh G0 is
grid-independent.
3.3.2 Boundary conditions
The symmetry boundary condition applies to the
central plane of the computational domain so that
only half of the geometry is simulated. The
hydrostatic pressure boundary applies to the
upstream end of the reservoir (Fig. 4). It is
implemented by means of a user-defined function
(UDF) in which the hydrostatic pressure p(z) at a
water depth of z is defined as
p(z) = (ρw – ρa)gz (5)
The gate shaft is open to the atmosphere and
serves as an air inlet, allowing air to flow freely in
and out. The same boundary condition applies to
the downstream outlet and to the de-aeration tube
in the de-aeration simulation. The remaining
boundaries are treated as walls.
3.3.3 Modelling moving gate
A dynamic mesh is created to model the upward
gate movement, and a dynamic layering method is
used to avoid mesh distortion.
The domain of the gate opening, i.e., the volume
connecting the upstream reservoir and the gate
shaft, is defined as the dynamic zone. The lower
edge of the bulkhead gate, moving vertically
upwards, is treated as a rigid body. The layering
method is activated for the dynamic zone, where
new layers of mesh are added following the lower
gate edge. A ‘profile’ text file of the gate opening
velocity specifies its moving velocity, which is
constant in this case. The cell height in the
dynamic zone is specified as hmin = 0.05m. A
close-up view of the mesh in the rectangular box
in Fig. 5a is shown in Fig. 7. Figs. 7a−b show the
growth of the dynamic zone with time. A split
factor of αs = 0.4 is used, indicating that the cell
adjacent to the rigid body splits into two layers of
cells when the cell height is larger than (1+ αs)hmin
(Fig. 7c).
3.3.4 Computations
The transient process of air entrainment and de-
aeration in the bottom spillway is calculated for
two gate opening scenarios, i.e., continuous
opening at a constant velocity and instantaneous
opening to a designated position. For the former
scenario, the gate, with a prescribed initial
opening of hini = 5cm, opens at a constant velocity
vg. The gate opening height at time t is hg = hini +
vgt. For the latter scenario, the gate opens
instantaneously from the closed position to a
designated opening height h.
In practical situations, the conduit may be dry or
partially full after maintenance. For this reason,
different initial water levels in the conduit are
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modelled to demonstrate their influences on air
entrainment (Fig. 4).
The implicit and explicit VOF models were
applied to compare the two. Simulations were
performed for the existing bottom spillway layout
without the de-aeration structure. The time step
was 0.001s for the continuous gate opening and
0.005s for the instantaneous opening. The
modelled scenarios are summarised in Table 1.
Parallel computing was performed on a
mainframe computer with 4–8 CPUs. The
residual values of the mass, velocity and volume
fraction were the convergence criteria. A
simulation was considered to have converged to a
solution when the scaled residuals were lowered
by at least three orders of magnitude.
4. RESULTS AND DISCUSSIONS
4.1 Gate opening at constant velocity
In this scenario, the bulkhead gate is opened at a
velocity of 1cm/s up to a height of 1.8m.
Considering that air entrainment ceases when the
gate becomes submerged in the gate shaft, full
gate opening is not necessary.
4.1.1 Water–air flow
The initial water depth in the conduit is 1.275m,
half of the conduit diameter. As the gate opening
increases, the water flow rate from the gate
increases (Fig. 8). The water outflow rate into the
river is zero at the beginning of the simulation.
When the water level at the downstream outlet is
higher than the riverbed elevation, the water starts
to run into the river. The outflow rate undergoes a
sudden increase at hg ≈ 0.85m. For gate openings
hg = 1–1.8m, the water level in the gate shaft
increases, and the water flow through the gate is
greater than the outflow into the river.
At each time step, the dynamic mesh due to the
gate movement is updated automatically. The
step-by-step gate opening gives rise to small
pressure perturbations in the reservoir, which in
turn affects the gate discharge. This explains the
somewhat ‘wavy’ shape of the calculated water
flow rate from the gate.
The simulated flow rate through the gate is
compared with empirical results. The points in
Fig. 8 correspond to the discharge through a
rectangular orifice under free and subsequently
submerged conditions, as determined by the
formula
hgCbhQ g 2 (6)
where Q is flow rate, C is discharge
coefficient, b is gate width, ∆h is difference in
elevation between the reservoir water surface
and the water surface at the centreline of the
gate opening, for free-orifice flow, or
between the reservoir water surface and the
gate shaft water stage for submerged
conditions. The comparison indicates a good
agreement up to a gate opening of 1.1m;
thereafter, the simulated flow rate is slightly
higher than that indicated by the empirical
results. The discrepancy is most likely due to
the assumption of a constant discharge
coefficient in the empirical formula, which
should increase with the gate opening. This
coefficient is also affected when the discharge
from the opening undergoes a change from
the free to the submerged outflows. Figs. 9a-d show the air volume fraction in the
upper part of the bottom spillway, from 5m
upstream to 35m downstream of the gate shaft
centreline. The water jet hits the wall of the gate
shaft and plunges into the pool of water (Fig. 9a).
