## Figures

## Abstract

During expiration, the carbon dioxide (CO_{2}) levels inside the dead space of a filtering facepiece respirator (FFR) increase significantly above the ambient concentration. To reduce the CO_{2} concentration inside the dead space, we attach an active lightweight venting system (AVS) comprising a one-way valve, a blower and a battery in a housing to a FFR. The achieved reduction is quantified with a computational-fluid-dynamics model that considers conservation of mass, momentum and the dilute species, CO_{2}, inside the FFR with and without the AVS. The results suggest that the AVS can reduce the CO_{2} levels inside the dead space at the end of expiration to around 0.4% as compared to a standard FFR, for which the CO_{2} levels during expiration reach the same concentration as that of the expired alveolar air at around 5%. In particular, during inspiration, the average CO_{2} volume fraction drops to near-to ambient levels of around 0.08% with the AVS. Overall, the time-averaged CO_{2} volume fractions inside the dead space for the standard FFR and the one with AVS are around 3% and 0.3% respectively. Further, the ability of the AVS to vent the dead-space air in the form of a jet into the ambient – similar to the jets arising from natural expiration without a FFR – ensures that the expired air is removed and diluted more efficiently than a standard FFR.

**Citation: **Birgersson E, Tang EH, Lee WLJ, Sak KJ (2015) Reduction of Carbon Dioxide in Filtering Facepiece Respirators with an Active-Venting System: A Computational Study. PLoS ONE 10(6):
e0130306.
https://doi.org/10.1371/journal.pone.0130306

**Editor: **Gongnan Xie, Northwestern Polytechnical University, CHINA

**Received: **September 26, 2014; **Accepted: **May 19, 2015; **Published: ** June 26, 2015

**Copyright: ** © 2015 Birgersson et al. This is an open access article distributed under the terms of the Creative Commons Attribution License, which permits unrestricted use, distribution, and reproduction in any medium, provided the original author and source are credited

**Data Availability: **All relevant data are within the paper.

**Funding: **The financial support of ST Dynamics and National University of Singapore is gratefully acknowledged. ST Dynamics provided support in the form of salaries for authors EHT, WLJL, KJS, but did not have any additional role in the study design, data collection and analysis, decision to publish, or preparation of the manuscript.

**Competing interests: ** EHT, WLJL, KJS are employees ST Dynamics, whose company partly funded this study. At the time of this study, ST Dynamics is developing a product and has applied for patents for the active venting system. International Patent name "An Active Venting System and Devices Incorporating Active Venting System" (Application Number: PCT/SG2014/000498) and International Patent name "Respiratory device with unidirectional valve for attaching active venting system" (Application Number: PCT/SG2014/000228). There are no further patents, products in development or marketed products to declare. This does not alter the authors' adherence to all the PLOS ONE policies on sharing data and materials.

## Introduction

The form and function of the human respiratory system ensures an efficient gas exchange with the environment. During expiration, hot, humid air that is rich in carbon dioxide (CO_{2}) and depleted in oxygen is vented away from the body in the form of one jet from the mouth or two jets from the nostrils that entrains air from the surrounding; during inspiration, air from the immediate surroundings of the face is inhaled in a diffuse manner from all directions in front of the mouth/nostrils. This combination of directed expiration and diffuse inspiration ensures that rebreathing is kept to a minimum, because we inhale air close to our faces and exhale far away and in a manner that dilutes the expired air. Respiration thus also significantly changes the airflow pattern around us. Now, when we put on a facepiece respirator (FFR) covering our mouth and nostrils, we alter the air exchange by not only extending the physiological dead space of the respiratory system by the dead-space volume of the FFR itself, but also by altering the airflow pattern during respiration.

