Project SEATTLER for renewable electricity.
Rugescu, Radu Dan ; Tache, Florin ; Chiciudean, Teodor Gelu 等
Abstract: The objective of the research described in this paper was
to develop numerical simulations and to compare the results with
laboratory experiments in new, promising zones of aeroacoustics,
considered fruitful for the environmental technologies, particularly
related to aerodynamic noise suppression. When noise measurements are
not being conducted, the cold air turbine embedded in the tower can be
used as an efficient, eco-friendly source of energy.
Named SEATTLER from Solar Energy Actuator for Tall Tower Low-cost
Electricity Research, this moderately tall tower creates a considerable
air acceleration and allows the aerodynamic noise to be definitely
perceived. Numeric simulations applied on this architecture reveal
astonishing air velocities well over 100 m/s in the test chamber area.
Key words: gravitational draught, infra-turbulence wind tunnel,
solar energy, cold air turbine
1. Introduction
The destination of the facility here described is to allow the
development of numerical simulation activities and laboratory
experiments in the new and important field of aeroacoustics, considered
fruitful for the environmenta technologies, particularly related to
aerodynamic noise suppression. The laboratory will consist of four
complementary branches, namely the gravitational draught for
aeroacoustics and infra-turbulence aerodynamics (GDA), solar energy
heating (SHE), space structures and orbital surveillance for
environmental management (SOS) and gravitational oscillator studies
(GOS). Each branch accommodates a subsequent number of specific
activities.
2. SEATTLER first hits
The SEATTLER S&T objectives are to create an innovative,
non-mechanical air accelerator with double application: as an
infra-turbulence, zero driving noise acoustic wind tunnel and as a cheap
solar radiation, direct action electric power plant.
The first, wind-tunnel application, means that noise of industrial
fans and especially of aircraft engines will be ideally studied and
means of suppression found, at a yet unattained level due to its zero
noise. The second one claims a small area alternative to the SB GmbH
Solar Tower power plant that uses a very large greenhouse solar
collector. With its reduced area collector and high radiation
temperature, the SEATTLER solar energy tower ends in a cheaper and
totally ecological manner of electricity production. Regarding the
SEATTLER tunnel, the crucial progress is the complete removal of all
moving parts and consequently of all driving noise sources.
Named SEATTLER from Solar Energy Actuator for Tall Tower Low-cost
Electricity Research, it allows the noise of the flowing air to be
definitely perceived. The new tool will address the area of both
fundamental and industrial research for noise protection of the
environment and especially noise reduction in aeronautics, as desired by
the ACARE-2020 project.
[ILLUSTRATIONS OMITTED]
The avenue towards environment-friendly aircraft engines will thus
be cleaned. Besides the obvious acoustical quality of the rig, its
construction is by far much simpler and far less expensive than of any
other existing noise test facility. It has a vertical, small space
consuming, lightweight design, to be easily incorporated amidst other or
twinned to other existing facilities. It is possible to accommodate it,
for example, near the well-known Bremen University Drop Tower (upper
photo), or directly side-added to such an existing tall building. A
height of the SEATTLER tunnel of 80 meters could attract air speeds of
more than 50 m/s in the test chamber. At the base of the vertical
exhauster (lower photo), a test chamber building is accommodated.
Neither noise nor vibrations will be sent by SEATTLER to the
surroundings, offering in addition a much higher safety-level in
operation also. Tinny noise reduction effects will become accessible and
new standards in aeroacoustics will emerge, with major benefits for
noise investigations on turbo-engine individual parts. Because all
existing facilities are propelled by fan type mechanical driving
equipment, they inevitably produce the well-known eigen-noise: part from
the driving equipment and part from the flow of air in the very tunnel
(see Fig. 3).
This behavior highly worsens the investigation and sensible
progress could only be made when the eigen-noise of the wind tunnel is
either drastically reduced or completely suppressed, as in the case of
the SEATTLER solution.
[FIGURE 3 OMITTED]
The current large-scale electrical fans, despite some recently made
progress, manifest a residual level of eigen-noise, while SEATTLER will
be free of any driving-equipment eigen-noise (see table below).
