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FINAL TECHNICAL REPORT
February 1, 2013, through July 31, 2014
Project Title: INCREASING EFFICIENCY OF AN EXISTING PC BOILER
USING VFDS AND IMPROVED HEAT EXCHANGERS
ICCI Project Number: 13/5A-1
Principal Investigator: Dr. James Mathias, Southern Illinois University
Project Manager: Joseph Hirschi, Illinois Clean Coal Institute
ABSTRACT
This study examined options for increasing the overall efficiency of a coal-fired power
plant by decreasing the auxiliary power load using variable frequency drives (VFDs) on
various motors and by improving heat transfer occurring in the power cycle. The study
was conducted at Southern Illinois Power Cooperative’s Lake of Egypt power plant. The
goal was to identify reductions in auxiliary power that would reduce the parasitic load on
the power plant by 1% and to identify areas of increased heat transfer that would increase
overall plant efficiency by 1%.
In power plants, gas and liquid flowrates are often controlled using dampers or valves
while motors powering pumps and fans stay at full speed resulting in a significant amount
of wasted electrical power. Recognizing this, the host plant installed VFDs on two forced
draft fans supplying air to the cyclone boiler and on two booster fans pushing air through
the scrubber. Energy savings and efficiency improvements resulting from that effort
were analyzed and documented. Then, six additional motors were evaluated for potential
energy savings resulting from installation of VFDs. Results indicate that using VFDs
achieves annual savings totaling 38.5 GWh, or a 2.05% increase in overall plant
efficiency. Total project costs are estimated to be $2.5 million resulting in a simple
payback period of less than two years assuming 0.04 $/kWh.
In addition to the parasitic load on the power plant, energy is also lost due to poor heat
recovery prior to exhaust gases leaving the system. For every degree reduction in the flue
gas temperature by means of heat recovery that is reused elsewhere in the cycle,
2,000 MMBtu of coal could be saved annually. Five heat recovery options were
examined with coal drying proving to be the most viable use of waste heat recovered
from the flue gas. With that option, coal could be upgraded from 11,000 to 11,740 Btu/hr
resulting in savings of $2.28 million annually for a payback period of just 2.1 years. For
this scenario, heat recovery results in a 120°F degree reduction in flue gas temperature
amounting to a 2.54% increase in cycle efficiency.
2
EXECUTIVE SUMMARY
With the United States (US) Environmental Protection Agency (EPA) having proposed
more stringent emissions regulations, maintaining and improving cycle efficiency is of
utmost importance to coal-fired power plants striving to reduce emissions and operating
costs. To that end, variable frequency drive (VFD) controls were installed on blowers
supplying air to a pulverized coal boiler (Unit 4) capable of generating 173 MW at
Southern Illinois Power Cooperative’s (SIPC’s) Lake of Egypt power plant. A
preliminary analysis of this effort indicated that VFDs reduced auxiliary power use and
created significant energy savings (Achelpohl, 2014). The purpose of this project was to
document those reductions and savings and to identify and evaluate additional VFD
applications throughout the same plant, which also has a fluidized bed boiler (Unit 123)
capable of generating 120 MW. Furthermore, areas in which improved heat transfer
could boost cycle efficiency were examined.
This study first examined VFDs installed in the previous project to determine how much
energy is being saved (Task 1). Next, several additional motors were analyzed for
potential VFD installation (Task 2). Task 3 determined how much cycle efficiency could
be improved if additional heat were recovered from the flue gas. Then, the best way to
recover and utilize that heat was examined (Task 4). Finally, the entire steam cycle was
analyzed to determine any potential improvements from using heat exchanges as
feedwater heaters (Task 5).
VFDs have proven to be an extremely viable method of saving energy in the right
application. Applications with significant energy saving potential include:
Motors that are oversized for their design load.
Motors that start and stop frequently.
Motors that produce a flow of air or liquid that is significantly controlled by a
valve or damper (throttled).
Initial VFD installations were on Unit 4’s two booster fans and two forced draft (FD)
fans totaling 14,000 HP. Total project cost was $2.9 million, of which $2 million was
provided by government grants. With annual savings of about $900K, this project
achieved a quick payback period even if grants had not been available.
Additional motors analyzed for VFD use included Unit 123’s primary, secondary, and
induced draft (ID) air blowers and Unit 4’s boiler feed and condensate pumps. Each
motor showed potential savings of greater than 40% with three cases exceeding 60%. If
all six VFDs were installed as suggested, potential energy savings could be $1.54 million
annually on a total of 14,600 HP, which is even higher than the initial VFD installation.
With a total project cost near $2.5 million, return on investment could be seen in less than
two years.
The fluidized bed boiler (Unit 123) has flue gas stack temperatures that are regularly
320°F. This is a significant amount of energy that if recovered could help improve
3
efficiency by up to 2.54%; however, due to a number of compounding factors the energy
is not recovered easily or cheaply. The major cost is due to the need for a special heat
exchanger. As stack temperature is reduced, there is a greater risk of corrosive
condensate that will likely destroy both the stack and any components inside. Thus,
recovering any additional energy from the flue gas calls for a condensing heat exchanger
set-up that is protected from any corrosive condensate.
There are very few industrial heat exchanger options capable of condensing flue gas and
recovering both sensible and latent heat from it. While the technology exists, it is most
often geared toward natural gas power plants where economic feasibility is much better
due to the fuel’s higher cost, a larger percentage of latent heat available, as well as less
corrosive chemicals in the flue gas.
If a condensing heat exchanger were to be implemented, the heat could be utilized in one
of many ways. Selling to a nearby industry is the simplest and has the lowest capital
cost; however, it is only an option if such an industry were readily available. Preheating
the combustion air at this plant would be very appealing if there were a way to modify
the existing steam-to-air heat exchanger, lowering the total project cost significantly.
Coal drying seems to be a great use of waste heat and is the most economically viable
option; however, it would be even more effective if higher temperature heat were
available or used with coal that is higher still in moisture content. Heating the feedwater
may be a good use of recovered heat in other plants; however, in this plant there is not
enough heat available to completely satisfy the heater’s needs, plus the length of the run-
around loop requires a premium cost to build and run. Organic Rankine cycles proved to
provide a decent amount of power; however, it is still much too low to have a payback
period that would justify the cost of the entire system.
While each project is feasible in principle and each has decent output, the total cost of
recovering most of the waste heat potential is still not economically feasible due to the
high cost of the condensing heat exchanger. The one exception to this is the coal dryer,
which has an excellent payback period. It should be noted that along with any energy
savings comes a reduction in CO2 emissions, which could make any application much
more appealing as EPA requirements continue to become more stringent.
In the final task, the steam cycle analysis did not yield results that would suggest
improvements that could be made in any of the feedwater heaters. All of these heaters
performed at an effectiveness above 77%, with most even in the mid 90% range. This
leaves little room for improvement, let alone any gains that would justify upgrades. Any
changes would have a payback period much too great to justify costs needed for
improvement.
4
OBJECTIVES
The purpose of this project was to determine energy efficiency gains by implementation
of variable frequency drives and additional heat transfer capability, as well as to
determine the feasibility of initial cost of investment for each project. These objectives
were accomplished by completing the following five major tasks:
Task 1 Conduct a thorough analysis of variable frequency drives (VFDs) already
installed at the host facility and determine energy savings that are being
achieved.
Task 2 Analyze six other motors which likely have the best potential to result in
savings by implementing VFD technology.
Task 3 Determine the overall plant efficiency increase that can be attained by
improved heat recovery in the flue gas stack.
