The next generation of Lunar rovers and landers requires variable thermal links to maintain payload temperatures nearly constant over wide sink temperature fluctuations. It has been demonstrated on earth that a hot reservoir variable conductance heat pipe (VCHP) can provide a much tighter passive thermal control capability compared to a conventional VCHP with a cold-biased reservoir. However, previous ISS test results revealed that the fluid management of a hot reservoir VCHP needs to be improved to ensure its long-term reliability. Under an STTR Phase I program, Advanced Cooling Technologies, Inc. in collaboration with Case Western Reserve University performed fundamental research to understand the complex transport phenomena within a hot reservoir VCHP. A novel loop VCHP configuration was developed during the program. This loop design allows a net flow to be induced and circulate along the NCG tubing system, which will continuously remove the excessive working fluid from the reservoir (i.e. purging) in a much faster rate compared to diffusion alone. Two potential mechanisms to induce net transport flow were identified:
1. By momentum transfer from vapor to NCG through shearing in the condenser/front region. It was called “DC” mechanism.
2. By filtering the pulses (via a tesla/check valve) generated in the heat pipe section of VCHP loop. It was called “AC” mechanism.
Although these two mechanisms are independent, the AC mechanism can be further added/superimposed on the top of the DC mechanism to achieve a higher flow rate. This paper presents the work performed in Phase I to prove the existence of momentum transfer flow (“DC flow) and its effectiveness on VCHP purging. The work includes theoretical analysis, numerical modeling, prototype development and experimental demonstration.
AC = fluctuating component of the flow within a loop VCHP
DC = constant component of the flow within a loop VCHP
D = diffusion coefficient
LNCG = length of NCG tube
RNCG = internal radius of NCG tube
U = average induced flow velocity
µ = viscosity of NCG
ψ = vapor concentration in the reservoir
Δp = pressure difference between inlet and outlet of NCG tube
NASA’s plans to further expand human and robotic presence in space automatically involve significant challenges. Spacecraft architectures will need to handle unprecedented thermal environments in deep space. In addition, there is a need to extend the duration of the missions in both cold and hot environments, including cis-lunar and planetary surface excursions. The heat rejection turn–down ratio of the increased thermal loads in the above-mentioned conditions is crucial for minimizing the usage of vehicle resources (e.g. power). Therefore, future exploration activities will need thermal management systems that can provide higher reliability and performance, and, at the same time, with reduced power and mass. To meet these requirements, passive thermal management concepts that offer large turn-down ratios are highly encouraged. As an example, the anchor node network (which is a lander that includes a seismometer, a laser reflector, and a probe for measuring heat flow from the Moon’s interior) has a Warm Electronics Box (WEB) and a battery, both of which must be maintained in a fairly narrow temperature range. A variable thermal link between the WEB and radiator is required. During the day, the thermal link must transfer heat from the WEB electronics to the radiator as efficiently as possible, with minimum thermal resistance, to minimize the radiator size. On the other hand, the thermal link must be as ineffective as possible (provide as high thermal resistance as possible) during the Lunar night. This will keep the electronics and battery warm with minimal power, even with the very low temperature (100 K) heat sink. At this time, heat must be shared between the electronics and battery, to keep the battery warm. Moreover, since the cold lunar night is very long (14 days) minimizing or even eliminating the survival power is highly desired. This can be done with a passive variable thermal link between the WEB and the Radiator. This variable thermal link can be a hot reservoir variable conductance heat pipe (VCHP).
It was already demonstrated both analytically and experimentally,, that hot reservoir VCHPs would offer tight passive thermal control as opposed to the traditional cold biased reservoir VCHPs that, for the same tightness of thermal control need reservoir heating. Figure 1 shows analytical thermal control predictions for two VCHP hot (Configuration 1) and cold (Configuration 2) reservoir designs with five different working fluids: Methanol, Toluene, Pentane, Ammonia and Propylene. As seen, the hot reservoir configuration shows a much narrower vapor temperature band compared to the cold reservoir configuration, as sink temperature sweeps vary between -90℃ and 40℃.
The hot reservoir VCHP was tested on ISS in 2017 as part of the Advanced Passive Thermal experiment (APTx) project. While the ground testing was a success, the microgravity testing failed. The pipe showed higher than admissible temperatures that tripped the safety thermostats. The explanation of the failure is as follows: during startup, the absence of natural convection in the reservoir delayed the non-condensable gas (NCG) heating compared to the vapor heating which is much more effective because of the metallic (copper) path of the incoming heat. The consequence was that vapor pressure increased faster than NCG pressure (because of poor heating) and the resulted pressure wave pushed vapor into the reservoir (where colder NCG was present), where part of it condensed. As a result, the NCG was displaced out in the condenser increasing vapor temperature considerably. The next step was the attempt to remove vapor from the reservoir by applying heat to the reservoir, which is referred to as the “purging process”. It was found that the rate of purging was very low. The slow purging rate became a show stopper for the experiment.
Based on the ISS test results, it was concluded that fluid management within the reservoir and the NCG tube (typically non-wicked) of VCHPs is the key area to be improved. Advanced features/solutions that can (1) prevent working fluid condensing inside a reservoir and (2) remove working fluid from the reservoir efficiently are needed to support foreseeable long-term warm reservoir VCHP space operations. Under this STTR program, Advanced Cooling Technologies, Inc (ACT) in collaboration with Case Western Reserve University (CWRU) perform a detailed and fundamental study to understand complex transport phenomena of multi-species within a hot reservoir VCHP. A novel “Loop hot reservoir VCHP” configuration resulted from this study, which can potentially enhance VCHP’s reliability in both ground and microgravity operations.