The examination of the table allows to point out the clear
distinction of the SEATTLER solution, where the driving noise is reduced
below 10dB, in contrast to all other high quality facilities, where the
best achievement of 29dB is offered in Sweden. It is obvious that the
SEATTLER aeroacoustics facility is a high quality tool for the in-depth
study of noise emission during aerodynamic flows around profiles,
especially through blade cascades of air compressors and turbines. The
separation of the soft noise of the flow is usually the main difficulty
of all existing installations. A wind tunnel with no moving parts, where
the airflow runs under gravity draught only, is a crucial advance in
this area and this solution is offered by SEATTLER [11].
The high consumption of energy had also found a practical solution
with SEATTLER through the involvement of the solar heating. A focusing
array of controlled mirrors is used to easy heat the fresh air and
produce the draught effect required to accelerate it through the test
chamber. When the wind tunnel is not under operation a cold air turbine
is imagined to be introduced in the airflow, powered by the draught of
the air and producing electricity after driving a coupled generator.
This dual capability is reducing costs further and offers an unexpected
solution for energy.
3. Gravity draught for air acceleration
The source of the gravitational draught is the ascending effect of
lower density volumes of warm gases in contrast with the higher density
surrounding air as a result of their different weights, quantitatively
described by the famous Archimede's law.
As far as we keep standing in the frames of this effect of gravity
the problem remains entirely immobile. The accompanying buoyant force
supplies the maximal estimate for the draught effect. However, when the
upward motion of the rarefied gas from the inside is considered, the
more elaborated dynamic equilibrium must be approached by the rules of
gasdynamics, although its roots remain in the realm of crude
Archimede's principle.
[FIGURE 4 OMITTED]
The draft in Fig. 4 shows a vertical stack circulated by the warmed
air that defuses into the atmosphere after exiting its top opening. It
is surrounded by higher density cold air and the effect of gravity must
be accounted in computing the different inner and outer pressures that
act on stack's walls. For the sake of simplicity, the air density
is considered as independent of altitude [11], while obviously different
inside and outside.
The aerostatic influence of the gravitation is then given by the
gradient equation both inside (inner density [rho]) and (outer density
[[rho].sub.0]) outside the tower,
d p / d z = -g [rho], d p / d z = -g [[rho].sub.0]. (1)
The right hand term in these equations is nothing but the slope to
the left of the vertical in each pressure diagram from figure 4, meaning
the inner pressure in the stack (left, dotted) is decreasing less
steeply and remains closer to the vertical than the outer pressure. The
dynamic equilibrium is established when, following a series of
transforms, the stagnation pressures inside and outside become equal
(Fig. 4).
While the air outside the stack is preserved immobile and due to
the effect of gravitation its pressure decreases with altitude from
[p.sub.ou](0)[equivalent to] [p.sub.0] at the stack's pad to
[p.sub.ou](l)- at the tip of the stack "4", the inner air is
flowing and, consequently, its pressure [p.sub.in] varies not only by
gravitation, but also due to acceleration and braking along the
0-1-2-3-4 cycle.
The air acceleration takes place at tower inlet between 0-1 as
governed by the energy compressible equation ([GAMMA] [equivalent to]
[kappa] - 1 / [kappa]) with constant density [[rho].sub.0] along,
[p.sub.1] = [p.sub.0] - [GAMMA] / 2 x [[??].sub.2] / [[rho].sub.0]
[A.sup.2], (2)
where A is the cross area of the inner channel and [??] the mass
flow rate, constant through the entire stack (steady-state assumption).
The air is warmed in the heat exchanger/solar receiver between 1-2 with
the heat q per kg with dilatation and acceleration of the airflow,
accompanied by the "dilatation drag" pressure loss [1].