Task 4 Determine the dew point of the flue gas as well as the best way to recover
additional energy from the stack.
Task 5 Examine five heat exchangers in the plant that have the largest approach
temperature.
INTRODUCTION AND BACKGROUND
Growing energy demand and increasing emphasis on cleaner emissions has caused the
cost of generating electricity to rise and many people have begun looking for more
efficient and/or alternative sources. Most of the United States (US) has been powered by
coal-fired electricity generation for years (US EIA, 2011); yet recent climate change
concerns have begun to erode coal’s market share. In an attempt to remain viable, many
coal-fired plants are looking for ways to compete with natural gas prices and renewable
energy mandates. To do this it is necessary to improve efficiency to meet both consumer
cost and environmental requirements. An increase in efficiency could either reduce fuel
consumption and emissions produced or allow for higher overall power generation to
meet demand without increasing plant size, fuel usage, or emissions. Both scenarios help
make coal a more viable source of energy (Achelpohl, 2014).
There are a few key ways to improve the efficiency of a power plant. The first is to
improve the amount of heat gained from the combustion of the coal. This can be done by
reducing the heat lost at the boiler by the use of additional insulation. The second is to
use more efficient components such as the turbines, generators, or burners. The third is
to reduce the amount of auxiliary power used by the plant. One method of doing this is
to use VFDs on motor driven blowers and pumps. The fourth is to recover as much of
the wasted heat as possible to be reused in the process. This can be done by adding or
improving heat exchange capabilities within various plant systems. This study focuses
on the last two options.
5
A mid-sized coal-fired power plant operated by Southern Illinois Power Cooperative
hosted this study. The plant has two completely independent systems. Both are typical
Rankine cycles (Moran and Shapiro, 2008), but each has a different type of steam boiler.
Unit 123 has three turbines supplied by a circulating fluidized bed boiler. The other
system, Unit 4, has one turbine supplied by a common pulverized coal boiler. Unit 123
has a total combined capacity of 120 MW and Unit 4 has a capacity of 173 MW.
In completing this study, a few assumptions were made. All monetary savings are based
on $0.04/kWh for the cost of electricity, which is an average cost determined by the
power plant. All payback periods are based on simple accrual at 0% interest. Flue gas
temperatures used in Tasks 3 and 4 are assumed to be constant at 320°F for the entire
year. Turbine calculations in Task 4 – Case 4 assume turbine efficiencies do not change
regardless of how much steam passing through each stage. Calculations in Task 5 are
based on continuous operation at full load as this was the only steady-state data available.
Variable Frequency Drives
Each system in the host power plant consists of many motors, which were analyzed to
determine where energy could be saved. Auxiliary power is the amount of power used by
these motors and other devices during the power generation process. This generally
includes blowers for air and pumps for working fluid and cooling water. A reduction in
auxiliary power can translate into significant energy savings. This can be accomplished
by installing VFDs on motors. VFDs are used to control the speed of a motor’s shaft.
Prime candidates for VFDs are motors powering devices whose fluid flow output varies
over time or motors powering devices that spend much of their time operating at
conditions that are below the design load.
There are three main types of VFDs: mechanical, hydraulic, and electrical (Saidur et al.,
2011). This study utilizes electrical VFDs, which work by taking typical 60 Hz AC
electricity, converting it to DC electricity, and then discharging pulses of energy that
resemble AC electricity, but at lower frequencies (Dieckmann et al., 2010a) as shown in
Figure 1. The solid blue line represents 60 Hz AC typically supplied to motors and
colored blocks represent electrical pulses output from the VFD to motors with blue
blocks at 60 Hz and orange blocks at 40 Hz. These electrical pulses are in the form of a
sine wave at differing frequencies, causing the motor to run at a different speed. When
an AC motor is powered with energy at a lower frequency, it slows down allowing for
significant energy savings. Figure 2 is a schematic of a VFD system with 60 Hz AC
power entering a control box where it is converted to DC power before pulses of
electrical energy in the form of a sine wave are sent to the motor (Battish, 2011). There
is also a “reference” control loop that measures a desired parameter such as motor speed,
flowrate, temperature, etc. and then sends control signals to the VFD.
It is estimated that 60% of US power generation is used for electric motors representing a
large potential market for VFD use (Lönnberg, 2007). Heating and cooling systems have
utilized VFDs on smaller motors for variable speed compressors and blowers and reduced
6
energy usage by about two-thirds (Dieckmann and Brodrick, 2010). Recently, cost and
reliability issues that had previously limited VFD use on large motors in many power
generation applications have been remedied. For example, electrical currents would
travel down the motor’s shaft and discharge through lubricant to bearings causing
lubricant breakdown and electrical pitting on bearing surfaces leading to vibrations and
eventual failure (Bloch, 2010). This has been fixed by electrically grounding the shaft.
Much of the VFD operation is not a simple linear relationship due to many complex
variables (Sun et al., 2013), which caused control issues. Control schemes have
improved, but previous methods of control are often left in place as a fail-safe option.
Figure 1: Sample of VFD Transformed Sine Wave (Achelpohl, 2014)
Figure 2: VFD Set-up Diagram
In pumping applications, a motor and pump are designed for maximum expected load;
however, the normal operating load is often much lower than the design load (Dieckmann
et al., 2010b). Because the desired load is lower than the design load, many facilities will
throttle the fluid by means of a valve, inlet guide vane, or damper (Bhaduri, 2001). This
could be compared to driving a car with one foot depressing the accelerator so the engine
-5000
-4000
-3000
-2000
-1000
0
1000
2000
3000
4000
5000
0 0.005 0.01 0.015 0.02 0.025 0.03
Vo
lts
Seconds
VFD 60 Hz VFD 40 Hz AC 60 Hz DC
7
runs at maximum power and then controlling the vehicle’s speed by applying brakes.
Using a VFD to control motor speed is akin to controlling vehicle speed using the
accelerator pedal instead of the brake pedal.
The energy saved by slowing a motor down can be proven with the affinity law. This law
states that the minimum amount of power required to generate flow varies with the cube
of the pumped fluid’s flowrate (Bernier and Bourret, 1999). For example, if flowrate is
lowered from 100 cfm to 50 cfm, the power requirement theoretically drops to 1/8th
the
original power (Su, 2011). While this is the ideal, a cubic relationship is not completely
accurate due to losses in the VFDs themselves plus the fact that pumps’ and motors’
efficiencies will vary at different speeds. Instead of assuming the cubic relationship,
which can result in overestimating savings by 7-74% depending on the size of the motor
(Bernier and Bourret, 1999), this study involves a more detailed energy analysis that
incorporates changes in efficiency for both motor and VFD at each load level.
Energy losses due strictly to the VFD’s function are nominally 1.8% (Ramey, 2012).
Even with these losses, reducing a fan’s speed, even if only 15-20%, can result in
significant energy savings. Another benefit of VFD controls is they allow for softer starts
(Phillips, 2004) when a motor uses significantly more than normal operating power.
Softer stops and slower motor speeds can also reduce vibrations, noise level, and
maintenance (Eisenhauer and Williams, 2011). Figure 3 shows power usage for a VFD-
controlled motor versus that of the same motor operating with 60 Hz AC electricity and
flow being throttled by a control valve with the difference being the amount of energy
that could be saved by using a VFD. The VFD power takes into account the minimum
pumping power needed (affinity laws), the efficiency of the motor, and the efficiency of
the VFD itself. The total amount of energy savings will vary based on the application.