 R&D Engineer III, Advanced Cooling Technologies, Inc., 1046 New Holland Ave., Lancaster, PA 17601
 Principal Engineer, Advanced Cooling Technologies, Inc., 1046 New Holland Ave., Lancaster, PA 17601
 R&D Engineer II, Advanced Cooling Technologies, Inc., 1046 New Holland Ave., Lancaster, PA 17601
 Chief Engineer, Advanced Cooling Technologies, Inc., 1046 New Holland Ave., Lancaster, PA 17601
 Graduate Student, Case Western Reserve University, 10900 Euclid Ave., Cleveland, OH 44106
 Assistant Professor, Case Western Reserve University,10900 Euclid Ave., Cleveland, OH 44106
 Professor, Case Western Reserve University, 10900 Euclid Ave., Cleveland, OH 44106
II. Loop Hot Reservoir VCHP Configuration
As depicted in Figure 2, a regular hot reservoir VCHP uses only one internal NCG tube connecting the reservoir with the condenser. A loop hot reservoir VCHP concept is illustrated in Figure 3. This novel configuration consists of a hot reservoir VCHP and two NCG tubes. One tube (internal) coming out from the NCG reservoir goes into the heat pipe section from the evaporator end. A second tube externally connects the end of the condenser with the reservoir. This loop configuration would allow a secondary (the vapor flow is considered as “primary”) fluid flow to be induced and move along the loop in the favorable direction (reservoir-internal tube-condenser) for purging (indicated with the black arrows). The mechanism to induce the secondary flow (i.e. transport flow) is as follows,
- A strong vapor flow (i.e. primary flow) is generated in the heat pipe section due to evaporation and condensation of the working fluid.
- The primary flow will carry momentum in axial direction. As the vapor passes by the end of the internal NCG tube, some of the momentum will be transferred to the NCG stream through the shear between two species as well as a low static pressure point is created at the end (entrance) of the NCG tube.
- Both the momentum transfer from vapor flow to NCG at the interaction region (shown in Figure 2) as well as the low-pressure point would induce a flow of NCG in a preferential direction.
Compared to the primary flow (vapor) velocity, the secondary flow (mostly NCG) is relatively weak but it would still be beneficial for VCHP purging in the following aspects,
- During startup, this flow will condition the VCHP by transporting NCG-vapor mixture from the reservoir to the condenser via the internal NCG tube. This reduces the vapor concentration (NCG humidity) in the reservoir by bringing dryer NCG from the condenser via the external tube.
- This secondary flow exists all the time as long as vapor flow exists within the heat pipe section. Therefore, the vapor concentration within the reservoir can be maintained at low (design) values all the time.
- Based on the above-described mechanism, heating of the reservoir (to encourage purging) may be eliminated.
- This convective-based purging will be significantly more effective than the diffusion-based purging. Diffusion is basically governed by concentration gradient between reservoir and condenser, so the rate of purging will decay as the concentration gradient decreases. But the convection-based purging rate is all thermally driven for as long as power/heat is transferred by the VCHP.
III. Concept Feasibility Study – Numerical and Theoretical Analysis
A. Diffusion-based Purging Model
To study the purging process of a hot reservoir VCHP, a CFD-based model was developed and by CWRU. The computational domain is shown in Figure 4. For simplicity, an axisymmetric model was considered where a thin NCG pipe is connected to a cylindrical reservoir at the center. This is a simplified version of the heat pipe internal tube, condenser and reservoir sections. The NCG pipe is cooled at the other end, which induces the condensation of the vapor. It is assumed that a uniform mixture of vapor and NCG exists before the cooling. After the start of cooling, the concentration of the vapor decreases gradually starting from the cooling section. Eventually, by diffusion process, the vapor concentration of the whole system is reduced to the value dictated by the cooling section temperature.
The vapor concentration (ψ) is determined by solving the diffusion equation.
The diffusion coefficient, D, changes with the temperature and pressure within the system.
where D = D0 at T0 = 273 K (0°C) and P0 = 1 atm (101 kPa). Except for the condenser, all other walls are assumed to be insulated. A mixture of water vapor and helium (NCG) is considered in the present analysis. Before the cooling starts, the mixture everywhere is assumed to be 50% water vapor and 50% helium at a temperature of 30°C. After time = 0, the cooling wall temperature is set at 10°C. For this mixture, D0 is estimated to be equal to 2 × 10-5 m2/s. The mixture temperature changes from 30°C to 10°C in the process. The variation of vapor concentration within the reservoir is shown in Figure 5.
Figure 5(a) shows how the values of ψmax change with time for several values of NCG pipe lengths. As the figure shows, diffusion (or purging) is a very slow process due to the fact that the mass transfer rate through the thin NCG pipe is limited. Although the total purging time depends on how we define the acceptable value of ψmax, the purging will take several days if the pipe length is longer than about 10 cm. The effect of the pipe diameter on the purging process is shown in Figure 5(b). As seen in the figure, a diameter of 2.8 mm reduces the purging time to around 15 hours. The analysis results demonstrated that the purging by diffusion may take tens of hours or even days, which matches ACT’s past testing experience.
B. Numerical Study of Hot Reservoir VCHP Loop
Another numerical model is developed by CWRU to study the interaction between vapor and NCG within a hot reservoir VCHP and verify the momentum inducing the flow mechanism described in the previous section. The computational domain is shown schematically in Figure 5. In this study the working fluid is acetone and the NCG is helium. The working temperatures are: 50, 60, 70, 80°C. It is assumed that the heat pipe operates in a gravity-assisted mode, so there is no wick structure. The pipe wall is made of aluminum. The relevant dimensions of the loop VCHP are summarized in Table 1. The amount of NCG is arbitrary determined such that the vapor-NCG interface is located halfway in the condenser section at 50°C. The interface moves more into the condenser section with an increase in operating temperature. The cooling is assumed to be done by forced convection cooling with a specified heat transfer coefficient. The heat transfer coefficient is specified such that the heat input is nearly equal to 30W at 50°C with the ambient temperature equal to 20°C. Since the phenomena in the evaporator are not the focus in the present study, it is assumed that the evaporator simply generates enough vapor to balance the amount of condensation in steady-state, so that the vapor flow is analyzed only in the adiabatic and condenser sections. The total pipe length (heat pipe and loop) is assumed to be 1 m. Since the NCG pipe is long and thin and the flow through the pipe is expected to be on the order of mm/s, the flow in the pipe can be assumed to be fully developed. Therefore, instead of analyzing the pipe flow in detail, the known pressure drop-velocity relation for fully-developed pipe flow is used. The relation can be written as
The computed pressure difference (∆P) within a heat pipe with an internal NCG tube is about 0.1 Pa. Even though the pressure difference is small, it is enough to generate appreciable flow. For example, 0.1 Pa of pressure difference can induce around 3.4 mm/s of flow (calculated based on Equation (3)).