Considering also A = const for the cross-area of the heating zone and
adopting the variable [gamma] for the amount of heating rather then the
heat quantity itself,
[gamm] = [[rho].sub.0] - [[rho].sub.2] / [[rho].sub.0] = 1 =
[beta], (3)
with a given control value for
[beta] = [[rho].sub.2] / [[rho].sub.0] > 1, (4)
the continuity condition shows that the variation of the speed is
simply given by
[c.sub.2] = [c.sub.1] / [beta]. (5)
The impulse equation gives now the value of the pressure loss due
to air dilatation,
[p.sub.2/ + [[??].sup.2] / [[rho].sub.2] [A.sup.2] = [p.sub.1] +
[[m.sub.2] / [[rho].sub.0] [A.sup.2] - [DELTA][p.sub.R]. (6)
where a possible pressure loss [DELTA][p.sub.R] due to friction
into the heat exchanger is considered. Once the dilatation drag is thus
perfectly identified, the total pressure loss [DELTA][p.sub.[SIGMA]]
from pad's outside up to the exit from the heat exchanger results
as depending on the yet unknown mass flow rate [??], as the sum of the
inlet acceleration loss (2) and the dilatation loss (6),
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (7)
equivalent to
[p.sub.2] = [p.sub.0] - [[??].sup.2] / [[rho].sub.0] [A.sup.2] x
[gamma](2 - [GAMMA]) + [GAMMA] / 2(1 - [gamma]) - [DELTA][p.sub.R]. (8)
The gravitational effect (1) continues to decrease the value of the
inner pressure up to the exit rim of the stack, where the inner pressure
becomes
[p.sub.3] = [p.sub.2] - g[[rho].sub.2]l [p.sub.0] - [[??].sup.2] /
[[rho].sub.0][A.sup.2] x [gamma](2 - [GAMMA]) + [GAMMA] / 2(1 - [gamma])
- [DELTA][p.sub.R] - g[[rho].sub.2]l. (9)
The constant density assumption along the upper stack [[rho].sub.2]
= [[rho].sub.3] [[rho].sub.4] was used. Recovery of the static air
pressure, previously [6] considered through a compressible process
governed by the Bernoulli equation
[p.sub.4.sup.*] = [p.sub.3] + [GAMMA] [[??].sup.2] /
2[[rho].sub.2][A.sup.2]
is here replaced with the Unger condition [5] of an isobaric exit
[p.sub.4.sup.*] = [p.sub.3] which, considered into (9) for replacing
[p.sub.3], ends in the equilibrium equation
[p.sub.4.sup.*] = [p.sub.0] - [[??].sup.2] / [[rho].sub.2][A.sup.2]
x [gamma](2 - [GAMMA]) + [GAMMA] / 2(1 - [gamma]) - [DELTA][p.sub.R] -
g[[rho].sub.2]l. (10)
This means that the dynamic equilibrium is re-established when the
stagnation pressure from inside the tower equals the one from outside,
at the exit level,
[p.sub.4.sup.*] [equivalent to] [p.sub.in](l) = [p.sub.ou](l)
[equivalent to] [p.sub.0](0) - g[[rho].sub.0]l. (11)
This equation is the end element that allows determining the
equilibrium value of the air mass flow rate passing through the stack.
Equaling (10) and (11),
[p.sub.0] - g[[rho].sub.0]l [equivalent to] [p.sub.0] -
[[??].sup.2] / [[rho].sub.2][A.sup.2] x [gamma](2 - [GAMMA]) + [GAMMA] /
2(1 - [gamma]) - [DELTA][p.sub.R] - g[[rho].sub.2]l. (12)
Reducing by the quotient g[[rho].sub.0]l the equilibrium equation
appears in the form
[DELTA] p(l) / g [[rho].sub.0]l [equivalent to] 1 + [gamma] -
[GAMMA] / 1 - [gamma] x [[??].sup.2] / 2g l [[rho].sup.0.sup.2]
[A.sup.2] + [DELTA] [p.sub.R](l) / g [[rho].sub.0]l - [[gamma] = 0. (13)
Depending on the construction of the heat exchanger the drag
largely varies. For simple, tubular channels the pressure loss due to
frictions stands negligible [6], [8], [9] and the reduced mass flow rate
(RMF) results from the simple equation
[R.sup.2] [equivalent to] [[??].sup.2 / 2g l [[rho].sup.2]
[A.sup.2] = [gamma] x (1 - [gamma] / [gamma](2 - [GAMMA]) + [GAMMA].