Air is entrained into the bottom spillway mainly
by the turbulent mixing in the gate shaft. Once the
downstream water level at the outlet becomes
higher than the conduit top, the initially filled air
in the conduit becomes trapped as well. The
entrained air from the gate shaft, together with the
trapped air, accumulates under the conduit roof,
forming air pockets in the bottom spillway (Fig.
9b). Once the gate opening becomes submerged,
little air is entrained into the bottom spillway
(Figs. 9c-d).
During the filling of the conduit, the flow pattern
in the middle of the conduit 40–50m downstream
of the gate shaft undergoes a change from
stratified flow (Fig. 9e) to plug flow (Fig. 9f) and
then to bubbly flow (Fig. 9g). The flow pattern
transition that occurs as the rate of water flow
increases during the gate opening agrees
qualitatively with that predicted by the Baker
chart (Baker, 1954).
Figs. 9h-j show the results for the lower part of
the conduit. In the outlet region, air pockets
escape from the water body. In the meantime, the
released air pockets blow up the water surface
immediately downstream of the conduit (Fig. 9h).
When the resulting air pocket penetrates into the
downstream water body, the next blowout is
prepared (Fig. 9i). The blowout height depends on
the air pocket size. As the air flow rate decreases,
the entrained air is discharged in the form of
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small air pockets, resulting in small water surface
fluctuations (Fig. 9j).
Two cross sections in the conduit, at distances of
2.55 and 103.9m from the centreline of the gate
shaft, are denoted by M and N, respectively (Fig.
4). The air flow through cross section M, i.e., air
flow into the conduit, is the entrained air from the
gate shaft. When the gate opening reaches
0.605m, the air entrainment slows down. When
the gate opening reaches 1.088m, the air inflow
drops to almost zero (Fig. 10). The air flow
through cross section N, i.e., the air outflow,
consists of the entrained air and the initially filled
air. When the opening is between 0.605 and
1.088m, spikes occur in the air outflow, which
suggests that air is present in the form of air
pockets.
The simulated results for air entrainment shown
in Fig. 10 are similar to the air flow conditions
observed at a Morning Glory spillway intake
(Khatsuria, 2005). As shown in Fig. 11, the air
inflow rate through the intake increases in Region
I, decreases to zero in Region II when the air
passage at the lower end is sealed by water and
remains zero in Region III for a submerged
discharge. The air flow rates in Regions I, II and
III correspond to the air entrainment for gate
openings of less than 0.605m, between 0. 605m
and 1.088m and more than 1.088m, respectively.
4.1.2 Air pocket release downstream
The flow in the conduit exhibits a plug flow
pattern when a series of air pockets is built up
(Fig. 9f). The air pockets are carried with the flow
and then escape downstream of the conduit,
blowing up the water surface locally (Fig. 9h).
The downstream water level, i.e., the water level
in the middle of the rectangular pool, keeps rising
until it is higher than the river bed elevation. The
blowout height corresponds to an air volume
fraction of 0.5. The water surface fluctuation
corresponds to the blowout height at the wall
above the downstream water level. The release of
an air pocket corresponds to one spike of the
fluctuations in Fig. 12, the size of which can be as
large as 4.54m. The frequency of occurrence is
approximately 6s during the interval t = 40–70s.
After t = 70s, the air outflow continues and
generates an average rise in the water surface of
0.69m. Blowouts were observed and documented
during the opening of the prototype bottom
spillway.
As shown in the 2nd
and 4th pictures in Fig. 3, two
of the highest consecutive blowouts following the
start of the gate movement had approximate
heights of 2.5 and 4.5m, respectively. The
corresponding heights predicted by the simulation
were 2.96 and 4.81m, respectively, at positions in
the blowout where the air content is 90%. At the
locations with air contents of 99%, the heights are
only 0.1–0.2m greater. The opening procedure in
the prototype test was not precisely defined;
presumably, the gate was opened at a constant
velocity as in the numerical model. As the air
pocket size is the dominant factor in this context,
the comparable blowout heights indicate that the
prototype tests and the CFD model generate air
pockets of similar dimensions up to a gate
opening of 1.8m.
