The cruise operation of a single-spool turbojet engine (Fig. 12.13) is defined as follows:
• Flight Mach number (M_{1}) = 0.85
• Ambient temperature (T_{1}) = 251.6 K
• Ambient pressure (p_{1}) = 0.45 bars
• Shaft speed (N) = 34,000 rpm
• Turbine-inlet total temperature (T_{t\ 4}) = 1152 K
• Combustor total-to-total pressure ratio (p_{t\ 4}/p_{t\ 3}) = 0.93
• Fuel heating value (H) = 4.42 × 10^7 J/kg
• Mechanical efficiency (η_{m}) = 98%
• Turbine total-to-total efficiency (η_{T}) = 84%
• Turbine stator is choked
Assuming a negligible fuel-to-air ratio only in items Ia through Id, calculate:
Ia) The turbine-exit total pressure (p_{t\ 5});
Ib) The turbine-exit total temperature (T_{t\ 5});
Ic) The physical mass-flow rate (\dot m) through the compressor;
Id) The nozzle-exit Mach number and the specific thrust;
Ie) The actual fuel-to-air ratio (f);
If) The specific fuel consumption (SFC).
II) Consider the case where the mass-flow rate (\dot m) and shaft speed (N) are gradually decreased, while maintaining the same compressor total-to-total pressure ratio, compressor inlet conditions, and turbine-inlet total temperature (T_{t\ 4}). Calculate the minimum magnitude of physical shaft speed (N) below which the compressor operation becomes unstable. Also calculate the corresponding magnitude of the compressor physical mass-flow rate (\dot m_{2}).
Part Ia:
T_{t\ 2}=T_{1}\biggl[1+\biggl(\frac{\gamma-1}{2}\biggr)M_{1}{}^{2}\biggr]=288.0\,\mathrm{K}
p_{t\ 2}=p_{1}\Big[1+\Big({\frac{\gamma-1}{2}}\Big)M_{1}{}^{2}\Big]^{\frac{\gamma}{\gamma-1}}=0.722\,\mathrm{bars}
N_{C2}=\frac{N}{\sqrt{\theta_{2}}}=34,000\,\mathrm{rpm}
N_{C4}={\frac{N}{\sqrt{\theta_{4}}}}=17,000\,\,\mathrm{rpm}
Because the turbine is choked,
\dot m_{C4}=2.0\,\mathrm{kg/s}
Let us now consider the following equality:
\dot{m}_{C4}=\dot{m}_{C2}\sqrt{\frac{T_{t\ 4}}{T_{t\ 2}}}\biggl(\frac{p_{t\ 2}}{p_{t\ 4}}\biggr)
In this equality, both \dot m_{C2} and p_{t\ 4} are unknown. Knowing that N_{C2} will always be 34,000 rpm (θ_{2} = 1.0), we can proceed to solve this equality through a trial-and-error procedure, as follows:
First attempt – Set \dot m_{C2} to 13.0 kg/s: Now
{\dot{m}}_{C4}=2.0\,\mathrm{kg/s}={\dot{m}}_{C2}{\sqrt{\frac{T_{t\ 4}}{T_{t\ 2}}}}\biggl({\frac{p_{t\ 2}}{p_{t\ 4}}}\biggr)
This will provide us with a magnitude of 9.39 bars for p_{t\ 4}.
On the other hand, we can compute the same variable (say p_{t\ 4}{}^{\prime}), where
p_{t\ 4}{}^{\prime}={\frac{p_{t\ 4}}{p_{t\ 3}}}{\frac{p_{t\ 3}}{p_{t\ 2}}}p_{t\ 2}=8.06\;\mathrm{bars}
Comparing the two magnitudes of p_{t\ 4}, this attempt has produced an error of 15.2%, which is unacceptable.
Second attempt – Set “\dot m_{C2}” to 12.0 kg/s: Following the same approach as on the first attempt, we get
p_{t\ 4}=8.66\;\mathrm{bars}
p_{t\ 4}{}^{\prime}=8.72\mathrm{~bars}
This yields an error of 0.7%, which is acceptable. Let us now proceed with an average p_{t\ 4} magnitude of 8.69 bars.