The dependence of the velocity on the NCG pipe outlet location is shown in Figure 7 (a). The velocity increases as LNCG becomes smaller. This happens because as the NCG pipe recedes (LNCG becomes smaller), the friction effect on the vapor flow in the heat pipe decreases so that the stagnation pressure (or the pressure in the NCG region) increases. For the condition of Figure 7 (a), the maximum velocity through the NCG pipe is about 4 mm/s. Figure 7 (b) shows how the velocity changes with Q while keeping Tsat constant. Q is changed from 8.9 to 41.5 W by changing the heat transfer coefficient for the cooling from 44 to 435 Wm-2∙K-1. The pipe flow velocity increases almost linearly with Q.
The effect of working temperature on the average NCG flow velocity is also numerically investigated. The relation between working temperature and induced NCG flow velocity when Q is fixed at 31W is presented in Figure 8(a). This figure shows that the velocity decreases with temperature. This occurs because as the vapor temperature increases, vapor density increases as well, which results in a decelerating vapor flow (for fixed Q), and therefore, the shearing effect on NCG decreases. To be noted is the fact that, in this case, the front goes away from the NCG tube which, according to modeling results, would increase the pressure difference. However, vapor velocity decrease dominates. Next, the combination effects of Q and the interface location with constant cooling rate is studied, which is shown in Figure 8 (b). As shown above, the effect of Q on the velocity is opposite to that of the interface location: increasing Q increases average flow velocity but moving the vapor front further away from the NCG tube end decreases the flow velocity.
Axial velocity profile along the cross-section A-A (aligned with the NCG pipe outlet) is presented in Figure 9. Since the NCG flow coming out from the internal tube is very small compared to the primary vapor velocity (~0.25 cm/s), it is very difficult to observe in the figure that there is a non-zero velocity near the center core (r = 0). In summary, utilizing this loop based VCHP concept, it is possible to obtain a sufficiently large velocity through the external pipe so that the purging can be accomplished within several minutes, which represents a significant improvement compared to the diffusion-based purging process discussed above. It is also found through simulation that multiple design parameters will affect the induced flow velocity, including
Internal NCG tube end location and vapor front location.
- Heat input.
- Vapor temperature.
- Annular space between heat pipe and NCG tube.
- Gravity level and orientation of the pipe.
IV. Concept Feasibility Study – Experimental Validation
A. Experimental apparatus
In parallel to the mathematical study, an experimental demonstration was conducted by ACT to prove the existence of the momentum transport flow within a VCHP Loop. The schematic experimental system is shown in Figure 10 and the actual test setup is shown in Figure 11. The test apparatus consists of a VCHP with a non-integrated reservoir and an external NCG tube connecting between the condenser and the reservoir. The structural material is stainless steel. Working fluid and NCG are acetone and helium. The heat pipe section is in a slight gravity-aid orientation (< 5°) and there is no wick structure inserted within the adiabatic and condenser sections for liquid return. According to the findings from numerical analysis (Figure 8(a)), the internal NCG tube length was adjusted so it ends in the adiabatic section before the condenser to obtain a higher induced flow velocity. Temperatures at various locations along the heat pipe and the loop are measured by 26 TCs. The key dimensions of the test setup are summarized in Table 2.
Measuring the secondary flow induced by the primary vapor flow, a gas flow transducer (Omega FMA 1702A) is mounted in the line of the external NCG loop. This flow meter has no moving parts and uses thermal-based technique to measure gas flow rate (hot wire anemometry). The measurement range of this flow meter is 0 to 10 cc/min. A very important fact is that this flow meter measures flow in only one direction. It allows however reverse flow but it reports “zero” flow rate in the DAQ system.
B. Thermal Control Capability Demonstration
A thermal control testing is performed to assess/verify that adding an external NCG loop to hot reservoir VCHPs will not compromise the thermal control capability of the VCHP. Figure 12(a) shows the operation of the VCHP loop at 80 W. At t = 2200 seconds, sink temperature is suddenly decreased from 75 °C to -10 °C. As the figure shows, the variation of evaporator temperature is less than 10 °C. Instantaneous temperature profiles\ of the heat pipe at steady state before and after a decrease of sink temperature are shown in Figure 12(b). It can be observed that the vapor NCG front is located beyond the end of the condenser during the hot sink temperature mode before the step change. Then, the vapor NCG-front moves to reduce the active condenser length after the sink temperature drops. The new front is located at end of the adiabatic section. Based on these test results, it is reasonable to state that adding an external NCG loop to a hot reservoir VCHP has minimal impact on its thermal control capability.
C. Flow Measurements
Figure 13 shows the temperature evolution of the Loop VCHP and the corresponding flow rate measured by the flow meter. For this test, an amount of 6 ml of acetone was charged.
- As the vapor/NCG is established within the condenser (shown as a purple line merging with the light blue line), an oscillating flow is observed.
- The amplitude of oscillations is at around 1.5 sccm before the valve connecting heat pipe and loop is closed.
- Immediately after closing the valve (t =8200 sec), the amplitude dramatically increases.
- As mentioned above, the flow meter cannot detect the flow in the opposite direction. All the “zero” values observed in this plot indicate that a reverse flow is passing the flow meter.
Flow test results reveal that the flow within the current Loop VCHP is a pulsating flow. One of the probable causes of these pulses is the puddle formation in the evaporator. Since the heat pipe is slightly tilted, the excess working fluid liquid will accumulate at the bottom of evaporator and form a puddle. The expansion and collapse of bubbles might generate pressure waves. Another hypothesis of the origin of these pressure waves is the liquid slug forming in the condenser. Both phenomenon (puddle and slug formation within a heat pipe) are gravity-dependent and related to wick design. In microgravity, puddles and slugs might not form within a wicked heat pipe (either sintered powder or screen). However, liquid bodies and slugs could form within a grooved heat pipe in microgravity. Further investigation/assessements are needed for future space and planetary applications. This pressure wave generated from the heat pipe section propagates through the NCG tubes. The response of flow in the NCG tube will change depending on the status of the valve
- If the valve is open, the pressure wave will propagate through both sides of NCG tube (external and internal) and partially cancel each other. The amplitude of the pulses is small.