(14)
It represents an alternative to the previous solution of Unger in
1988 [5]
[R.sup.2] [gamma](1 - [gamma]) / 1 + [gamma] (15)
or to the one of Rugescu [6]
[R.sup.2] = [gamma](1 - [gamma] / 1 + [gamma] - [GAMMA] (16)
and gives optimistic values in the region of smaller values of
heating (Fig. 5).
[FIGURE 5 OMITTED]
The accelerating potential and the expense of heat to perform this
acceleration at optimal conditions result from equations (14)-(16). In a
practical manner, the velocity [c.sub.2] results in regard to the
free-fall velocity (Torricelli) [c.sub.l]. Its upper margin is given by
(17) through (14) while the lower margin by (18) through (15),
[c.sub.2H] = [square root of [gamma] x 2gl / (1 -
[gamma])[[gamma](2 - [GAMMA]) + [GAMMA]], (17) [c.sub.2L] = [square root
of [gamma] x 2gl / 1 - [[gamma].sup.2] (18)
In fact these formulae render identical results for the optimal
[gamma] values (Table 2). For a contraction aria ratio of 10 the maximal
airflow velocities in the test chamber [c.sub.e] of the aeroacoustic
tunnel versus the tower height are given in Table 2.
The value of [c.sub.e] was computed according to the simple,
incompressible assumption, which renders a minimal estimate for the air
velocity in the contracted area.
Compressibility whatsoever will tend to increase the actual
velocity in the test area, while drag losses, especially in the heat
exchanger, will decrease that speed. The optimum values for the heating
intensity [gamma] are as follows for upper and lower margin
respectively:
[[gamma].sub.H opt] = [square root of 7 - 1] / 6 = 0 0.274292, (19)
[[gamma].sub.L opt] = [square root of 2] - 1 = 0.414214. (20)
By substituting these optimum values in the corresponding relations
for the c2 velocity, one can easily see that
[c.sup.2.sub.2H] [c.sup.2.sub.2L] = g x l. (21)
4. Turbine effects
According to the design in Fig. 2, a turbine is introduced in the
SEATTLER facility next to the solar receiver, with the role to extract
at least a part of the energy recovered from the sun radiation and
transmit it to the electric generator, where it is converted to
electricity. The heat from the flowing air is thus transformed into
mechanical energy with the payoff of a supplementary air rarefaction and
cooling in the turbine. The best energy extraction will take place when
the air recovers entirely the ambient temperature before the solar
heating, although this desire remains for the moment rather
hypothetical.
[FIGURE 6 OMITTED]
For accesible energy extraction, a quotient is introduced. Major
differences appear in the theoretical model with the turbine system as
compared to the simple gravity draught wind tunnel previously described.
The process of air acceleration at tower inlet is governed by the same
energy (Bernoulli) incompressible (constant density [[rho].sub.0]
through the process) equation as in the previous case,
[p.sub.1] = [p.sub.0] - [[??].sup.2 / 2[[rho].sup.0][A.sup.2]. (22)
The air is heated in the solar receiver with the amount of heat q,
into a process with dilatation and acceleration of the airflow,
accompanied by the usual pressure loss, called sometimes
"dilatation drag" [8]. Considering a constant area
cross-section in the heating solar receiver zone of the tube and
adopting the variable a for the amount of heating rather then the heat
quantity itself,
[gamma] = [[rho].sub.0] - [[rho].sub.2] / [[rho].sub.0] = 1 -
[beta], (23) with a given value for [beta] = [T.sub.1] / [T.sub.2], (24)
the continuity condition shows that the variation of the speed is
given by [c.sub.2] = [c.sub.1] / [beta] (25) No global impulse
conservation appears in the tower in this case, as long as the turbine
is a source of impulse extraction from the airflow. Consequently the
impulse equation will be written for the heating zone only, where the
loss of pressure due to the air dilatation occurs,
[p.sub.2] + [[??].sup.2] / [[rho].sub.2][A.sup.2] = [p.sub.1] +
[[??].sup.2] / [[rho].sub.2][A.sup.2] - [DELTA][p.sub.R]. (26)
A possible pressure loss due to friction into the lamellar solar
receiver is considered through [DELTA][p.sub.R]. The dilatation drag is
thus perfectly identified and the total pressure loss
[DELTA][p.sub.[SIGMA]] from outside up to the exit from the solar heater
is present in the expression
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (27)
Observing the definition of the rarefaction factor in (23) and
using some arrangements, equation (27) gets the simpler form
[p.sub.2] = [p.sub.0] - [[??].sup.2] / [[rho].sub.0][A.sup.2] x
[gamma] + 1 / 2(1 - [gamma]) - [DELTA][p.sub.R]. (28)
The thermal transform further into the turbine stator grid is
considered as isentropic, where the amount of enthalpy of the warm air
is given by
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII].