At this point, the compressor operating conditions can be read-off the compressor map as follows:
\dot m_{C2}=12.0\,\mathrm{kg/s}
\pi_{C}={\frac{p_{t\ 3}}{p_{t\ 2}}}=13.0
N_{C2}=34,000\,\mathrm{rpm}
\eta_{C}=80%
The compressor total-to-total temperature ratio (\tau_{C}) can be computed as
\tau_{C}=1+\frac{1}{\eta_{C}}\biggl[(\pi_{C})^{\frac{\gamma_{C}-1}{\gamma_{C}}}-1\biggr]=2.351
With the fuel-to-air ratio f\approx0, we can compute the turbine total-to-total temperature ratio (\tau_{T}) as
\tau_{T}=1-\left[\frac{1}{\eta_{m}}\frac{c_{p_{C}}}{c_{p_{T}}}\frac{T_{t\ 2}}{T_{t\ 4}}(\tau_C -1)\right]=0.701
Just as easily, we can calculate the turbine total-to-total pressure ratio (π_{T}) as
\pi_{T}=\left[1-\frac{1}{\eta_{T}}(1-\tau_{T})\right]^{\frac{\gamma_{T}}{\gamma_{T}-1}}=0.169
It follows that
p_{t\ 5}=\pi_{T}p_{t\ 4}=1.472\;\mathrm{bars}
Part Ib:
T_{t\ 5}=\tau_{T}T_{t\ 4}=807.6\,\mathrm{K}
Part Ic:
{\dot{m}}_{2}={\dot{m}}_{C2}{\frac{\delta_{2}}{\sqrt{\theta_{2}}}}=8.66\;{\mathrm{kg/s}}
Part Id:
p_{t\ 5}=p_{t\ 6}=p_{6}\biggl[1+\biggl(\frac{\gamma_{T}-1}{2}\biggr)M_{6}{}^{2}\biggr]^{\frac{\gamma_{T}}{\gamma_{T}-1}}
which, upon substitution, yields
M_{6}=1.307
Noting that T_{t\ 5} is equal to T_{t\ 6}, we can calculate the exit static temperature as follows:
T_{6}=\frac{T_{t\ 6}}{\left[1+(\frac{\gamma_{T}-1}{2})M_{6}{}^{2}\right]}=630.0\mathrm{\,K}
We can now proceed to calculate the engine specific thrust as follows:
V_{6}=M_{6}a_{6}=M_{6}\sqrt{\gamma_{T}R T_{6}}=641.0\,\mathrm{m/s}
V_{1}=M_{1}a_{1}=M_{1}\sqrt{\gamma_{C}R T_{1}}=270.3\,\mathrm{m/s}
F/\dot m=V_{6}-V_{1}=370.7\ \mathrm{N/kg}
Part Ie: We now calculate the accurate value of the fuel-to-air ratio (by applying the energy equation to the combustor) as follows:
f=\frac{(c_{p_{T}}\,T_{t\ 4}-c_{p_{C}}\,T_{t\ 3})}{(H-c_{p_{T}}\,T_{t\ 4})}=0.0152
Part If: The specific fuel consumption is now easy to calculate:
S F C={\frac{f}{F/\dot m_{2}}}=4.11\times10^{-5}{\mathrm{~kg/N}}
Part II: Following a constant -π_{C} (i.e., horizontal) line on the compressor map until we get to the surge line, the compressor instability prevails at the point where
(N_{C})_{m i n.}=33{,}700\;\mathrm{rpm}
(\dot m_{C})_{m i n.}=10.7\mathrm{~kg/s}
which, in terms of physical variables, translate into
(N)_{m i n.}=\sqrt{\theta_{2}}(N_{C})_{m i n.}=33,700\;\mathrm{rpm}
(\dot m_{2})_{m i n.}=\frac{\delta_{2}}{\sqrt{\theta_{2}}}(\dot m_{C})_{m i n.}=7.73\mathrm{~kg/s}