The pressure fluctuations in the conduit are
mainly the combined result of the water level rise
in the gate shaft, entrained air and air pocket
release downstream. The pressure fluctuations at
four points along the top of the conduit, A, B, C
and D, are shown in Fig. 13, at distances of 2.55,
25, 75 and 100m from the gate shaft centreline
(Fig. 4), respectively. The transient pressures are
recorded every 0.2s during the gate opening. The
pressure at point A is lower than that at point B,
and the pressure drop is caused by the 90-degree
bend. The amplitudes of the pressure oscillations
above the mean pressure are ≈104Pa for points B,
C and D and ≈2×104Pa for point A during the
filling of the conduit. The oscillations at point A
are larger than those at the other points.
4.1.3 Implicit VOF
For the same mesh grid used in this study, the
implicit VOF requires approximately 25% of the
computational time that the explicit VOF
requires. The use of the implicit VOF improves
the convergence, and the calculations are
performed more efficiently. The air flow rate, a
parameter of interest, is chosen for comparison of
the two methods.
For the implicit and explicit VOF, Fig. 14 shows
the total air flow passing through the air inlet of
the gate shaft and the flow through the
downstream outlet. A larger difference exists for
the air inlet than for the downstream outlet. The
peak values of the air flow rates also differ. The
implicit VOF results in maximum differences of
79% and 28% in the air flow rate through the gate
shaft and the downstream outlet, respectively.
There is also a phase shift in time: the time to the
peak is shifted by approximately 2s for the gate
shaft air inlet and 8s for the downstream outlet.
The accuracy of the previously mentioned
polynomial given by Ervine (1998) for calculating
the maximum aeration rate is likely to be ±30%
Engineering Applications of Computational Fluid Mechanics Vol. 8, No. 1 (2014)
112
(Khatsuria, 2005). Hence, the implicit VOF gives
reasonable results with acceptable accuracy,
especially with respect to the air flow through the
downstream outlet and the peak values of air
flow.
Fig. 10 Air flow rate through upstream and
downstream ends of conduit versus gate
opening.
Reservoir level
Air
dis
char
ge
Region I Region II Region III
Air discharge Air passage at
lower end sealed
Submerged discharge
Fig. 11 Air discharge versus reservoir level of Morning
Glory intake (Khatsuria, 2005).
Fig. 12 Water surface fluctuations in downstream
outlet caused by release of air pockets for t =
40–100s.
Fig. 13 Transient pressure along the top of conduit
during gate opening.
Fig. 14 Air flow rate for (a) inflow through gate shaft
and (b) outflow through downstream outlet,
using implicit and explicit VOF.
Fig. 15 Entrained air flow rate versus gate opening for
initially full, half-filled and empty conduit.
Fig. 16 Entrained air flow rate for t = 0–40s for
instantaneous gate opening ratios β of 10%,
20%, 30%, 40% and 50%.
Fig. 17 Air flow rate in the bottom spillway with a de-
aeration device during gate opening.
4.1.4 Initial water level in conduit
The initial water level in the conduit affects the
amount of air entrainment. Therefore, three initial
conduit water levels were simulated to
quantitatively evaluate this effect. Initial water
Engineering Applications of Computational Fluid Mechanics Vol. 8, No. 1 (2014)
113
heads of 0, 1.275 and 10.5m, measured from the
conduit bottom and corresponding to an empty, a
half-filled and a fully filled conduit, respectively,
were simulated.
As Fig. 15 shows, the amount of air entrained
during the gate opening is the greatest for the
initially empty conduit and slightly lower for the
initially half-filled conduit. For the fully filled
conduit, a limited amount of air is entrained into
the conduit. When the gate opening is larger than
0.4m, little air entrainment is detected, which
indicates that a submerged conduit can effectively
reduce air entrainment during the gate opening.
Fig. 18 Water surface fluctuations downstream with
and without a de-aeration device for t = 40–
120 s.
Fig. 19 Transient pressure along the top of the conduit
during gate opening with a de-aeration device
installed between Points C and D.
4.2 Instantaneous gate opening
Five instantaneous gate opening cases, in which
the gate opens instantaneously from a closed
position to a designated position, were simulated
for the initially fully filled conduit. The flow in
the conduit was calculated until a steady-state
flow condition was reached, i.e., up to t = 40s.
The opening ratio β was defined as β = hg/hmax.
The instantaneous gate opening cases were
hypothetical scenarios. The air entrainment into
the conduit during gate opening varies with the
opening ratio (Fig. 16). For a larger opening ratio
(β), more air is entrained into the conduit; the
process is more intense at the beginning and
terminates earlier. In order words, the larger the
gate opening is, the more air is entrained into the
bottom spillway, because of the higher flow rate
and more intense mixing in the gate shaft. If a
blowout occurs, allowing a small gate opening
velocity may help improve the situation.