- If the valve is closed, pressure wave will propagate through only one side of NCG tube (internal) and the flow meter will experience a higher amplitude of oscillation.
Based on this finding, two potential mechanisms associated with Loop VCHP configuration to induce/enhance a net flow for purging are identified:
- Flow induced by the momentum generated in the NCG tube through pressure variation (original mechanism). This mechanism is called “DC” mechanism.
- Flow induced by filtering (via a Tesla or a check valve) the pulse generated within the heat pipe section. This mechanism is called “AC” mechanism.
Note that the DC and AC mechanisms are independent in this context, meaning that they can be superimposed to induce a higher net mass flow rate within a loop VCHP.
D. Momentum Transfer Flow (DC Mechanism) Identification
The flow induced by DC mechanism is embedded within the total flow with pulses. In order to detect the flow, it is necessary to minimize the amplitude of the pulses. This is done by inserting a layer of screen mesh into the evaporator section and minimizing fluid inventory to avoid puddle formation in the evaporator. Test results are shown in Figure 14. The red line represents the heat input to the evaporator and the blue line represents the induced net flow rate. With a 2 ml of working fluid inventory, pulse amplitude is minimized to be within the resolution of the flow meter. A clear relationship between the induced flow rate and the heat input can be identified. The flow rate of induced flow increases as the heat input increases. With 72W of heat input, the net flow velocity being induced is 0.8 cm/min (0.13 mm/s). All the evidence points to the same conclusion: there is a net flow induced by the momentum transfer from the vapor to NCG within the Loop VCHP. The existence of DC flow is successfully proven.
V. Prototype Development and Performance Demonstration
A hot Reservoir VCHP loop prototype is then developed for concept demonstration, which is shown in Figure 15(a). This VCHP prototype has an integrated reservoir similar to the VCHPs previously developed under another NASA Phase II program. This prototype consists of several parts, including reservoir, condenser, internal NCG tube, heat pipe adiabatic section and the external NCG tube. These parts are joined by Swagelok fittings, so they can be exchangeable. The working fluid is acetone and NCG is helium. No wick structure is inserted within the heat pipe adiabatic and condenser sections. liquid return is simply achieved by gravity. Similar to the loop VCHP experimental setup, a layer of screen is inserted into the evaporator to avoid puddle formation. There are two fill tubes in this prototype: one fill tube attached to the end of the condenser is for working fluid and NCG charging; another fill tube welded on the top of the reservoir is used for the purging test only. The experimental system for VCHP prototype testing is shown in Figure 15(b). Heating to the evaporator is provided by a heater block from the bottom of the evaporator. The cooling of the condenser is provided by a chiller block. The instrumentation includes 25 T-type TCs and the flow meter to measure the induced flow rate through the NCG loop. Two DAQ systems (one for temperature and one for flow meter) are simultaneously operating to collect both temperature and flow data.
The purging performance of this prototype was tested and the result are shown in Figure 16. At t=t0, heat input incrementally increases from 110W to 140W. At t=t1, 0.3 ml of acetone, which is 12% of the working fluid inventory is directly injected into the reservoir. Immediately, payload temperatures increase and condenser temperatures decrease, meaning that the vapor front is pushed towards the adiabatic section decreasing the active length of the condenser. Monitoring payload temperature decaying rate between t2 and t3 it can be observed that the average dropping rate is around -4°C in 3000 seconds. The corresponding induced flow rate measured by the flow meter is around 0.16 ml/min. Compared to a regular hot reservoir VCHP without a loop, the purging speed of this prototype is 6.7 times faster. This test results conclude that new loop configuration and the induced flow concept does improve the purge rate and reliability of VCHP.
Still, there is significant room for improvement. ACT and CWRU team believe that an even higher induced flow can be achieved by design optimization and implementation of other features (e.g. pulse filtering devices and nozzles etc.). Figure 17 below shows how effective the purging process would be if a transport flow can be induced within the Loop VCHP. This calculation assumes that an NCG reservoir volume of 100 c.c. contains 50% of vapor initially and the internal NCG tube (with 0.18”ID) has a length of 50 cm. Purging by diffusion will take roughly 24 hours to reduce vapor concentration within the reservoir from 50% to 35%. If a 0.5 mm/s of transport flow can be induced within the loop VCHP, it will only take 6 hours to achieve the same level of concentration reduction (from 50% to 35%). If a 20 mm/s flow velocity within a VCHP loop can be achieved (through superimposing DC and AC mechanisms discussed above), purging time can be significantly reduced to less than 10 mins. To achieve a higher flow rate in the loop VCHP, the ACT-CWRU team plans to (1) systematically study the momentum induced flow and identify influential design parameters (2) develop features that can amplify the momentum induced flow and (3) develop pules filtering devices to obtain a net flow from pulses.
Under this STTR Phase I, ACT and CWRU performed a fundamental investigation to understand the complex transport phenomena within a hot reservoir VCHP. In order to address the slow purging problem of a hot reservoir VCHP, a novel loop configuration is developed that uses an external NCG tube connecting the reservoir and the condenser to create a closed flow path for NCG to replenish the reservoir. With the loop configuration, the momentum of vapor within the heat pipe section will generate a pressure difference that can induce a net NCG flow in a favorable direction for reservoir purging (i.e. removal of vapor from the reservoir). Modeling results demonstrate the possibility of flow generation through momentum transport/transfer in a Loop hot reservoir VCHP. A Loop VCHP experiment is performed and the following key findings are identified:
- Thermal control capability of hot reservoir VCHP is not affected by adding a loop.
- Flow within a hot reservoir VCHP loop is pulsating.
- The momentum transfer based induced flow is successfully identified using an accurate gas flow meter.
In addition, two independent mechanisms that can induce a net flow are identified:
- By the momentum transfer from the vapor to NCG through shearing. This mechanism is called “DC” mechanism .
- By filtering the pulses generated within Loop VCHP, using a fluid diode (e.g. Tesla valve). This mechanism is called “AC” mechanism.