Figure 1: VFD vs. Valve Control Power Comparison (Bhaduri, 2001)
8
Improved Heat Exchange
Coal-fired power plants have many areas in which heat may be recovered, such as
economizers, feedwater heaters, and super heaters. Improving heat exchange in older
plants may be accomplished with newer, more efficient heat exchangers or by increasing
the size of the heat exchanger. This study considers recovering additional heat in the flue
gas stack by means of a heat exchanger that condenses water moisture from the exhaust,
hereinafter called a condensing heat exchanger. This technology is similar to that used by
a high efficiency condensing furnace in a residential home.
When higher efficiency furnaces were introduced in 1979, non-condensing furnaces with
a burner had a maximum efficiency of around 60%. Pulse furnaces, which generated a
spark for combustion (as opposed to using a pilot light) and an automated damper,
operated at near 80% efficiency. High efficiency furnaces entered the market with an
efficiency of greater than 82% (Brodrick and Moore, 2000) and condensing furnaces
today can reach efficiencies upwards of 90%.
As seen in Figure 4, a high efficiency furnace actually has two heat exchangers, a
primary and a secondary. The primary heat exchanger is very similar to the heat
exchanger in normal furnaces. The secondary heat exchanger must be made of a material
that will withstand the corrosion caused by condensed water, yet is still thermally
conductive. Different alloys of stainless steel were originally used in residential furnaces,
but more recent furnaces use non-metal coatings to protect areas where condensation
occurs (Brodrick and Moore, 2000).
Figure 2: Diagram of a Typical High Efficiency Condensing Furnace (Formisano, 2014)
9
These same condensation problems are seen in the flue gas of a power plant. Flue gas
from coal firing contains different chemicals than flue gas from natural gas firing. It is
required to go through pollution control devices where it can condense into a liquid
containing corrosive chemicals such as sulfuric acid that will damage unprotected
surfaces very quickly. If heat exchange will result in condensation, the heat exchanger
must be protected as well as the stack itself. Special alloys and composites comprised of
different combinations of nickel, phosphorus, and copper have proven to protect against
corrosion from flue gas condensate (Liu et al., 2010). Teflon has been applied to the
outside of heat exchanger tubes during their production. Fiberglass reinforced plastic is
commonly used to protect non heat exchanging surfaces such as the stack itself.
If heat (energy) is to be recovered, it should be utilized. Typically heat recovered from
flue gas is low grade heat, which can limit its usability. The Lindal diagram in Figure 5
shows many industrial processes that are capable of utilizing low grade heat. Thus, one
option for using recovered heat is to sell it to an industrial processing plant. An abundant
supply of low grade heat could be an incentive for a company to build such a plant next
to the power plant.
Figure 3: Lindal Diagram (Colorado Geological Survey, 2011)
10
Within the plant a few potential uses of the energy are preheating combustion air, coal
drying, heating feedwater, or running an organic Rankine cycle (ORC). The first two
options would reduce the amount of coal input needed while producing the same amount
of power; the latter two would allow for additional electricity to be generated.
In terms of their thermodynamic process, ORCs are essentially the same as a typical
steam Rankine cycle with the only difference being the working fluid. Instead of water,
an organic working fluid, such as a refrigerant that boils at a much lower temperature but
at the same pressure, is used to drive a turbine. ORC’s can utilize heat as low as 165°F
making them an ideal use for low grade heat. The cost of an ORC system ranges from
$1,300 to $3,000 per kilowatt (Arvay et al., 2011). Pay back periods have been as low as
2.5 years; however, this is assuming an electrical cost of $0.15/kWh. Electrical costs this
high are typically only found in Europe or in residential areas. Using the power plant’s
cost of $0.04/kWh to supply power, the payback period would be much longer.
EXPERIMENTAL PROCEDURES
TASK 1: Document Cost of and Energy Savings from Initial VFD Installations
An earlier project supported by the State of Illinois added VFD controls to two forced
draft blowers (4000 HP each) and two booster blowers (3000 HP each) on Unit 4 at the
Lake of Egypt power plant. Installation cost data was provided by the utility company.
To document energy savings, electrical current data for each motor was collected prior to
VFD installation as well as after installation. Current was used because the plant does
not record power used by motors. Due to the timing of air tube repairs that altered
airflow and power required by these blower motors, only 8.5 months of data was accurate
prior to VFD installations. A full year of data was collected post VFD installation.
With this data, a relationship between power used by each fan and total power produced
by Unit 4 was created both pre-VFD and post-VFD as shown in Figure 6, which is a
sample of the data for Forced Draft Blower A. While a clear trend is seen in the data,
there is some spread. Prior to VFD installation, this was likely due to weather changes.
Weather changes were also a factor post-VFD installation, but changes in operators likely
contributed as well.
The amount of time spent operating at various output levels was also analyzed. As seen
in Table 1, the largest percentage of operating time for Unit 4 was at 78% of full load.
As previously discussed, operating at less than full load for extended periods of time
allows for significant energy savings potential.
11
Figure 4: Sample Data from Forced Draft Blower A
Table 1: Typical Unit 4 Operation
Unit 4
Gross MW
% of Max
Unit 4
Output Hours
% of
Operating
Year
110 61% 9 0%
115 64% 1 0%
120 67% 634 7%
125 69% 246 3%
130 72% 87 1%
135 75% 98 1%
140 78% 2555 29%
145 81% 493 6%
150 83% 358 4%
155 86% 299 3%
160 89% 269 3%
165 92% 303 3%
170 94% 431 5%
175 97% 1005 11%
180 100% 592 7%
Total 7380 84%
12
Energy savings was determined by comparing actual energy used by each motor with
what energy usage would have been with VFDs during the period of data collection prior
to VFD installation. Using Equation 1, power usage was calculated for every hour of
data for both the actual pre-VFD motor current and a post-VFD motor current calculated
using the previously determined relationship between power used and power generated.
The power factor for a typical three-phase motor is about 0.9, while a motor controlled
with a VFD has a power factor of 1.0. Large motors at the plant operate at 4160 V.
√ ( ) ( ) (1)
The difference between the two calculated powers is the amount of power saved. These
savings were added up for the full 8.5-month period of data collection prior to VFD
installation and then extrapolated to a full year. An estimate of $0.04/kWh was assumed
for monetary calculations. Table 2 illustrates the procedure for one motor.
Table 2: Example of Task 1 Procedure
TASK 2: Identify Additional VFD Applications Based on Energy Savings and Cost
The procedure for this task is much more involved than the analysis done in Task 1 due
to so much data available for other motors and the lack of post-VFD data for any of these
motors. Motors considered for VFD application fit the criterion that a VFD generates
significant savings for motors operating in throttled applications or that are rarely at full
load. Motors fitting these operating conditions include primary, secondary (over-fire),
and induced draft (ID) air blowers for the circulating fluidized bed boiler (Unit 123) as
well as condensate and boiler feed pumps for Unit 4. For each motor, one year
(excluding shut-down periods) of fluid flowrate data was collected and compiled and then
a flowrate profile in 5% increments that spans a full year was created. Then energy use
was calculated at each flowrate for two scenarios - without a VFD and with a VFD.
A sample of the first scenario for one motor is shown in Table 3. The “% Motor Power
Needed” column is based on a curve fit to a motor that has been throttled similar to that
shown in Figure 6. The amount of power a motor uses drops slightly when its load is
reduced by throttling, thus creating this curve. The power used at each condition for the
entire year is then calculated using Equation 2 to create the final column.