If the simplifying assumption is accepted that, under this aspect
only, the heating progresses at constant pressure, then a far much
simpler expression for the enthalpy fall in the stator appears,
[DELTA][h.sub.23] = [omega]q = [omega]c [sup.p][T.sub.2] [gamma].
(29)
To better describe this process a choice between a new rarefaction
ratio of densities [[rho].sub.3]/[[rho].sub.2] or the energy quota
[omega] must be engaged and the choice is here made for the later. Into
the isentropic stator the known variation of thermal parameters occurs,
[T.sub. 3] / [T.sub.2] = 1 [omega][gamma], (30) [p.sub.3] /
[p.sub.2] = [(1 - [omega][gamma]).sup.[kappa] / [kappa] - 1], (31)
[[rho].sub.3] / [[rho].sub.2] = [(1 - [omega][gamma]).sup.1 / [kappa] -
1]. (32)
The air pressure at stator exit follows from combining (31) and
(28) to render
[p.sub.3] = [[p.sub.0] - [[??].sup.2] / [[rho].sub.0][A.sup.2] x
[gamma] + 1 / 2(1 - [gamma] - [DELTA][p.sub.R]] [(1 -
[omega][gamma]).sup.[kappa] / [kappa] - 1]. (33)
Considering a Zolly-type turbine the rotor wheel is thermally
neutral and no variation in pressure, temperature and density appears.
The only variation is in the air kinetic energy, when the absolute
velocity of the airflow decreases from [c.sub.3] to [c.sub.3] sin
[[alpha].sub.1] and this kinetic energy variation is converted to
mechanical work outside. Consequently [[rho].sub.4] = [[rho].sub.3],
[p.sub.4] = [p.sub.3], [T.sub.4] = [T.sub.3] and
[c.sub.4] = [c.sub.1] / (1 - [gamma])[(1 - [omega][gamma]).sup.1 /
[kappa] - 1]. (34)
The air ascent in the tube is only accompanied by the gravity
up-draught effect due to its reduced density, although the temperature
could drop to the ambient value. We call this quite strange phenomenon
the cold-air draught. It is governed by the simple gravity form of
Bernoulli's equation of energy,
[p.sub.5] = [p.sub.3] - g[[rho].sub.3]l. (35)
The simplification was assumed again that the air density varies
insignificantly during the tower ascent. The value for [p.sub.3] is here
the one in (34). At air exit above the tower a sensible braking of the
air occurs in compressible conditions, although the air density suffers
insignificant variations during this process.
The Bernoulli equation is used to retrieve the stagnation pressure
of the escaping air above the tower, under incompressible conditions
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII]. (36)
Value for [p.sub.5] from (35) and for the density ratio from (23)
and (32) are now used to write the full expression of the stagnation
pressure in "6" as
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (37)
It is observed again that up to this point the entire motion into
the tower hangs on the value of the mass flow-rate, yet unknown. The
mass flow-rate itself will manifest the value that fulfils now the
condition of outside pressure equilibrium, or
[p.sub.6.sup.*] = [p.sub.0.] g[[rho].sub.0]l. (38)
This way, the local altitude air pressure of the outside atmosphere
equals the stagnation pressure of the escaping airflow from the inner
tower. Introducing (37) in (38), after some re-arrangements, the
dependence of the global mass flow-rate along the tower, when a turbine
is inserted after the heater, is given by the final developed formula:
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (39)
where the notations are again recollected:
[gamma] = [[rho].sub.0] - [[rho].sub.2] / [[rho].sub.0], the
dilatation by heating in the heat exchanger;
[omega] = the part of the received solar energy which could be
extracted in the turbine;
[DELTA][p.sub.R] = pressure loss into the heater and along the
entire tube either.