These two mechanisms are independent, so they can be superimposed to induce a higher flow rate for purging. A proof-of-concept prototype that has an integrated evaporator and reservoir design similar to the hardward tested at ISS is developed. The thermal control capability and momentum induced flow of the prototype are experimentally demonstrated. The reliability of the prototype is also tested, which shows a 6.7 times of purging rate improvement compared to regular hot reservoir VCHP without loop and induced flow. If a 20 mm/s flow velocity within a VCHP loop can be achieved (through superimposing DC and AC mechanisms discussed above), purging time can be significantly reduced to less than 10 mins.
This project is sponsored by NASA Marshall Space Flight Center (MSFC) under an STTR Phase I program (Contract# 80NSSC18P2155). We would like to thank the program manager, Brian O’Connor and Dr. Jeff Farmer for their supports and valuable inputs during the program. Special appreciation goes to Philip Texter and Chris Jarmoski who have provided significant technical contributions to the program.
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Advanced Passive Thermal eXperiment (APTx) for Warm-Reservoir Hybrid-Wick Variable Conductance Heat Pipes on the International Space Station (ISS),”
Calin Tarau, et al., International Conference on Environmental Systems (ICES 2018), Albuquerque, NM July 8-12, 2018Download PDF
Titanium Water Heat Pipe Radiators for Space Fission System Thermal Management
Kuan-Lin Lee, et al., 19th International Heat Pipe Conference, Pisa, Italy, June 10-14, 2018Download PDF
Copper-Water and Hybrid Aluminum-Ammonia Heat Pipes for Spacecraft Thermal Control Applications
Mohammed Ababneh, et al., 19th International Heat Pipe Conference, Pisa, Italy, June 10-14, 2018Download PDF
Loop Heat Pipe Wick Fabrication via Additive Manufacturing
Bradley Richard, et al., 19th International Heat Pipe Conference, Pisa, Italy, June 10-14, 2018Download PDF
Meshless Computational tools for Fatigue Damage and Failure Modeling
Srujan Rokkam et al., ITHERM 2018 (17th Intersociety Conference on Thermal and Thermomechanical Phenomena in Electronic Systems), San Diego, CA, May 29 – June 1Download PDF
Thermal Management Technologies for Embedded Cooling Applications
Andy Slippey et al., ITHERM 2018 (17th Intersociety Conference on Thermal and Thermomechanical Phenomena in Electronic Systems), San Diego, CA, May 29 – June 1Download PDF
Experimental, Numerical and Analytic Study of Unconstrained Melting in a Vertical Cylinder with a Focus on Mushy Region Effects
Chunjian Pan,⇑, Joshua Charles, Natasha Vermaak, Carlos Romero, Sudhakar Neti, Energy Research Center, Lehigh University, Bethlehem, PA 18015, USA Ying Zheng, Chien-Hua Chen, Richard Bonner III, Advanced Cooling Technologies, Inc., Lancaster, PA 17601, USA International Journal of Heat and Mass Transfer, Accepted 2 April 2018Download PDF
A Non-Thermal Gliding Arc Plasma Reformer for Syngas Production
Howard Pearlman, 3rd Thermal and Fluids Engineering Conference (TFEC), Fort Lauderdale, FL, March 4-7, 2018Download PDF
An Innovative Volatile Organic Compound Incinerator
Joel Crawmer et al., International Thermal Treatment Technologies (IT3), Houston, TX, March 6-8 2018Download PDF
Developing High-Temperature Water-Repellent Glass Fibers Through Atomic Layer Deposition
Mohammad Reza Shaeri et al., 3rd Thermal and Fluids Engineering Conference (TFEC), Fort Lauderdale, FL, March 4-7, 2018.Download PDF
Dropwise Condensation on Hydrophobic Microporous Powder and the Transition to Intrapowder Droplet Removal
Sean Hoenig and Richard W. Bonner, III, 3rd Thermal and Fluids Engineering Conference (TFEC), Fort Lauderdale, FL, March 4-7, 2018.Download PDF
The Key Role of Pumping Power in Active Cooling Systems
Mohammed Reza Shaeri, 3rd Thermal and Fluids Engineering Conference (TFEC), Fort Lauderdale, FL, March 4-7, 2018.Download PDF
Nucleating agent enhanced thermal desalination at the triple point
Fangyu Cao et al., 3rd Thermal and Fluids Engineering Conference (TFEC), Fort Lauderdale, FL, March 4-7, 2018Download PDF
Dropwise Condensation on Superhydrophobic Microporous Wick Structures
Sean Hoenig, Richard Bonner, Ph.D., ASME doi:10.1115/1.4038854 History: Received April 28, 2017; Revised December 06, 2017Download PDF
A Peridynamics-FEM Approach for Crack Path Prediction in Fiber-Reinforced Composites
Srujan Rokkam et al., 2018 AIAA SciTech Forum, Kissimmee, FL, January 8-12, 2018.Download PDF
Vapor chambers with hydrophobic and biphilic evaporators in moderate to high heat flux applications
Mohammad Reza Shaeri, Daniel Attinger, Richard W. Bonner III, Applied Thermal Engineering, Volume 130(5), Pages 83-92, February 2018View Full Paper
Model-Based Dynamic Control of Active Thermal Management System
ASME 2017 International Mechanical Engineering Congress and Exposition IMECE 2017 - 71918, November 3-9, 2017 Tampa, FL. Nathan Van Velson, Srujan Rokkam, Quang Truong, Bryan RasmussenDownload PDF
Efficient optimization of a longitudinal finned heat pipe structure for a latent thermal energy storage system
Sean Hoenig et al., Energy Conversion and Management, 153, pp. 93-105, 2017.View Full Paper
The Electroneutrality Constraint in Nonlocal Models
Eitan Lees, Srujan Rokkam, Sachin Shanbhag, and Max Gunzburger. Journal of Chemical Physics 147, 124102 (2017)View Full Paper
Heat Pipe Embedded Thermoelectric Generator for Diesel Generator Set Waste Heat Recovery