In this context, it is therefore perhaps not surprising that FFRs are known to adversely affect the comfort of the wearer in terms of, for example, lowered thermal comfort [1–3] and elevated CO_{2} levels [4,5]. The decreased thermal comfort is mainly due to increased humidity and temperature inside the dead space of the FFR from respiration and thermal regulation, which together give rise to a significantly higher apparent temperature than the ambient under normal conditions; apparent temperatures around 53°C have been measured by Roberge et al. [3] for ambient conditions of 22°C and 24% relative humidity. The elevated CO_{2} levels originate from the CO_{2}-rich expired air that is around one-hundred times higher in CO_{2} concentration than that of atmospheric air; CO_{2} volume fractions of around 3.0 ± 0.5% [6] have been measured for subjects carrying out low-intensity exercise inside the dead space of a FFR. Especially the significantly increased CO_{2} concentration is potentially hazardous: increased CO_{2} levels have been linked to changes in visual performance, altered exercise endurance, headaches, shortness of breath, decreased reasoning and alertness as well as increased irritability [7].

In order to reduce the CO_{2} levels in the dead space to near-ambient levels, we introduce an active venting system (AVS) that aims to mimic and thus restore the functionality of the human respiratory system even when a FFR is covering our mouth and nostrils. In short, the lightweight AVS comprises a housing for a one-way valve, a blower and battery that can be attached to the FFR with negligible mechanical deformation of the filter. The blower illustrated in Fig 1 vents the air out from the FFR and should thus reduce the CO_{2} concentration inside the dead space.

(a) a standard FFR, (b) a FFR equipped with the blower of the AVS and (c-d) the computational domains comprising the dead space of the FFR, the filter and the blower; for the simulation of the standard FFR, the blower region was treated as a filter.

We quantify the reduction by solving a computational-fluid-dynamics (CFD) model for conservation of mass, momentum and the dilute species CO_{2} together with constitutive relations for the respiratory cycle, filter and blower in the dead space between the face and the FFR as well as the filter and blower. The surrounding of the FFR and the likelihood of rebreathing CO_{2} is then discussed in terms of simple scaling arguments. Here, the key advantage of solving a standard CFD model for passive transport is the high spatial and temporal resolution that can be achieved, whereas corresponding experimental measurements are usually carried out for average quantities [3,7]. As a point of reference, we validate our simulations with existing experimental measurements for a standard FFR.

## Mathematical Formulation

We consider a three-dimensional representation of the dead space and filter of a FFR as well as the blower for the AVS-equipped FFR as depicted in Fig 1c and 1d based on a computer-aided design of the human head [8] and additions carried out in Solidworks. Here, we have assumed that the face and mask are symmetric, whence we only need to consider half of the domain in Fig 1a and 1b.

The physical phenomena associated with respiration and passive transport of CO_{2} are captured via the equations of change for turbulent and laminar momentum in the dead space and filter respectively and for mass and the species CO_{2}, boundary conditions and constitutive relations for the breathing cycle, expired carbon dioxide, filter and blower. These are based on the following main underlying assumptions and characteristics:

- CO
_{2}is dilute since its volume fraction ranges from around 0.04% in the ambient to around 5% in the alveolar air. - The ambient is well ventilated, such that any CO
_{2}vented out from the FFR is removed and not rebreathed—we shall later discuss this condition in detail. - The flow is isothermal, because the temperature variations, Δ
*T*∼ 15 K, arising from respiration are less than the total ambient temperature,*T*_{amb}∼ 300 K; i.e. Δ*T*<<*T*_{amb} - The pressure variations in the dead space of the FFR and across the filter are small compared to the ambient pressure, because the pressure drop, Δ
*p*, across the filter for the air flow is ∼ 30 Pa for the conditions considered here; i.e., Δ*p*<<*p*_{amb}∼ 10^{5}Pa. - The flow is incompressible and the air behaves as an ideal gas.
- In view of the above, the volume fraction is equal to the molar fraction.
- The flow pattern can be captured with the standard
*k*-*ε*turbulent model in the dead space and with the Brinkman equation in the filter. - Quiet breathing through the nostrils for a young adult man as summarized by Guyton et al. [9].
- The transition of expired CO
_{2}from the anatomic dead space to the alveolar air can be described with linear functions. - The physiological dead space is equivalent to the anatomic dead space in the respiratory system.
- The respiratory cycle follows that described by Lee et al. [10].
- The blower of the AVS is represented by a boundary condition.
- The one-way valve that is part of the AVS is not resolved explicitly to reduce the degree of complexity; instead, the impact of the one-way valve on the fan characteristic curve is assumed accounted for by increasing the driving voltage of the blower, thus compensating for the increased pressure drop in the system.