All other variables are already specified in the previous chapters.
It is clearly noticed that by zeroing the turbine effect ([omega] = 0)
the formula (39) reduces to the previous form in (13), or by neglecting
the friction to (14), which stays as a validity check for the above
computations. For different and given values of the efficiency [omega],
the variation of the mass flow-rate through the tube depends
parabolically of the rarefaction factor [gamma].
4.1. Discussion
Notice must be made that the result in (39) is based on the
convention (29). The exact expression of the energy q introduced by
solar heating yet does not change this result significantly. Regarding
the squared mass flow-rate itself in (39), it is obvious that the right
hand term of its expression must be positive to allow for real values of
[R.sup.2].
This only happens when the governing terms present the same sign,
namely
[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (40)
The larger term here is the ratio [p.sub.0] / g[[rho].sub.0]l),
which always assumes a negative sign, while not vanishing. The
conclusion results that the tower should surpass a minimal height for a
real [R.sup.2] and this minimal height were quite huge. Very reduced
values of the efficiency [omega] should be permitted for acceptably tall
solar towers. This behavior is nevertheless altered by the first factor
in (40) which is the denominator of (29) and which may vanish in the
usual range of rarefaction values [gamma]. A sort of thermal resonance
appears at those points and the turbine tower works properly well.
4.2. Discussion on denominator
The expression from the denominator of the formulae (39) which gave
the flow reportedly, it can be canceled (become 0) for the usual values
of the dilatation rapport (ratio) gamma and respectively quota part from
energy extracted omega. This strange behavior must be explained. The
separate denominator in (40) is,
A [equivalent to] {[gamma] + 1)[(1 - [omega][gamma]).sup.[kappa] +
1 / [kappa]] - [GAMMA]} = 0. (41)
The curve of zeros and the zones with opposite signs are:
[FIGURE 7 OMITTED]
It is yet hard to accept that such a self-amplification or pure
resonance of the flow can be real and in fact the formulae (39) does not
allow, in its actual form, the geometrical scaling of the tunnel and of
the turbine. The rigor of computational formulae is out of any
discussion, this showing that the previous result outcomes from the
hypotheses adopted. Among those, the hypothesis of isobaric heating
before the turbine is obviously the most doubtful.
5. Organisation of the research area
The height of the construction is from 20-m to 140-m. Below and
around the test chamber situated at floor 1, a multi-purpose building of
the laboratory will be installed (Fig. 8,a). The air inlets are located
above the ground floor (Fig. 8,b).
[FIGURE 8 OMITTED]
A surface of around 0.8 ha suffices [7] to collect enough solar
energy for powering the aeroacoustic wind tunnel at its highest
capacity.
Figure 9 shows a 3D model of the tower assembly designed in a CAD
application environment. It comprises the tower with the inlet geometry,
the laminator, the turbine and the heater.
[FIGURE 9 OMITTED]
6. Numerical simulations
The geometry presented above has been implemented in a commercial
CFD application in order to compare the previously mentioned theory and
formulae with numerical simulations on the full-scale model of the
draught tower.
The grid used for integrating the equations that describe the air
flow through the tower is made of 152600 cells, 307519 faces and 154914
nodes. The operating conditions adopted for the simulation are as
follows: operating pressure 101325 Pa, operating temperature 300 K,
operating density 1.225 kg/[m.sup.3] gravitational acceleration 9.81
m/[s.sup.2]. Though the flow is primarily laminar, the numerical model
used was a well-known k-epsilon model for turbulence, which presented
the advantage of taking into account full buoyancy effects. And by
giving a low turbulence intensity as input data (1%), the numerical
model was very close to the real phenomena occuring in the draught
tower. The properties adopted for air are: [c.sub.p0] = 1006.43 j/kg/K,
[[lambda].sub.0] = 0.0242 w/m/K, [[eta].sub.0] = 1.7894 x [10.sup.-5]
kg/m/s. The boundary conditions for the important sections of the tower
were adopted as follows: atmospheric pressure of 101325 Pa and 300 K
temperature for the area surrounding the inlet, 101000 Pa and 300 K for
the exit section at the top of the 80 m tall tower. For the heater: a
temperature of 418 K. No heat exchange with the exterior environment was
considered (perfectly isolating walls). Results after some 50000
iterations are briefly presented in the figures below.