Plant Gross
MW Produced
Motor
(amps)
Energy Used
Hourly (kW)
Motor
(amps)
Energy Used
Hourly (kW)
Energy Used
Hourly (kW) Cost ($)
200 450 2893 317 2260 633 25.31$
175 419 2693 284 2024 669 26.76$
150 388 2493 250 1787 706 28.22$
125 357 2293 217 1551 742 29.68$
100 326 2093 184 1315 778 31.13$
Pre-VFD Post-VFD Savings
13
Table 3: Sample Calculations for Primary Air Blower without VFD
( ) ( )
( ) (
) (2)
The approach for the scenario with a VFD incorporated all of the different efficiencies
from the line to the pump as shown in Figure 7.
Figure 5: VFD System Efficiencies (Bernier and Bourret, 1999)
A sample of the second scenario for the same motor is shown in Table 4. Calculations
incorporate the same flow profile as the first scenario so that the same operational year is
compared. The “Minimum Power WRT Full Load” column refers to the minimum
theoretical power needed to pump the fluid at that condition based on affinity laws (WRT
means “with respect to”), which is essentially the power required at the shaft going into
the pump.
( ) (3)
Values in this column are then divided by the motor’s efficiency at that pumping flowrate
or motor speed to produce the value in the “Power into Motor WRT Full Load” column
as seen in Equation 4. This is the power necessary in the wires going into the motor.
(4)
% of
Design
Flow
% Hours of
Operation
% Motor
Power
Needed
Existing annual
non-VFD energy
use (kWh)
50% 2% 82% 309,357
55% 5% 84% 833,643
60% 6.9% 87% 1,204,590
65% 26.2% 89% 4,640,489
70% 40.8% 90% 7,387,730
75% 16.7% 92% 3,093,132
14
This value is then divided by the “VFD Efficiency at Condition” to give the “Power into
VFD WRT Full Load” as seen in Equation 5. This is power going into the actual VFD.
(5)
This value is finally used in Equation 6 to calculate the total energy used at this operating
condition over the operating year.
( ) ( )
( )
(6)
Table 4: Sample Calculations for Primary Air Blower with Proposed VFD
For both scenarios, total energy for all conditions over the operating year is summed.
The difference between these two summations is the total savings if a VFD were to be
installed on the motor.
TASK 3: Calculate Increase in Efficiency by Using Energy from Exhaust Gases
The objective of this task was to determine the overall increase in plant efficiency if
additional heat were to be recovered from the flue gas. Unit 4 flue gas was not
considered as it has a scrubber and other emissions equipment that lowers flue gas
temperature to near 120°F. Flue gas from the Unit 123 CFB is regularly near 320°F
allowing for a large amount of potential heat recovery.
Calculating the overall increase in efficiency required determining coal cost and energy
content, as any energy recovered would directly result in a reduction of coal use when
determining monetary savings. The amount of energy required per unit of electrical
power (MW) produced by the plant and typical flue gas flowrates were also required.
Thermophysical properties of air were obtained from Engineering Equation Solver
(EES). Recovered energy was calculated using Equation 7 and then multiplied by the
cost and energy content of coal ($2/MBtu) to determine hourly savings.
( ) ( ) (7)
% of
Design
Flow
% Hours of
Operation
Minimum
Power WRT
Full Load
Motor
Efficiency at
Condition
Power into
Motor WRT
Full Load
VFD
Efficiency at
Condition
Power into
VFD WRT
Full Load
New energy use
using hours of
operation (kWh)
50% 2% 12.1% 84.5% 14.3% 89.5% 16% 59,960
55% 5% 16.1% 89.5% 17.9% 92.3% 19% 191,885
60% 6.9% 20.9% 92.4% 22.6% 93.9% 24% 334,728
65% 26.2% 26.5% 93.9% 28.3% 94.7% 30% 1,562,471
70% 40.8% 33.1% 94.8% 35.0% 95.2% 37% 2,997,514
75% 16.7% 40.8% 95.5% 42.7% 95.5% 45% 1,497,768
15
The efficiency increase of the plant with respect to the nominal efficiency can be found
using Equation 8 where energy recovered (see Equation 7) is divided by the current
efficiency of the cycle (12,000,000 Btu/hr/MW) and then divided by the average energy
generation of the plant.
( ) (
)
(
) ( )
(8)
TASK 4: Determine How to Utilize Heat Recovered from Exhaust Gases
The objective of this task was to determine at what temperature flue gas condenses and
how to best recover and utilize the wasted energy found in Task 3. This required an
energy analysis to determine feasible temperatures of a run-around loop obtained by
transferring recovered energy from the flue gas. Then five cases were examined to
determine their ability to utilize the recovered heat and to assess their economic
feasibility. Case 1 considered selling the waste heat to a nearby manufacturer. Case 2
used the heat to help preheat combustion air going into the boiler. Case 3 utilized the
heat in a coal dryer. Case 4 transferred the heat to the lowest pressure feedwater heater to
reduce the amount of steam extracted from the turbine. Case 5 used the heat to power an
organic Rankine cycle (ORC).
A condensing flue gas heat exchanger was discussed with a qualified consultant and it
was determined that the project is possible (Burch, 2014). It has rarely been implemented
in coal-fired power plants due to the low cost of coal and the fact that flue gas from a
coal-fired boiler has less latent heat content than flue gas from other fuels; however, there
is still a significant amount of recoverable energy. One possible configuration is shown
in Figure 8. The heat exchanger would be Teflon-coated and the stack would be
fiberglass-reinforced plastic to protect them from corrosive condensation.
Each case requires a condensing heat exchanger in the exhaust stack to recover energy
from the flue gas as well as a loop containing a fluid, likely water, to transfer the
recovered heat from the stack heat exchanger to the area of the plant in which it will be
utilized. A schematic of the proposed system is shown in Figure 9.
Case 1: Selling Waste Heat to a Nearby Manufacturer
This case pumps the recovered heat by means of a run-around loop to a nearby industry
plant of some sort. For this case, the utility company would need to lure a manufacturer
to build nearby the power plant. This manufacturer would be one that typically acquires
heat needed for processes by burning natural gas. Potential industries that may be
interested in purchasing the waste heat are identified in Figure 5.
16
Figure 6: Condensing Heat Exchanger (Condensing Heat Exchanger Corp., 2014)
Figure 7: Schematic of System to Distribute Recovered Waste Heat
17
Case 2: Preheating Combustion Air
This case utilizes the recovered heat in a heat exchanger to preheat combustion air prior
to entering the boiler. Currently steam is used to preheat air so that it will not condense
on any of the injectors. If recovered heat is used to preheat air, this steam could instead
be sent through the turbine to create additional power.
The proposed system incorporates a liquid-to-air heat exchanger similar to an
economizer; however, instead of air heating liquid, liquid heats combustion air with
energy recovered from the stack. For this case, a full energy analysis was completed
using EES to determine how much heat could actually be transferred to combustion air.
Calculations began by determining how much energy could be recovered from the flue
gas (Equation 7). Knowing the difference in enthalpies required, a stack exit temperature
leaving the proposed condensing heat exchanger of 200°F was chosen based on what
would be a feasible effectiveness of the air-to-water heat exchanger and knowing that the
stack temperature is regularly at 320°F.
Next, the flowrate of the heat transfer fluid loop was calculated using Equation 9. The
temperature of the fluid entering the stack heat exchanger is 130°F, which was chosen
based on having at least 50°F difference between the stack exit temperature and the
temperature of the ambient air that will be heated. Thus, the temperature of the fluid
leaving the condensing heat exchanger is 260°F based on a feasible effectiveness of heat
exchange between this fluid loop and the combustion air.
(
)
(
)
(
)
(9)
Finally, the enthalpy of heated air was determined using Equation 10. Using this
thermophysical property, the preheated combustion air temperature was determined.