While several of these assumptions could easily be relaxed or removed, they allow for the derivation of a relatively simple mathematical model that captures all the leading-order phenomena associated with the salient features of breathing in a FFR with and without AVS.

### Governing equations

In the dead space of the FFR, we solve for incompressible, turbulent flow described by the standard *k*-*ε* model [15]:
(1)
Where
(2)

Here, *ρ* is the density of the air (kg m^{−3}), **u** is the air velocity (m s^{−1}), *t* is the time (s), *p* is the pressure (Pa), *μ* and *μ*_{t} are the dynamic and turbulent viscosities (Pa s), *k* is the turbulent kinetic energy (m^{2} s^{−2}), *ε* is the turbulent dissipation (m^{2} s^{−3}) and σ_{k}, σ_{ε}, *C*_{μ}, *C*_{ε1} and *C*_{ε2} are adjustable parameters (1).

In the filter, we solve for laminar flow in a porous medium, given by [16]
(3)
where *κ* is the permeability (m^{2}) and *γ* is the porosity (1). In the plain fluid, described by the *k*-*ε* model, the dependent variables and parameters are Reynold's averaged quantities, whereas the corresponding counterparts in the porous medium are volume-averaged quantities.

Throughout the dead space and the filter, we solve for transport of dilute CO_{2}:
(4)
with *ϕ* denoting the volume fraction of CO_{2} (1); the effective diffusivity coefficient, *D*^{eff}, is defined as
(5)

The turbulent diffusivity, *D*_{t}, is described by
(6)
where Sc_{t} is the turbulent Schmidt number (1). The effective diffusion coefficient in the filter has been described with a standard Bruggeman relation with denoting the molecular diffusion (m^{2}s^{−1}) of CO_{2} in air.

### Boundary and initial conditions

At the nostril inlet, we prescribe the airflow velocity, turbulent intensity and length scale:
(7)
and either fully developed flow during inspiration
(8)
or the volume fraction during expiration of CO_{2} as
(9)

Here, **n** is the unit normal pointing out of the domain, is the air flow from the respiration (m^{3} s^{−1}), *I*_{t} and *l*_{t} are the turbulent intensity and length scales respectively, *A*_{nose} is the cross-sectional area of the nostrils, and *ϕ*_{exp} is the volume fraction of CO_{2} (1) from the respiration.

At the walls, we prescribe standard wall functions and zero flux of CO_{2}, and at the exterior of the filter, we specify the gauge pressure
(10)
and either fully developed flow during expiration
(11)
or the volume fraction during inspiration of CO_{2} as
(12)
where *ϕ*_{amb} is the volume fraction of CO_{2} of the ambient.

For the FFR equipped with the AVS, we prescribe the following boundary condition for the blower: (13)

The minus sign on the RHS of Eq 13 results in a negative gauge pressure inside the FFR, which corresponds to the fan sucking the air out.

The initial conditions for *t* = 0 are set as follows:
(14)

The initial volume fraction of CO_{2}, *ϕ*_{0}, was found from the steady periodic behavior of the solution, as we shall see later. The initial values of the turbulent kinetic energy and dissipation were computed by the software COMSOL 4.4 (see *Numerics* for more details).