[FIGURE 11 OMITTED]
7. Conclusions
Numerical simulations performed had shown that the boundary
conditions play a major influence upon the results and the numerical
problem is mainly related to the correct formulation of those
conditions. In most cases however the air acceleration was found in very
good agreement to the experimental data.
The experimental set-up was established with minimal size and
maximal simplicity, according to the resources of the CNCSIS grant. Two
parameters of the airflow were subjected to measurements: the mean speed
in the entrance zone of the tunnel and the exiting air temperature. The
experiments were only run with the free gravitational draught and
electrical heating of the air. The turbine efect was not yet covered
during the tests. It was in the intention of the research team to first
demonstrate the capacity of free air acceleration and the value of the
theoretical predictions. All these aspects were well covered and the
further development of the SEATTLER project depends now on the funding
available. The present results prove that the concept is established and
really promising. The path towards the gravitational energy extraction
tool for ecological, renewable electricity is open.
8. References
[1] Bejan, A., Convection Heat Transfer, New York, Wiley and Sons,
1984.
[2] Gunter, H., In hundert Jahren--Die kunftige Energieversorgung
der Welt, Kosmos, Gesellschaft der Naturfreunde, Franckh'sche
Verlagshandlung, Stuttgart, 1931.
[3] Jaluria, Y., Natural Convection, Heat and Mass Transfer,
Oxford, New York, Pergamon 1980.
[3] Jaluria, Y., Natural Convection, Heat and Mass Transfer,
Oxford, New York, Pergamon 1980.
[4] Raiss, W., Heiz- und Klimatechnik, Springer, Berlin, vol. 1,
pp. 180-188, 1970.
[5] Unger, J., Konvektionsstromungen, B. G. Teubner, ISBN 3-519-03033-0,Stuttgart, 1988.
[6] R. D. Rugescu, T. G. Chiciudean, A. C. Toma, F. Tache, Thermal
Draught Driver Concept and Theory as a Tool for Advanced
Infra-Turbulence Aerodynamics, in DAAAM Scientific Book 2005, ISBN
3-901509-43-7 (Ed. B. Katalinic), DAAAM International Viena, 2005.
[7] F. Tache, R. D. Rugescu, B. Slavu, T. G. Chiciudean, A. C.
Toma, V. Galan, Experimental Demonstrator of the Draught Driver for
Infra-Turbulence Aerodynamics, 17th International DAAAM Symposium,
Vienna, Austria, 8-11 Nov. 2006;
[8] R. D. Rugescu, Thermische Turbomaschinen, ISBN 973-30-1846-5,
Ed. D. P. Bucuresti, Romania, 2005.
[9] Flandro, Gary A., Majdalani, Joseph, Aeroacoustic Instability
in Rockets, AIAA Journal v. 41 no. 3, March 2003, p. 485-97, ISSN 0001-1452.
[10] T. G. Chiciudean, R. D. Rugescu, F. Tache, A. Toma, Draught
Tower Driver for Infra-Turbulence Aerodynamics, The 16th DAAAM
Symposium, 19-22nd October 2005, Opatija, Croatia.
[11] R. D. Rugescu, S. Staicu, I. Magheti, T.G. Chiciudean, F.
Tache, B. Slavu et al., Research Grant CNCSIS code A308/2005 (MEC,
Romania), Metodica de calcul [s.sub.i] proiectare dinamica inversa
pentru tunelul aeroacustic neconventional fara mecanisme de antrenare
WINNDER, Bucharest, 2005.
[12] Carafoli, E., Constantinescu, V. N., Dynamics of compressible
fluids, Ed. Acad. R.S.R., Bucuresti, pp. 136-137, 1984.
[13] Scharmer, K., Greif, J. (2000), The European Solar Radiation
Atlas, Presses de l'Ecole des Mines, Paris, France.