James Schmidt and Mohammed Ababneh. 14th International Energy Conversion Engineering Conference, AIAA Propulsion and Energy Forum, (AIAA 2016-4605)View Full Paper
Efficient Modeling of Phase Change Material Solidification with Multidimensional Fins
C. Pan et al., International Journal of Heat and Mass Transfer, Vol. 115, Part A, pp. 897-909, December 2017.View Full Paper
Integrated Vapor Chamber Heat Spreader for Power Module Applications
Clayton Hose et al., InterPACK 2017, San Francisco, CA, August 29 – September 1, 2017Download PDF
Heat transfer and pressure drop in laterally perforated-finned heat sinks across different flow regimes
Mohammad Reza Shaeri, Richard Bonner Advanced Cooling Technologies, Inc., Lancaster, PA 17601, United States , Available online 24 August 2017View Full Paper
Feasibility Study of a Vapor Chamber with a Hydrophobic Evaporator Substrate in High Heat Flux Applications
Mohammad Reza Shaeria et al., International Communications in Heat and Mass Transfer, Vol. 86, pp. 199–205, 2017.View Full Paper
Effect of Perforation Size to Perforation Spacing on Heat Transfer in Laterally Perforated-Finned Heat Sinks
Mohammed Reza Shaeri, and Richard W. Bonner III, ASME 2017 Summer Heat Transfer Conference (HT2017), July 9-14, 2017, Bellevue, Washington, USADownload PDF
Two-Phase Heat Exchanger with Thermal Storage Capability for Space Thermal Control System
Two-Phase Heat Exchanger with Thermal Storage Capability for Space Thermal Control System, Kuan-Lin Lee, et al. 47th International Conference on Environmental Systems (ICES 2017), July 16-20, 2017, Charleston, South CarolinaDownload PDF
Advanced Passive Thermal Experiment for Hybrid Variable Conductance Heat Pipes and HiK™ Plates on the International Space Station
Advanced Passive Thermal Experiment for Hybrid Variable Conductance Heat Pipes and HiK™ Plates on the International Space Station, Mohammed T. Ababneh, et al. 47th International Conference on Environmental Systems (ICES 2017), July 16-20, 2017, Charleston, South CarolinaDownload PDF
LHP Wick Fabrication via Additive Manufacturing
LHP Wick Fabrication via Additive Manufacturing. Bradley Richard, et al. 47th International Conference on Environmental Systems (ICES 2017), July 16-20, 2017, Charleston, South CarolinaDownload PDF
High Temperature Water Heat Pipes for Kilopower System
Derek Beard et al., IECEC – AIAA Propulsion and Energy Forum and Exposition (AIAA Propulsion and Energy 2017), July 10-12, Atlanta, GeorgiaDownload PDF
Laminar Forced Convection Heat Transfer From Laterally Perforated-Finned Heat Sinks
Mohammad Reza Shaeri and Richard W. Bonner III, Applied Thermal Engineering, Volume 116, pp. 406-418, April 2017.View Full Paper
An Innovative Volatile Organic Compound Incinerator
Joel Crawmer et al., 10th U. S. National Combustion Meeting, College Park, MD, April 23-26, 2017Download PDF
A Swiss Roll Style Combustion Reactor for Non-Catalytic Reforming
Ryan Zelinsky et al., 10th U. S. National Combustion Meeting, College Park, MD, April 23-26, 2017Download PDF
Thermal Resistance Network Model for Heat Pipe-PCM Based Cool Storage System
Sean Hoenig et al., 2nd Thermal and Fluid Engineering Conference (TFEC2017), Las Vegas, NV, April 2-5 2017.Download PDF
Development of Low Cost Radiator for Surface Fission Power
Calin Tarau et al., International Energy Conversion Engineering Conference (IECEC), Salt Lake City, UT, July 25-27, 2016Download PDF
Generation of amorphous carbon models using liquid quench method: A reactive molecular dynamics study.
Raghavan Ranganathan, Srujan Rokkam, Tapan Desai, Pawel Keblinski Carbon, Volume 113, March 2017, Pages 87–99Download PDF
Self-Venting Arterial Heat Pipes for Spacecraft Applications
Derek Beard, William G. Anderson, and Calin Tarau, International Energy Conversion Engineering Conference (IECEC), Salt Lake City, UT, July 25-27, 2016Download PDF
Hybrid Heat Pipes for Lunar and Martian Surface and High Heat Flux Space Applications
Mohammed T. Ababneh et al., International Conference on Environmental Systems (ICES) 2016, Vienna. Austria, July 11-14, 2016Download PDF
Development of a Pumped Two-phase System for Spacecraft Thermal Control
Michael C. Ellis and Richard C. Kurwitz, International Conference on Environmental Systems (ICES) 2016, Vienna. Austria, July 11-14, 2016Download PDF
Vapor Chamber with Phase Change Material-Based Wick Structure
James Yun, Calin Tarau, and Nathan Van Velson, International Conference on Environmental Systems (ICES) 2016, Vienna. Austria, July 11-14, 2016Download PDF
A Novel Closed System, Pressure Controlled Heat Pipe Design for High Stability Isothermal Furnace Liner Applications
Taylor Maxwell et al., 13th International Symposium on Temperature and Thermal Measurements in Industry and Science (TEMPMEKO 2016), Zakopane, Poland, June 26 – July 1, 2016Download PDF
Thermal Enhancements for Separable Thermal Mechanical Interfaces
James Schmidt et al., AIAA Thermophysics Conference, Washington, D.C., June 13-17, 2016Download PDF
Hot Reservoir Stainless-Methanol Variable Conductance Heat Pipes for Constant Evaporator Temperature in Varying Ambient Conditions
Jens Weyant et al., Joint 18th International Heat Pipe Conference and 12th International Heat Pipe Symposium, Jeju, Korea, June 12-16, 2016Download PDF
Hybrid Variable and Constant Conductance Heat Pipes for Lunar and Martian Environments and High Heat Flux Space Applications
