steady state and transient ampacities of gas-insulated transmission lines
TRANSCRIPT
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8/11/2019 Steady State and Transient Ampacities of Gas-Insulated Transmission Lines
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I MELECON
2002,
May 7-9,2002, Cab,EGYPT.
Steady State and Transient Ampacities of
Gas-Insulated Transmission
Lines
M.
B.Eteiba
ElectricalEngineeringDepartment
Cairo
University,
Fayoum, Egypt
Tel: 02)0101
500885
Email [email protected]
Abstract
This
paper presents
a t h d
model
for
predicting the
steady state and transient ampacities
of gas--
transmissionlines (GILs).
Using the
t h d
odel, a
computerprogram
hasbeen formulated such
th t it caa
estimate he ampacity of a GIL for any time-varyingor
collstant QllTent loading and any variation
m
e n v i r o d
conditions
Relations
for
the oonve tion
and
radiation
heat
trander d u e a h
ar a GIL
tilled
mixture
of
both
gases
arepresente&
The
validity
and a c ~ u ~ c yf
the
ampacity
model were
vaified
by
comparing
the predicted tempersture of
core, gas,
and
enclosure
of
the GIL wiib
measured
temperatures
reported
m
the l i t e under the 58me
conditions. Analytically predicted and -tally
values both show close agreement to each
nitrogen resulted
in
a
CoadudOT temperatwe of only
lessthan1chotteal3lailsF6alone.
Keywords transmission
lines,
t hermal rating,
m w as cables, trans iatcableamPScity.
with sutfiuHeaxfluoride
( S F s ) ,
& &
OT a gas
O k . bkeOVer, using
a 50 -50
R l h l l l ?Of
SF6
and
1. INTRODUCTION
Convdonal solid insulation power t r d o n
cables are gtmerally limited to working below about
2000
A. Superconducting cables
can
of course,
transnit a considerably higher ament, but
the
method
at
present in
an
early state of
development and much
would
seea
to
depend
on the economic
ma f
.
the ceramic
conductor [l]. Gas-hsdated transmssi on
Lines (GILs), on the other hand,
are
promising
alternatives as
the
basic technology has a proven
pedigree because
it is well established in the form of
not require
supplementay
cooling
and can
be run over
di stances of more than
25-30
km
without additional
power
faEtor
c o d o n
[4].
Typical
i nstal l ati ons
of
GIL systems
have
been in buried and abovegrouud
getaways,
links
iuside substations, and far systems
SFs s w i t c h g ~nd bus ducts [2,3].Moreover,
they
Q
. .
inside unnels, vertical shafts, and n
owers
A few papers
have
been written that discuss the
calculation of
steady state ampacity
of
GILs [5,6].
Little
effort
has
been put mto
the
subject of transient
q a c i t y models for GILs
p].
i r e ratingsbetter
refled the
thermal
performance
of
a d u c t o r than
steady
state
values,
because
H
d u c t o r
will
not
mstantaneouslyjump nnn
one
itemperatueto another
when the
current or environmeartal
conditionschauge.
The
conductor
h ever ,
changes tern-
graduauy as the
metal
s t o r e s e l u ~ d u e t otsthemal
capacitance.
The object of the present p i w is to present a
ahl
hermal
model which enables the
prediction
of the
heat transfix characteristicsof
a single
[5-lo].
abovegrwnd
GIL
systan
nlsulated
wth
p m
F6
OT sF6 m g e n gas
The factors f i m c h g
such charaG-9 are
s y s t s ~
tudied and
compared
with
the
available
reported a p e r i m e d
data
m
the
iteratwe.
After thisbriefintroduction,afull
descnption of
the
Gal model
is
pmealted.
The
result
of
testing
the
model
on
a
real experimental
data is followed togethea with fi nal u m d d and
l-ehmxx.
2. THERMAL,MODEL DEVELOPMENT
The CUrrentGarrying capacity, or ampacity,
of al l
elements
in
he
current path of
a
power delivery system
is
limited by a
maximum
openlting
temperature.
The
equation relating
the
c u t
to temperatue is
suggested, m
the
present inv&ation,
to be
duived
by
applymg the comation ofenergy approach.A cross
Section of a typical GIL system can be considered as
comprised of three major
components:
1 the core;
2
the
insulating gas; and 3 the externd she h or
enclosure.
An tmexgy
balance
is performed on
each of
these
components
ielding
a
set
of
hree,
ordinary,
first
order, Mkent i a l
equations.
Aftea calculating
the
iuitial compolrent tempatures,
the transient
temperaaues
are
obtained by :knultawously solving
the
three equations,
0-7803-7527-0/02/S17.00 02002 IEEE. 424
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2 1
Energy B alance Equations
A n energy balance on the core may be expressed
as:
cl--W,Tc
-
-h,A,(T, -Tg)-aA,FW(T: -TY)
2.1
dt
An energy balance on the insulating gas yields:
2.2
2$=h,A,bc-Tg)-h,A,(TgT -T8)
An energy balance on the outer sheath
or
enclosure
results in
the foilowing equation:
C3--=Wz+W3+aTs AcF,(Tz4-T,'4)
dt
+h, A, (Tg -
T,
- h, A,
T,
T, )
-
a Am,
(T8.4
-Ti4)
2.3
Where: To, T T,, and
T,
are
conductor,
gas
enclosure,
and ambient temperature> in
'C,
espectively. A n
asterisk denotes the absolute temperature in
K.