(10)
Case 3: Drying Coal
This case utilizes the recovered heat in a coal dryer to reduce the moisture content of coal
entering the boiler for combustion. This results in a decrease in the total amount of coal
needed to produce the same amount of power. Data regarding the amount of waste heat
available and its temperatures were sent to Carrier Vibrations Inc. for a project quote and
analysis of potential improvements to coal quality.
Case 4: Heating Feedwater
This case transfers the recovered heat to the lowest pressure feedwater heater of Unit 4’s
steam cycle. Feedwater entering the heater is at 106°F and the hot water from the
18
condensing heat exchanger was predicted to be at 260°F. Equation 11 shows how the
total heat requirement of the heater was found. Steam is typically extracted from the
turbine and used to heat the feedwater. By using recovered energy to heat the feedwater
instead of steam, the steam is instead passed through the final stages of the turbine to
create additional power. Equation 12 was used to determine the flowrate of additional
steam available to pass through the turbine and to determine how much power is made.
(
) ( ) (11)
(
)
( ) ( ) (12)
Case 5: Organic Rankine Cycles
This case makes use of the recovered heat by powering an organic Rankine cycle (ORC).
The additional power made by the ORC is then sold for profit. The ORC would be
purchased as a complete system and all energy calculations were completed by the
manufacturer. A typical ORC system schematic is shown Figure 10. Data regarding
stack temperatures and flowrates were collected and provided to the manufacturer to
complete their analysis.
Figure 8: Schematic of Typical ORC (Hattiangadi, 2013)
19
TASK 5: Examine Heat Exchangers at the Plant
Based on a recommendation from the company hosting the study, low- and high-pressure
feedwater heaters on Unit 4 were evaluated for potential to increase the plant’s overall
efficiency by making improvements to them. Analysis of these heaters required an in-
depth study of Unit 4’s entire steam cycle, which is shown in Figure 11.
In Unit 4, the main steam from the boiler first enters the high-pressure turbine where the
first amount of steam is extracted and the remaining steam continues back through the
reheat cycle. After the reheat cycle, steam enters the intermediate pressure turbine where
the second amount of steam is extracted at two different stages and the remaining steam
finishes through the turbine before entering the low pressure turbine. Here the working
fluid splits in opposite directions with multiple extraction points. Once the steam has
been expanded to its lowest pressure, it enters the condenser where it is then condensed.
At this point the working fluid is referred to as condensate, until it reaches the deaerator,
after which it is referred to as feedwater.
Low- and high-pressure feedwater heaters are similar to that seen in Figure 12. Each
extraction steam line is piped to one of the feedwater heaters. The extraction steam then
condenses within the heater as it transfers heat to the condensate/feedwater. The
condensation from the extraction steam collects at the bottom of the heater to maintain a
consistent level that is monitored. This condensate leaves the heater through a drip line
where it passes through a valve lowering the pressure to that of the lower heater and the
drips partially consist of vapor. This vapor then joins the next lower pressure extraction
steam in the subsequent heater.
To properly analyze each heater, data was collected regarding steam, feedwater, and
condensate flowrates as well as temperatures and pressures at each necessary state point.
This data is seen in Table 5. The entire cycle was then modeled using EES.
Calculations in the software included results of effectiveness of each heater as well as the
turbine efficiency at each steam extraction point. Effectiveness was defined as the actual
amount of heat transferred (Equation 13), compared to the maximum amount of heat
transfer possible (Equation 14). The maximum heat transfer was defined as the enthalpy
difference between saturated steam and entering feedwater. Effectiveness was then the
ratio between the actual and maximum heat transfers (Equation 15). Turbine efficiencies
were calculated using classic methods based on the actual drop in enthalpy compared to
the isentropic drop in enthalpy (Equation 16).
( ) (13)
( ) (14)
(15)
(16)
20
Figure 9: Unit 4 Steam Cycle
21
Figure 10: Diagram of a Typical Closed Feedwater Heater (Moran and Shapiro, 2008)
Table 5: Feedwater Heater State Point Data
RESULTS AND DISCUSSION
TASK 1: Document Cost of and Energy Savings from Initial VFD Installations
The total savings in terms of power and dollars resulting from the initial VFD installation
project is seen in Table 6. Figure 13 shows total costs for the installation broken down by
project cost category. State and federal government grants provided $2 million of the
total $2.9 million cost of the project. This resulted in a simple payback period of
approximately one year; without grants the simple payback period would be just over
three years. The initial VFD installations have now been in operation for three years
without any major maintenance issues.
State
Point Description
Temperature
(°F)
Pressure
(psia)
Flowrate
(kpph)
12 Entering lowest pressure feedwater heater 4-1 106 91.7 911
13 Entering feedwater heater 4-2 156 108.7 911
14 Entering feedwater heater 4-3 195 105.7 911
15 Entering Deaerator 266 81.7 911
16 Entering feedwater heater 4-5 320 2408 1414
17 Entering feedwater heater 4-6 355 2215 1414
22
Table 6: Total Savings of Task 1
Figure 11: Project Cost Breakdown
TASK 2: Identify Additional VFD Applications Based on Energy Savings and Cost
After completing a detailed energy analysis, energy saving results for VFD installations
on five additional motors is shown in Table 7. Due to a lack of flowrate data for the ID
blower, calculations for this motor are a conservative estimate based on combined
flowrates of primary and secondary air blowers. If operating flowrate were available for
the ID blower, a more detailed analysis could suggest savings of as much as $410,000
annually. Operating hours in a year vary slightly due to differences in years that the data
was collected. There is also a difference between Unit 123 and Unit 4 in the amount of
time spent in shut-down periods. Data for primary, secondary, and ID air fans was
collected while Unit 123 was operating above 80 MW, and data for pumps was collected
while Unit 4 was operating above 100 MW. Total energy savings for the proposed VFD
installations is 38.5 GWh, which amounts to approximately 2.05% increase in overall
cycle efficiency. All monetary savings were evaluated based on a $0.04/kWh.
Annual savings kWh
$ (assuming
$0.04/kWh)
FD A 5,489,277 219,571
FD B 5,992,786 239,711
Booster A 5,652,144 226,086
Booster B 5,626,483 225,059
Total 22,760,690 910,428
23
Table 7: Summary of Task 2 Savings
A summary of total project costs for Task 2 can be seen in Table 8. Housing costs for
VFDs will vary based on the space in which they are placed. A quote from a nearby
contractor was obtained for a 416 square foot building for housing VFD for the three
blowers for the CFB if there is adequate space available, otherwise each could be housed
individually. Each VFD requires two feet of overhead clearance for ventilation and three
feet of clearance around the unit for maintenance. Clearance space around VFDs could
be shared if two VFDs were placed facing each other. A factory authorized start-up and
testing procedure must be completed on each installed VFD and will take a minimum of
four days per VFD. Project management and engineering costs were scaled from the
previous project analyzed in Task 1. VFD prices and startup costs were quoted by a local
electrical equipment supplier (Baker, 2014). With a total cost of about $2.5 million, the
project has a simple payback period of less than two years.