Mohammed T. Ababneh et al., Joint 18th International Heat Pipe Conference and 12th International Heat Pipe Symposium, Jeju, Korea, June 12-16, 2016Download PDF
Self-Venting Arterial Heat Pipes for Spacecraft Applications
William G. Anderson et al., Joint 18th International Heat Pipe Conference and 12th International Heat Pipe Symposium, Jeju, Korea, June 12-16, 2016Download PDF
Performance Life Testing of a Nanoscale Coating for Erosion and Corrosion Protection in Copper Microchannel Coolers
Nathan Van Velson and Matt Flannery, IEEE ITherm Conference, May 31-June 3, 2016, Las Vegas, NVDownload PDF
Heat Pipes used as Heat Flux Transformers and for Remote Heat Rejection
Devin Pellicone and Jens Weyant, PCIM Europe 2016, Nuremberg, Germany, May 10-12, 2016Download PDF
Enhanced Filmwise Condensation with Thin Porous Coating
Ying Zheng, Chien-Hua Chen, Howard Pearlman, Richard Bonner, First Pacific Rim Thermal Engineering Conference, PRTEC, March 13-17, 2016, Hawaii's Big Island, USA.Download PDF
Optimized Alkali Metal Backup Cooling System Tested with a Stirling Convertor
Calin Tarau, Nuclear and Emerging Technologies for Space (NETS) 2016, Huntsville, AL, February 22-25, 2016.Download PDF
Status of the Development of Low Cost Radiator for Surface Fission Power II
Calin Tarau, Nuclear and Emerging Technologies for Space (NETS) 2016, Huntsville, AL, February 22-25, 2016.Download PDF
Passivation and Stabilization of Aluminum Nanoparticles for Energetic Materials
Matthew Flannery, Journal of Nanomaterials, vol. 2015, Received 17 June 2015; Accepted 13 October 2015View Full Paper
Optimized Heat Pipe Backup Cooling System Tested with a Stirling Convertor
Carl L. Schwendeman, Calin Tarau, Nicholas A. Schifer, John Polak, and William G. Anderson, 13th International Energy Conversion Engineering Conference (IECEC), Orlando, FL, CA, July 27-29, 2015.Download PDF
Status of the Low-Cost Radiator for Fission Power Thermal Control
Taylor Maxwell, Calin Tarau, William G. Anderson, Scott Garner, Matthew Wrosch, and Maxwell H. Briggs, 13th International Energy Conversion Engineering Conference (IECEC), Orlando, FL, CA, July 27-29, 2015.Download PDF
Water-Titanium Heat Pipes for Spacecraft Fission Power
Rebecca Hay and William G. Anderson, 13th International Energy Conversion Engineering Conference (IECEC), Orlando, FL, CA, July 27-29, 2015.Download PDF
Two-Phase Thermal Switch for Spacecraft Passive Thermal Management
Nathan Van Velson, Calin Tarau, and William G. Anderson, 45th International Conference on Environmental Systems (IECS), Bellevue, WA, July 12-16, 2015.Download PDF
Multiple Loop Heat Pipe Radiator for Variable Heat Rejection in Future Spacecraft
Nathan Van Velson, Calin Tarau, Mike DeChristopher, and William G. Anderson, 45th International Conference on Environmental Systems (IECS), Bellevue, WA, July 12-16, 2015.Download PDF
Hybrid Heat Pipes for Planetary Surface and High Heat Flux Applications
Mohammed T. Ababneh, Calin Tarau, and William G. Anderson, 45th International Conference on Environmental Systems (IECS), Bellevue, WA, July 12-16, 2015.Download PDF
Experimental Investigation on the Thermal and Hydraulic Performance of Alumina–Water Nanofluids in Single-Phase Liquid-Cooled Cold Plates
Ehsan Yakhshi-Tafti, Sanjida Tamanna and Howard Pearlman, Journal of Heat Transfer, Vol. 137, July 1, 2015View Full Paper
A “Swiss-Roll” Fuel Reformer: Experiments and Modeling
Chien-Hua Chen, Bradley Richard, Ying Zheng, Howard Pearlman, Shrey Trivedi, Srusti Koli, Andrew Lawson, and Paul Ronney, “A “Swiss-Roll” Fuel Reformer: Experiments and Modeling,” 9th U. S. National Combustion Meeting, Cincinnati, OH, May 17-20, 2015.Download PDF
Effect of Porous Coating on Condensation Heat Transfer
Ying Zheng, Chien-hua Chen, Howard Pearlman, Matt Flannery and Richard Bonner. 9th International Conference on Boiling and Condensation Heat Transfer, April 26-30, 2015, Boulder, Colorado.Download PDF
High Temperature Water-Titanium Heat Pipes for Spacecraft Fission Power
Rebecca Hay and William G. Anderson, Nuclear and Emerging Technologies for Space (NETS-2015), Albuquerque, NM, February 23-26, 2015.Download PDF
Nanoscale Coating for Microchannel Cooler Protection in High Powered Laser Diodes
Tapan Desai, Matthew Flannery, Nathan Van Velson, and Philip Griffin, “Nanoscale Coating for Microchannel Cooler Protection in High Powered Laser Diodes,” Semiconductor Thermal Measurement and Management Symposium (SEMI-THERM 2015), San Jose, CA, March 16-19, 2015.Download PDF
Fuel-Flexible Hybrid Solar Coal Gasification Reactor
M. Flannery et al., "Fuel-Flexible Hybrid Solar Coal Gasification Reactor," 2014 Pittsburgh Coal Conference, Pittsburgh, PA, October 6 - 9, 2014.Download PDF
Heat Pipe Embedded Carbon Fiber Reinforced Polymer Composite Enclosures for Avionics Thermal Management
Andrew Slippey, Michael C. Ellis, Bruce Conway, and Hyo Chang Yun. SAE 2014 Aerospace Systems and Technology Conference, Cincinnati, OH, September 23-25, 2014.Download PDF
Passive Thermal Management for Avionics in High Temperature Environments
Michael C. Ellis, William G. Anderson, and Jared R. Montgomery. SAE 2014 Aerospace Systems and Technology Conference, Cincinnati, OH, September 23-25, 2014.Download PDF
Passivation of Aluminum Nanoparticles by Plasma-Enhanced Chemical Vapor Deposition for Energetic Nanomaterials
T. Desai et al., ACS Applied Materials and Interfaces Journal, 2014, 6 (10), pp. 7942–7947, DOI: 10.1021/am5012707Download PDF