4.3 De-aeration
As in the situation without any de-aeration
structure, the entrained air accumulates at the top
of the conduit and forms air pockets. After the
conduit becomes submerged at hg = 0.51m, the air
in the conduit becomes trapped. Most of the
entrained air is released through the de-aeration
tube, and a small amount is carried downstream
by the flow. The largest de-aeration rate of the de-
aeration structure is 4.4m3/s (Fig. 17).
The simulation results showed that during the
filling of the bottom spillway, complete de-
aeration is not achieved because the incoming air
flow rate is higher than the value measured in the
experiment for the determination of the de-
aeration chamber layout (Wickenhäuser and
Minor, 2008). The results indicate that the
chamber dimensions needs to be larger to achieve
higher de-aeration efficiency during the gate
opening.
As Fig. 18 shows, the addition of the de-aeration
chamber mitigates the water surface fluctuations
downstream. Without the de-aeration structure,
the average water surface fluctuation is 3.23m for
10% of the highest peaks. With the de-aeration
structure, the corresponding average fluctuation is
only 0.91m.
The transient pressure change with time at points
A, B, C and D along the conduit is shown in Fig.
19. Compared with the case without de-aeration,
the magnitudes of the pressure oscillations at the
beginning of the gate operation are larger. The
reason for this is that air release from the de-
aeration structure introduces wave propagations
in the conduit and gives rise to somewhat larger
pressure fluctuations.
5. CONCLUSIONS
The flow jet plunging into the pool of the gate
shaft causes strong mixing of air and water and
leads to entrapped air in the bottom spillway
conduit, which characterises the opening process
of the spillway gate. A 3D numerical model was
set up in FLUENT for the purpose of modelling
the water–air flow in the bottom spillway with an
upward-moving bulk-head gate. A dynamic mesh
was devised to simulate the gate movement. The
VOF model was employed in combination with
the k–ε turbulence model. The simulated flow rate
through the gate agreed well with the empirical
Engineering Applications of Computational Fluid Mechanics Vol. 8, No. 1 (2014)
114
results. The documented and simulated blowout
heights at the downstream outlet were compared
and also agreed well.
During the filling of the conduit, the conduit flow
pattern evolves from stratified flow to plug flow
to bubbly flow. The transition of the flow patterns
indicates that less air is entrained through the gate
shaft as the gate opens. That is, when the water
level in the gate shaft increases and the gate
finally becomes submerged, the air entrainment
slows down and finally ceases. The initial water level in the conduit is an
important factor in the amount of air entrained.
The total amount of entrained air during the gate opening is similar for an empty and a half-filled
conduit, while a fully filled conduit results in much less air entrainment. Furthermore, a small
gate opening reduces air entrainment.
With the addition of a de-aeration chamber, most
of the entrained air can be released through the
chamber. During the early phase of the gate
opening, pressure fluctuations in the conduit are
larger because the chamber introduces
propagating pressure waves as air is released
through it. Compared with the case without any
de-aeration chamber, the height of the water
surface fluctuations downstream of the conduit
are reduced by 60–70%.
For hydropower purposes, most simulations of air
entrainment are performed with the ordinary VOF
model. The affordability of CPU resources are
most likely to be the limiting factor, as it requires
considerable computational effort to model a
long, transient process in 3D. Furthermore, the air
entrainment caused by the plunging jet in the gate
shaft and the air blowout downstream are not
exactly separated two-phase flow problems with
well-defined interfaces. Free-surface penetration
by plunging water gives rise to air bubbles that
are initially transported in discrete clusters. This
behaviour is attributed to bubble entrapment by
shear vortices (i.e. large eddies) travelling in the
edge of the jet (Thomas et al., 1984). A refined
CFD model, such as the multi-fluid VOF model
or the dispersed multi-phase model, would most
likely yield more accurate results. These models
are characterised by better physics in dispersed
regions and improved accuracy of interfacial
exchanges.
ACKNOWLEDGEMENTS
This study was conducted as part of a PhD
programme in the area of hydraulic design
financed by the Swedish Hydropower Centre
(Svenskt Vattenkraftcentrum, SVC), Stockholm.
SVC was established by the Swedish Energy
Agency, Elforsk and Svenska Kraftnät, together
with Luleå University of Technology, the Royal
Institute of Technology, Chalmers University of
Technology and Uppsala University.
www.svc.nu. The authors are indebted to Mr Rolf
Steiner, Fortum Generation, for providing the
necessary prototype data for the study. The
computations were performed on the mainframe
computer at the PDC Centre for High
Performance Computing (PDC-HPC) at the Royal
Institute of Technology, Stockholm.
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