Table 8: Summary of Task 2 Project Costs
TASK 3: Calculate Increase in Efficiency by Using Energy from Exhaust Gases
Task 3 results show that for every 1°F reduction of the flue gas temperature by means of
heat recovery that is reused elsewhere in the cycle, 2,000 MMBtu of coal is saved
VFD Cost
Motor MWh $ MWh $ MWh $ % $
PRIMARY AIR 3500 7670 17,951 718,030 6,925 277,003 11,026 441,026 61% 412,000
SECONDARY AIR 1000 7552 4,933 197,309 1,628 65,133 3,304 132,175 67% 197,500
ID BLOWER 3500 7553 18,352 734,098 10,997 439,873 7,356 294,225 40% 412,000
BOILER FEED (A) 3000 7390 15,334 613,356 8,541 341,629 6,793 271,727 44% 412,000
BOILER FEED (B) 3000 7390 14,945 597,795 6,721 268,839 8,224 328,956 55% 412,000
CONDENSATE 600 7233 2,882 115,260 1,120 44,813 1,761 70,447 61% 185,000
Total 14,600 38,464 1,538,556$ 2,030,500$
Blo
wer
sPu
mps
Pre VFD Post VFD SavingsOperating
Hours
Power
(hp)
Project Summary Unit Cost Unit Size (HxWxD)
Primary Air 412,000$ 103.7x174x49.5 in.
Secondary Air 197,500$ 103.7x122x43.4 in.
ID Fan 412,000$ 103.7x174x49.5 in.
Boiler Feed (A) 412,000$ 103.7x174x49.5 in.
Boiler Feed (B) 412,000$ 103.7x174x49.5 in.
Condensate 185,000$ 103.7x48x48 in.
VFDs Sub-Total 2,030,500$ -
Project Management and
Engineering 300,000$ -
Testing for Suitabliity on Boiler Feed
Water Pumps ($15,000 per pump) 30,000$ -
Structure to House VFDs (Primary,
Secondary, and ID Air Blowers only) 32,000$ 11x26x16 ft.Startup Procedure ($12,000 per VFD) 60,000$ -
Project Total 2,452,500$ -
VFD
Info
A
ddit
iona
l Co
sts
24
annually. Heat recovery resulting in a 120°F reduction, as suggested in Task 4, amounted
to a 2.54% increase in cycle efficiency, as shown in Figure 14. This is approximately a
0.87% increase in total plant efficiency.
Table 9: Savings Relative to Temperature Reduction
Figure 12: Plant Efficiency Gains by Stack Temperature Reduction
Exhaust gas
lowered by (°F)
Annual Coal
Cost Saved
10 40,054$
20 80,075$
30 120,064$
40 160,020$
50 199,946$
60 239,841$
70 279,708$
80 319,547$
90 359,359$
100 399,145$
110 438,906$
120 478,643$
25
A system in which flue gas enters another heat exchanger, similar to a second
economizer, and partially condenses prior to leaving the stack was determined to be
suitable for this application. There are very few manufacturers of heat exchangers
capable of withstanding the corrosive nature of coal flue gas condensate. Condensing
Heat Exchanger Corp. makes a system in which the heat exchanger tubes are coated in
Teflon and the exhaust stack is made of fiberglass-reinforced plastic to withstand the
corrosive condensate. They determined a cost estimate of approximately $2 million
(Brooks, 2014) for a system of suitable size for the power plant evaluated in this project.
TASK 4: Determine How to Utilize Heat Recovered from Exhaust Gases
Case 1: Selling Waste Heat to a Nearby Manufacturer
Task 3 results showed that there would be approximately 2.4 million therms available to
sell annually. Over the past five years, the industrial cost of natural gas has varied from
$0.34 to $0.75 per therm, averaging around $0.53 per therm. This equates to $1.27
million if the plant were able to sell all of the recovered heat to a nearby industry at a
similar price. Total cost was almost $3 million with the heat exchanger being the majority
of the cost as shown in Table 10. It is unlikely a company could be lured to build next to
the plant if the energy were to be sold at market cost; thus, assuming the plant could sell
the energy at 50% of market value, the payback period would be 4.6 years.
Table 10: Case 1 (Selling Energy) Project Material Costs
Case 2: Preheating Combustion Air
Parametric tables in EES allowed for determination of recovered heat quantities that were
then transferred to the combustion air. This process suggests that it is practical to recover
heat from the stack resulting in the stack temperature dropping from 320°F to 200°F.
This amount of recovered energy allows for combustion air to be preheated from 70°F to
190°F resulting in a yearly savings of 244 MMBtu in coal usage. At present, the plant
requires 12 MMBtu per MWhr produced. With the energy recovered in this case, the
heat requirement for one MWhr drops to 11.7 MMBtu, an improvement of 2.54%. Total
cost was about $3.3 million with annual savings of nearly $410,000 resulting in an 8.1-
Part/Model Supplier Deliverable Quantity Cost
Condensing Heat Exchanger Condensing Heat Exchanger Corp 30 mmBTU/hr 1 2,000,000$
Pump, Centrifugal, CI, 15 HP,
3CCW3 Grainger
350 GPM (125
FT of head) 2 7,600$
3 in. Standard-Wall Black Steel
Threaded Pipe (4457K67) McMaster-Carr 10.5 FT 115 22,658$
Pipe Insulation, Seam-Seal, 3
1/2 In, 6 Ft (2CKP7) Grainger 6 Ft 202 11,595$
Low-Pressure Pipe Couplings
(44605K82) McMaster-Carr 3 in. 115$ 4,309$
Estimated Installation 842,325$
Total 2,888,487$
26
year simple payback period. A summary of material costs is provided in Table 11
showing that the heat exchanger is the major cost.
Table 11: Case 2 (Preheating Air) Project Material Costs
Case 3: Drying Coal
A quote from Carrier Vibrating Equipment indicates that drying coal with recovered heat
could upgrade the coal from 11,000 Btu/lb to 11,740 Btu/lb (Mueller, 2014) with
moisture content reduced from 11% to 5%. This results in coal use being lowered by
almost 50,000 tons/year. A 13'-10" wide x 33'-0" long stationary fluidized bed with in-
bed heat exchangers was quoted for this project. The cost of the coal dryer and some
auxiliary equipment such as supply and exhaust fans was $1.45 million. Total cost
including the run-around loop and condensing heat exchanger was about $4.8 million as
shown in Table 12 and additional operating costs for pumps and fans was approximately
$180,000/year. Net annual savings amounted to nearly $2.28 million resulting in a 2.1-
year simple payback period.
Table 12: Case 3 (Drying Coal) Project Material Costs
Part/Model Supplier Deliverable Quantity Cost
Condensing Heat Exchanger Condensing Heat Exchanger Corp 30 MBTU/hr 1 2,000,000$
Air Preheater/Heat Exchanger *estimated 30 MBTU/hr 1 173,125$
Pump, Centrifugal, CI, 15 HP,
3CCW3 Grainger
350 GPM (125
FT of head) 2 7,600$
3 in. Standard-Wall Black Steel
Threaded Pipe (4457K67) McMaster-Carr 10.5 FT 38 7,487$
Pipe Insulation, Seam-Seal, 3
1/2 In, 6 Ft (2CKP7) Grainger 6 Ft 67 3,846$
Low-Pressure Pipe Couplings
(44605K82) McMaster-Carr 3 in. 38 1,424$
Estimated Installation 1,136,964$
Total 3,330,445$
Part/Model Supplier Deliverable Quantity Cost
Condensing Heat Exchanger Condensing Heat Exchanger Corp 30 MBTU/hr 1 2,000,000$
Coal Drying System Carrier Vibrating Equipment, Inc.