Thermal Modeling and Experimental Validation for High Thermal Conductivity Heat Pipe Thermal Ground Planes
Ababneh, Mohammed T., Shakti Chauhan, Pramod Chamarthy, and Frank M. Gerner. "Thermal Modeling and Experimental Validation for High Thermal Conductivity Heat Pipe Thermal Ground Planes." Journal of Heat Transfer 136, no. 11 (2014): 112901.View Full Paper
Launch Vehicle Avionics Passive Thermal Management
W. G. Anderson et al., “Launch Vehicle Avionics Passive Thermal Management,” 44th International Conference on Environmental Systems (ICES 2014), Tucson, AZ, July 13-17, 2014.Download PDF
Low Cost Radiator for Fission Power Thermal Control
Taylor Maxwell et al, 12th International Energy Conversion Engineering Conference (IECEC), Cleveland, OH, July 28-30, 2014.Download PDF
Flow Boiling Heat Transfer Enhancement in Subcooled and Saturated Refrigerants in Minichannel Heat Sinks
E. Yakhshi-Tafti et al., ASME 2014 4th Joint US-European Fluids Engineering Division Summer Meeting and 12th International Conference on Nanochannels, Microchannels, and Minichannels, August 3-7, 2014, Chicago, IL.Download PDF View Full Paper
Thermal-Fluid Modeling for High Thermal Conductivity Heat Pipe Thermal Ground Planes
M. T. Ababneh et al., published in the AIAA Journal of Thermophysics and Heat Transfer, Vol. 28, No. 2, pp. 270-278, April 2014.Download PDF
Thermoelectric Performance Model Development and Validation for a Selection and Design Tool
Thomas Nunnally, Devin Pellicone, Nathan Van Velson, James Schmidt, Tapan Desai, 2014 IEEE Intersociety Conference on Thermal and Thermomechanical Phenomena in Electronic Systems (ITherm), Orlando, FL, May 27-30, 2014.Download PDF
Enhancing Thermal Performance in Embedded Computing for Ruggedized Military and Avionics Applications
Darren Campo, Jens Weyant, Bryan Muzyka, 2014 IEEE Intersociety Conference on Thermal and Thermomechanical Phenomena in Electronic Systems (ITherm), Orlando, FL, May 27-30, 2014.Download PDF
A Corrosion and Erosion Protection Coating for Complex Microchannel Coolers used in High Power Laser Diodes
Tapan G. Desai, Matthew Flannery, Angie Fan, Jens Weyant, Henry Eppich, Keith Lang, Richard Chin, and Aland Chin, 2014 IEEE Intersociety Conference on Thermal and Thermomechanical Phenomena in Electronic Systems (ITherm), Orlando, FL, May 27-30, 2014Download PDF
The Thermal Conductivity of Clustered Nanocolloids
T. Desai et al., APL Materials, 2, 066102 (2014); doi: 10.1063/1.4880975. 21 May 2014;Download PDF
Diffuse interface modeling of void growth in irradiated materials. Mathematical, thermodynamic and atomistic perspectives
Anter El-Azab Karim Ahmed, Srujan Rokkam, Thomas Hochrainer, Published in Current Opinion in Solid State and Materials Science (COSSMS), Vol. 18, pg. 90-98, 2014.Download PDF
Correlation for dropwise condensation heat transfer: Water, organic fluids, and inclination
Richard W. Bonner III, International Journal of Heat and Mass Transfer, Volume 61, June 2013, Pages 245-253View Full Paper
Planar vapor chamber with hybrid evaporator wicks for the thermal management of high-heat-flux and high-power optoelectronic devices
P. Dussinger et al., International Journal of Heat and Mass Transfer, Volume 60, pp. 163–169, May 2013.View Full Paper
Preliminary First Principle Based Electro-thermal Coupled Solver for Silicon Carbide Power Devices
Angie Fan et al., 29th IEEE SEMI-THERM Symposium, San Jose, CA, March 17-21, 2013Download PDF
Long-Lived Venus Lander Thermal Management System Design
Rebecca Hay et al., 9th Intersociety Energy and Conversion Engineering Conference (IECEC), Atlanta, GA, July 30 July-August 1, 2012.Download PDF
A 2-D Numerical Study of Microscale Phase Change Material Thermal Storage for GaN Transistor Thermal Management
Xudong Tang, et al., Semitherm, San Jose, CA, March 2011Download PDF
Loop Heat Pipe with Thermal Control Valve for Variable Thermal Conductance Link of Lunar Landers and Rovers
Loop Heat Pipe with Thermal Control Valve for Variable Thermal Conductance Link of Lunar Landers and Rovers, J. R. Hartenstine et al., 49th AIAA Aerospace Sciences Meeting, Orlando, FL, January 4-7, 2011.Download PDF View Full Paper
Heat and Mass Transfer in a Permeable Fabric system Under Hot Air Jet Impingement,
Sangsoo Lee et. al., International Heat Transfer Conference (IHTC14), Washington, DC, August, 2010Download PDF
Sodium Variable Conductance Heat Pipe for Radioisotope Stirling Systems – Design and Experimental Results
Calin Tarau and William G Anderson, IECEC, Nashville, Tennessee, July, 2010Download PDF
Sodium Variable Conductance Heat Pipe with Carbon-Carbon Radiator for Radioisotope Stirling Systems
Calin Tarau and William G. Anderson, 15th International Heat Pipe Conference, Clemson, SC, April 2010Download PDF
Intermediate Temperature Fluids for Heat Pipes and Loop Heat Pipes
William G. Anderson, John R. Hartenstine, David B. Sarraf, and Calin Tarau, Advanced Cooling Technologies, Inc., Pennsylvania, 15th International Heat Pipe Conference (15th IHPC) Clemson, USA, April 25-30, 2010.Download PDF View Full Paper
Anisotropic Shock Response of Columnar Nanocrystalline Cu
Sheng-Nian Luo et. al., Journal of Applied Physics , 107, 123507 (2010)Download PDF
Pressure Controlled Heat Pipe for Precise Temperature Control
David Sarraf, et al., Space Technology and Applications International Forum (STAIF), Albuquerque, New Mexico, February 2008Download PDF