[14] Mueller R.W., Dagestad K.F., Ineichen P., Schroedter M., Cros
S., Dumortier D., Kuhlemann R., Olseth J.A., Piernavieja G., Reise C.,
Wald L., Heinnemann D. (2004), Rethinking satellite based solar
irradiance modelling--The SOLIS clear sky module. Remote Sensing of
Environment, 91, 160-174.
[15] Energy Information Administration, Form EIA-63B, "Annual
Photovoltaic Module/Cell Manufacturers Survey."
[16] Schleich Bergermann und Partners, EuroDish System Description,
2005.
[17] Energy Information Administration, Office of Coal, Nuclear,
Electric and Alternate Fuels, Renewable Energy Annual 1996, U.S.
Department of Energy, Washington, DC 20585, April 1997.
[18] Majdalani, J., Van Moorhem, W. K., Improved time-dependent
flowfield solution for solid rocket motors, AIAA Journal v. 36 no. 2
(February 1998) p. 241-8.
Authors data: Dr. Sc. Rugescu R.[adu] D.[an] & Eng. MSc student
Researcher Tache F.[lorin], Eng. MSc student Slavu B.[ernard], Eng. MSc
student Galan V.[iorel], Eng. PhD student Chiciudean T.[eodor] G.[elu],
Eng. PhD & MSc stud. Toma A.[dina] C.[ristina], University
"POLITEHNICA" of Bucharest, Romania, rugescu@yahoo.com,
flotasoft@yahoo.com, slavu_bernard@yahoo.com, teodorgelu@yahoo.com,
tomaadinacristina@yahoo.com
This Publication has to be referred as: Rugescu, R.D.; Tache, F.;
Chiciudean, T. G.; Toma, A.C.; Slavu, B. & Galan, V. (2006). Project
Seattler for Renewable Electricity, Chapter 42 in DAAAM International
Scientific Book 2006, B. Katalinic (Ed.), Published by DAAAM
International, ISBN 3-901509-47-X, ISSN 1726-9687, Vienna, Austria
DOI: 10.2507/daaam.scibook.2006.42
Table 1. Comparative outlook of some known low noise tunnels
Speed
Wind Tunnel Test Section Range
Facility owner Type (m) (Mach No.)
United Acoustic 1.5 Dia. 1 Mach [less than
Technologies or equal to]
USA 0.65
Georgia Inst. Low turbulence 1 x 1 3 - 23 m/s
Tech. USA
NASA Langley Low turbulence 2.25 x 0.9 x 2.25 0.05 - 0.5
R.C. USA
Goldstein Low turbulence 0.5 x 0.5 x 3.0 42 m/s
Research Lab.
UK
Maibara RTRI Low Noise 3 x 2.5 x 8 85 m/s
Japan
Audi Germany Low noise 9 x 15 x 16 83 m/s
TsAGI Russia T-32 1 x 1 x 4 2 - 80 m/s
Royal Institute Low turbulence 0.8 x 1.2 x 7 68 m/s
Sweden
SEATTLER Zero driver [less than or 0 - 140 m/s
Project noise equal to] 0.4
Turbulence/ Reynolds
/Eigen- (/mx
Facility owner noise [10.sup.6])
United n.a. 0.16
Technologies
USA
Georgia Inst. 16%/50dB 0.15
Tech. USA
NASA Langley n.a. 0.13-5.
R.C. USA
Goldstein <0.03%/n.a. n.a.
Research Lab.
UK
Maibara RTRI <0.3%/35dB n.a.
Japan
Audi Germany n.a./46dB 2
TsAGI Russia >0.01%/n.a. 0.13-5.3
Royal Institute <0.02%/29dB n.a.
Sweden
SEATTLER 0.01%/<<10 up to 1
Project dB
Table 2. Draught vs. tower height for a contraction ratio 10
l [c.sub.l] [c.sub.1] [c.sub.2] [c.sub.e]
m m/s m/s m/s m/s
7 11.72 4.85 8.28 82.8
14 16.57 6.86 11.72 117.2
30 24.26 10.05 17.15 171.5
70 37.05 15.35 26.20 262.0
140 52.40 21.71 37.05 370.5