108 tons/hr
of coal 1 1,450,000$
Pump, Centrifugal, CI, 15 HP,
3CCW3 Grainger
350 GPM (125
FT of head) 3 11,400$
3 in. Standard-Wall Black Steel
Threaded Pipe (4457K67) McMaster-Carr 10.5 FT 48 9,457$
Pipe Insulation, Seam-Seal, 3
1/2 In, 6 Ft (2CKP7) Grainger 6 Ft 84 4,822$
Low-Pressure Pipe Couplings
(44605K82) McMaster-Carr 3 in. 48 1,799$
Estimated Installation 1,304,955$
Total 4,782,433$
27
Case 4: Heating Feedwater
Heat recovered from the flue gas stack is equivalent to 73% of the heat currently supplied
to the lowest pressure feedwater heater. Using it for that purpose allows additional steam
to pass through the low-pressure turbine. Determining the efficiency of final stages of
the turbine was difficult due to uncertainties about the quality of fluid leaving the turbine
so an efficiency of 70% was assumed based on other nearby stages. The additional steam
passing through the turbine generated an additional 0.522 MW of electrical power. Total
cost was about $3.4 million as shown in Table 13 with annual savings of nearly $170,000
resulting in a 20.1-year simple payback period.
Table 13: Case 4 (Heating Feedwater) Project Material Costs
Case 5: Organic Rankine Cycles
Two manufacturers provided quotes for an ORC system. The first manufacturer, Infinity
Turbine, offered ORCs with radial turbines, identified herein as Turbine A. Their largest
was the IT250 Radial Outflow Turbine. It has a maximum output of 0.25 MW and
utilizes 11 MMBtu of heat input. With about 30 MMBtu available, three of these
systems would be needed at a cost of $500,000 each (Giese, 2014). Total cost for a
Turbine A system was about $4.8 million with annual savings of nearly $240,000
resulting in a simple payback period of 20.1 years.
The second manufacturer, Transpacific Energy, offered an ORC system with an axial
turbine, identified herein as Turbine B. Their quote was for a system costing $3 million
that provides a gross power output of 1 MW (Sami, 2014). Total cost for a Turbine B
system was about $6.8 million with annual savings of nearly $320,000 resulting in a
simple payback period of 21.3 years. A summary of project costs for both Case 5 options
is provided in Table 14.
Part/Model Supplier Deliverable Quantity Cost
Condensing Heat Exchanger Condensing Heat Exchanger Corp 30 MBTU/hr 1 2,000,000$
Plate Heat Exchanger RS Means 2200 GPM 1 165,000$
Pump, Centrifugal, CI, 15 HP,
3CCW3 Grainger
350 GPM (125
FT of head) 2 7,600$
3 in. Standard-Wall Black Steel
Threaded Pipe (4457K67) McMaster-Carr 10.5 FT 95 18,718$
Pipe Insulation, Seam-Seal, 3
1/2 In, 6 Ft (2CKP7) Grainger 6 Ft 167 9,586$
Low-Pressure Pipe Couplings
(44605K82) McMaster-Carr 3 in. 95 3,560$
Estimated Installation 1,158,927$
Total 3,363,390$
28
Table 14: Case 5 (ORC System) Project Material Costs
A summary of total cost, predicted annual savings, and payback period for each case is
provided in Table 15. For cases that generate additional power, monetary savings were
determined assuming an electricity cost of $0.04/kWhr. In the other cases, any energy
recovered and reused in the cycle directly resulted in a reduction in the amount of coal
used. Thus, energy content and cost of coal was used to determine monetary savings.
Installation costs for large items such as the condensing heat exchanger, coal dryer, and
ORC systems were assumed to be one-third of the material cost, which is experience with
the large VFD installation project analyzed in Task 1 (Achelpohl, 2014). For all other
materials such as piping, the installation cost was assumed to be equal to the material cost
based on a professional engineer’s recommendation (Green, 2014).
Case 1 requires the lowest investment to implement in terms of total cost; however,
predicted annual savings for Case 3 is clearly superior to the other options and makes it
the option with the shortest payback period.
Table 15: Total Cost and Payback Period for All Cases
Part/Model Supplier Deliverable Quantity Cost
Condensing Heat Exchanger Condensing Heat Exchanger Corp 30 MBTU/hr 1 2,000,000$
Pump, Centrifugal, CI, 15 HP,
3CCW3 Grainger
350 GPM (125
FT of head) 2 7,600$
3 in. Standard-Wall Black Steel
Threaded Pipe (4457K67) McMaster-Carr 10.5 FT 48 9,457$
Pipe Insulation, Seam-Seal, 3
1/2 In, 6 Ft (2CKP7) Grainger 6 Ft 84 4,822$
Low-Pressure Pipe Couplings
(44605K82) McMaster-Carr 3 in. 48 1,799$
Pre ORC Total 2,023,678$
(A) IT250 Radial Outflow
Turbine (x3) Infinity Turbine 0.75 MW 1 1,500,000$
(B) ORC System (Axial Turbine) Transpacific Energy 1 MW 1 3,000,000$
(A) Estimated Installation 1,297,355$
(B) Estimated Installation 1,797,355$
Project Total (A) With Infinity Turbine 4,821,033$
Project Total (B) With Transpacific Energy Turbine 6,821,033$
Case Purpose Total Cost
Predicted Annual
Savings
Payback Period
(years)
Case 1 Selling Energy 2,888,487$ 625,000$ 4.6
Case 2 Preheating Air 3,330,445$ 409,139$ 8.1
Case 3 Drying Coal 4,782,433$ 2,276,144$ 2.1
Case 4 Heating Feedwater 3,363,390$ 167,040$ 20.1
Case 5 (A) ORC 4,821,033$ 240,000$ 20.1
Case 5 (B) ORC 6,821,033$ 320,000$ 21.3
29
TASK 5: Examine Heat Exchangers at the Plant
A temperature versus entropy diagram of the Unit 4 cycle is shown in Figure 15. Results
showing heater effectiveness are provided in Table 16. Each heater’s effectiveness was
examined at full load, as this was where the system operates almost all of the time, and
this was deemed to be adequate. These results show that any changes made to the
existing system would not be economically feasible or prudent.
Figure 13: Temperature vs. Entropy Diagram of Unit 4 Cycle
Table 16: Results of Heater Effectiveness Analysis
Heater Effectiveness
Low Pressure 4-1 0.9615
Low Pressure 4-2 0.9649
Low Pressure 4-3 0.9312
Deaerator 0.9297
High Pressure 4-5 0.7787
High Pressure 4-6 0.8253
1801.1 psia
30
CONCLUSIONS AND RECOMMENDATIONS
VFDs
VFDs were cost effective for all six motors examined.
If there is adequate space, appropriate ambient temperature, and dust control,
all six motors are recommended to be fitted with VFDs.
Waste Heat Recovery
Heat in the flue gas stack is free, but recovering and utilizing it is not free.
A condensing heat exchanger protected from corrosion is expensive, but it is
still a viable option.
Selling recovered heat to a nearby manufacturer or utilizing it in a coal dryer
are the best options and both are worth pursuing further.
Feedwater Heaters
All feedwater heaters in the model facility are working properly and
efficiently.
Many of the temperatures and pressures of drips did not correspond to
saturated conditions. Using the saturation temperature related to the pressure
produced logical results. It is recommended to check temperature sensors and
their locations.
With properly written equations, Engineering Equation Solver (EES) can
automatically calculate turbine efficiencies, effectiveness of heat exchangers,
and quality of steam at any condition and plot results.
ACKNOWLEDGEMENTS
The principal investigator would like to thank the Illinois Clean Coal Institute (ICCI) and
Dr. Hirschi for their funding, support, and assistance during this project. Likewise, the
cooperation and assistance provided by Southern Illinois Power Cooperative (SIPC) in
regards to data collection and knowledge of plant systems, especially the work of Clark
Madden and Scott Achelpohl, is greatly appreciated. Also, the assistance given by Justin
Harrell, Physical Plant Engineer at SIUC, and his background working with variable
frequency drives is sincerely valued and was extremely beneficial in getting the project
started in the right direction. Finally, the principal investigator would like to thank
graduate assistant, Jeff Green, for his efforts with the project.