C,, C2
and
CJ
are conductor,
gas,
and enclosure
heat capacityin J/'K.m, respectively.
W1,
W2,
nd
W3
re conductor, enclosurepower
loss,
and the
heat increase
of enclosure by
solar
radiation,
in
Whn, respectively.
EG E L
emissivity coelficient of conductor
surface, enclosure inner surface, and enclosure
outersurface espectively.
= A Dc, = A D , , ,
= A
D,. D,, D, and D,
m) re the conductor outside
metex
and the
enclosure
inside and outside diameters,
respectively.
2.2 Heat TransferCoefficients
There are several convective heat
transfer
coefficients
in
the
energy
balance equations that must be evaluated
to
determine the average temperature of the cable
components. The convective heat trandkr weficient
between the cable core and the surrounding gas, h,
,
s
given
by
classical
Nusselt number correlation's
as
[11,12]:
where
2.4
2
N, = 9 ?
In[1+_4_]
Nui
(0.649
R ~ c [ l + ( ~ ) ' ] - X ) 1 5 + ( 0 . 1 2 R $ c ) ' 5
Pr
The convective heat transfer coefficient between the
insulating
gas
and the inside of the outer
sheath,
hp
canbe
evaluated using a similar
procedw
as:
2.5
- 2
N =
2
N
ud
usi
f
In
El--]
To
evaluate the convective heat transfer coefficient on
the outer surface of the sheath, the sheath is modeled
as a long horizontal cylinder in a r If the a r velocity
over the
sheath is
zero
(no
wind effect is considered),
the heat transfer coefficient
from
the sheath
is
by
fiee
convection. The fiee convection heat transfer Nusselt
number can be approximated by the equation
[
131:
where
gpp2(Ts-Ta)D' P, and the convective heat
w
a m
transier coefficient for
fiee
convection between the
outside
of
the sheath and the
air
is given by
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the cmlmure
inside
surfrrce
a d
also
from
the
OIL
outer
X to
the ambient air The pr0pamon of heat
removed by radiation
is
considerable
and must be
account
for in
calculations.The
8mount of
heat
trmder
by radiation depends upon a
number of
faders
including surface temp- and
anissivitieS.
The
shapefactorF, isexpressedas:
2.7
2.4
ThermophysicalProperties
several fhamophysical properties
of
the
three
cable
components
and the mundjng
air
must
be
determined
bef ore the energy
balance
equations c ~ n
e
solved. Gas viscoSity
@),
thermal amductivity (k),
density
@It and
@heat GI be expressed as
function
of
GIL component temperatureand ev lu ted
ollce the tt-m-
has been
specified
E x p
for the
hermopbysical
PrOPeXtk Of
sF6,
OgeIl, a;,
and GIL condu~tox~material as
f uncti on
of
tempaatureare . A in[l]. Expressions for
specificheatsofthe
GIL
mrrterialsare
also
included.
3.THERMALMODEL VERIFECATION
The
capability
of
the thermal
model is
i l l ustrated by
calculating the
component
tmp
hen
the
GIL
system
is
subjected to a lypaa set of opeaafing
conditions
reported
in
171. The
tested
system
con sts
of a horizontal coaxial d g u r n with the
c o m i u c W s outea
diameter
of0.18 m and a thickness
of 0.02 IIL
The enclosure's
inner
diameter
and
thi ckness are 0.47
m
and
0.015 m,@vely. Both
the amductor and the enclosure are made of
Aluminum
alloy.
The conductor's outeh sl f ce
was
tre ted wt black Alumite EO = 0.9 , while the
enclosure's
inner surface was eft
unpainted ( ~ e 0.1).
The
enclosure's OW surface was
coatedwith
a paint
having
an emissivity
E
of 0.8. Figure 3.1 showsthe
relation
between
curretlt and temperature rises above
ambient
kmpe for
the system
under
agnxment
between
calculated and measured
values is
good
and reasonable for
both the
conductor
and
the
@ d i o n With SF6 gaS PreSnae
Of
0.45
The
enclosure.
The
slight
fdakenw
between
calculated
end ahKs Of
the
sF6 gaS
hIlpelXbSe
k
I
O4 4 5 9
5.5
6
6
7
7.5
Fig. 3.1 Calculated and measu~d
emperature
rise vs.
-*A
clmelt load
t8.1 0.2 0 3 0.A
o.rP=-=ww
Fig. 3.2 Calculated and
w . e d
tempeaature ise
vs.
The
temperature
change
with time
for
a
ament
load of
7300 A
and with
no wind
ad without direct
solar
radiation
is
shown
m
Fig.
3.3, where
conductor
heat
capacity
C1=
24 (kJfK.m), SFa
gas
heat
capacity
C2
655
(JTKm),
and enclosure 'heat capacity
C,
=
45
gaspressure
at8000A
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Acknow IedBment
The author
is
grateful to
his
txAleague Dr. I.
Awad
whose cooperative
effort
has contributed
to
the
computer resultsumtained in the paper.
428