31
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34
APPENDICES
35
Appendix A: Nomenclature
CFB Circulating Fluidized Bed
cfm cubic feet per minute
Cp Specific heat of feedwater
hin Enthalpy before turbine expansion
hnew Enthalpy of flue gas after losing heat to heat exchanger
horiginal Enthalpy of flue gas prior to heat removal
hout Actual enthalpy after turbine expansion
h'out Ideal enthalpy after turbine expansion
HX Heat exchanger
ICCI Illinois Clean Coal Institute
Flowrate
ηm Efficiency of Electric Motor
ηturbine Efficiency of turbine
ηvfd Efficiency of Variable Frequency Drive
ORC Organic Rankine Cycle
p Efficiency of Pump
Pin Required electrical power going into VFD
Pm Electrical power going into motor
Pshaft Shaft power going into pump
Ptheo Theoretical pumping power
Qactual Actual heat transferred
Qf.w. Flowrate of feedwater
Qthemaxo. Theoretical Maximum heat transferred
Tf.w. in Temperature of feedwater entering heater
Tf.w. out Temperature of feedwater exiting heater
TSat. Ext. Steam Saturation temperature of extraction steam
VFD Variable Frequency Drive
WRT With respect to
36
Appendix B: Variable Frequency Drive Calculator Sample
PR
IMA
RY
AIR
BLO
WER
Thro
ttlin
g C
oe
ffic
ien
ts
76
70
Op
erat
ing
Ho
urs
C0
0.5
52
1C
00
.96
74
11
01
1C
00
.97
$0
.04
0el
ectr
ic c
ost
($
/kW
h)C
10
.63
70
C1
-19
.99
40
27
84
C1
-26
.42
36
10
24
35
00
Mo
tor
Ho
rsep
ow
er (
No
min
al)
C2
-0.1
90
0C
20
.31
54
74
86
C2
0.0
34
02
11
18
60
%P
um
p E
ffic
ien
cy
33
88
.03
Pu
mp
Des
ign
BH
P
(SH
AFT
PO
WER
)W
eigh
t0
.01
LB/G
allo
n
96
.6%
Mo
tor
Effi
cien
cy @
Des
ign
Lo
ad6
5IN
WC
97
%M
oto
r D
esig
n L
oad
89
9K
LB/H
R
75
%M
oto
r Lo
ad B
EP5
.37
5FT
32
72
.83
7D
esig
n L
oad
Mo
tor
Po
wer
14
97
66
6.6
67
GP
M
% o
f D
esig
n
Flo
w
% H
ou
rs o
f
Op
erat
ion
% M
oto
r
Po
wer
Nee
ded
Exis
tin
g an
nu
al n
on
-
VFD
en
ergy
use
(kW
h)
Min
imu
m
Po
wer
WR
T
Full
Load
Mo
tor
Effi
cien
cy a
t
Co
nd
itio
n
Po
wer
into
Mo
tor
WR
T
Full
Load
VFD
Eff
icie
ncy
at C
on
dit
ion
Po
wer
into
VFD
WR
T Fu
ll Lo
ad
New
en
ergy
use
usi
ng
ho
urs
of
op
erat
ion
(kW
h)
Savi
ngs
(Dif
fere
nce
)
0%
0%
55
%0
0.0
%0
.0%
5%
0%
58
%0
0.0
%0
.2%
5.5
%6
3.8
%9
%0
49
.8%
10
%0
%6
1%
00
.1%
1.7
%5
.5%
64
.1%
9%
05
2.8
%
15
%0
%6
4%
00
.3%
5.8
%5
.7%
64
.9%
9%
05
5.6
%
20
%0
%6
7%
00
.8%
13
.1%
5.9
%6
6.4
%9
%0
58
.3%
25
%0
%7
0%
01
.5%
23
.9%
6.3
%6
8.7
%9
%0
60
.7%
30
%0
%7
3%
02
.6%
37
.3%
7.0
%7
2.0
%1
0%
06
2.9
%
35
%0
%7
5%
04
.1%
51
.7%
8.0
%7
6.2
%1
0%
06
4.7
%
40
%0
%7
8%
06
.2%
65
.4%
9.5
%8
0.9
%1
2%
06
6.0
%
45
%0
%8
0%
08
.8%
76
.6%
11
.5%
85
.6%
13
%0
66
.6%
50
%2
%8
2%
30
9,3
57
1
2.1
%8
4.5
%1
4.3
%8
9.5
%1
6%
59
,96
0
6
6.4
%
55
%5
%8
4%
83
3,6
43
1
6.1
%8
9.5
%1
7.9
%9
2.3
%1
9%
19
1,8
85
6
5.0
%
60
%6
.9%
87
%1
,20
4,5
90
20
.9%
92
.4%
22
.6%
93
.9%
24
%3
34
,72
8
62
.5%
65
%2
6.2
%8
9%
4,6
40
,48
9
2
6.5
%9
3.9
%2
8.3
%9
4.7
%3
0%
1,5
62
,47
1
5
8.8
%
70
%4
0.8
%9
0%
7,3
87
,73
0
3
3.1
%9
4.8
%3
5.0
%9
5.2
%3
7%
2,9
97
,51
4
5
3.8
%
75
%1
6.7
%9
2%
3,0
93
,13
2
4
0.8
%9
5.5
%4
2.7
%9
5.5
%4
5%
1,4
97
,76
8
4
7.6
%
80
%2
.3%
94
%4
31
,84
7
49
.5%
96
.0%
51
.5%
95
.8%
54
%2
47
,02
8
40
.2%
85
%0
.2%
96
%4
7,4
22
5
9.3
%9
6.4
%6
1.6
%9
6.1
%6
4%
31
,76
0
3
1.6
%
90
%0
.0%
97
%2
,53
6
7
0.4
%9
6.6
%7
2.9
%9
6.4
%7
6%
1,9
74
2
1.5
%
95
%0
.0%
99
%0
82
.8%
96
.5%
85
.8%
96
.6%
89
%0
9.8
%
10
0%
01
00
%9
6.6
%9
6.1
%1
00
.5%
96
.9%
10
4%
-3.8
%
10
5%
10
1%
11
1.8
%9
5.3
%1
17
.4%
97
.0%
12
1%
-19
.9%
11
0%
10
2%
12
8.6
%9
3.8
%1
37
.1%
97
.0%
14
1%
-39
.0%
11
5%
10
3%
14
6.9
%9
1.6
%1
60
.4%
96
.8%
16
6%
-62
.4%
12
0%
10
4%
16
6.9
%8
8.4
%1
88
.8%
96
.2%
19
6%
-91
.9%
Tota
l1
00
%1
7,9
50
,74
6
6,9
25
,08
7
Co
st7
18
,03
0$
$2
77
,00
3
Savi
ngs
$4
41
,02
6
VFD
En
ergy
Cu
rren
t En
ergy
39
%
Mo
tor
Co
eff
ice
nts
Var
iab
le F
req
ue
ncy
Dri
ve
Co
eff
icie
nts
Dis
char
ge P
ress
ure
Des
ign
Flo
w
Des
ign
Hea
d
Des
ign
Flo
w
37
Appendix C: Pump Inspection Quote
38
Appendix C: Pump Inspection Quote (continued)