### Respiration

In order to capture the air flow, , from the nostrils as a function of time, we start with the experiments for quiet breathing by Lee et al. [10], who measured the inspiration (1.6 s duration) and expiration (2.4 s duration) for a breathing frequency of 15 breaths min^{−1} and a tidal volume of 0.58 liter as shown in Fig 2.

(●) experiments^{(6)} for a tidal volume of 0.58 liter at a breathing frequency of 15 breaths min^{−1} and (−) cubic spline interpolation thereof; (■) breathing pattern adjusted for a tidal volume of 0.5 liter at a breathing frequency of 12 breaths min^{−1}and (−) cubic spline interpolation thereof. (*N*.*B*.: The breathing pattern can easily be extended beyond the ten seconds shown here.)

For our respiratory cycle with a breathing frequency of 12 breaths min^{−1} and a tidal volume of 0.5 liter, we therefore multiply the time series for the measured air flow with the factor 15/12 to obtain the total period for respiration, *t*_{resp}, of 5 s with 2 s and 3 s for inspiration and expiration respectively. We further multiply the magnitude of the air flow during inspiration and expiration with one constant each to reduce the tidal volume to 0.5 liter, which results in the breathing pattern depicted for 10 s in Fig 2. Finally, the volume flow of air at any time is determined via interpolation with cubic splines between the data points.

### Filter

For the filter, we determine the permeability numerically such that the filter resistance is 10 mmAq for airflow of 85 liter min^{−1}and a surface area of 100 cm^{2}.

### Blower

The fan characteristic curve for the centrifugal blower of the AVS is fitted to measurements by the manufacturer Risun Corp. [11], which results in the following functional form for the static fan pressure, *p*_{fan} (Pa), and the volume flow through the blower, (m^{3}s^{−1}):
(15)

(Note that we have not included the units of the constants for the sake of brevity.) The volume flow through the fan is determined by integrating the air flow over the blower: (16)

The factor 2 is included since we only consider half of the geometry and blower; see Fig 1c and 1d.

### Carbon dioxide

In the ambient, we assume a volume fraction of 0.04% of CO_{2} and well-ventilated conditions such that any expired CO_{2} is removed once it is vented out of the FFR. For the CO_{2} originating from expiration, we derive a function that is illustrated in Fig 3.

In essence, air from the anatomical dead space is expired first with a CO_{2} volume fraction of the ambient, followed by a transition period from the ambient CO_{2} level to that of the alveolar air, and finally alveolar air rich with CO_{2}, which can be written as
(17)
where *M(t)* is the modulus, defined as
(18)

The parameters, *t*_{pd} and *t*_{mix}, were fitted to ensure that
(19)
and
(20)
here, is the volume of CO_{2} from one expiration, *V*_{ads} is the volume of the anatomic dead space of the respiratory system and is the airflow during expiration, i.e. the air flow with a positive magnitude in Fig 2. The end-tidal CO_{2} in our derived expression is similar to that measured by Zhao et al. [12].

## Numerics

The CFD model for passive transport of CO_{2} inside a FFR was implemented in the commercial finite-element software Comsol Multiphysics 4.4. Around 10^{6} elements, amounting to ∼10^{6} degrees of freedom for the geometries with and without AVS were employed to ensure mesh-independent solutions for the dependent variables **u**, *p*, *k*, *ε* and *ϕ*. The parameters are summarized in Table 1. In particular, we note that the volume of the dead space, *V*_{ds}, for the FFR is 0.1 liter and that the cross-sectional area of the nostrils is 0.98 cm^{2}, which is close to the measured average of around 1 cm^{2} by Gupta et al. [13]. Further, we note that the fitted permeability is of the same order of magnitude as that employed by Lei et al. [14].

## Results and Discussion

As alluded to in the *Introduction*, we expect the CO_{2} concentration for respiration in a standard FFR to increase significantly above that of the ambient—this is indeed the case as can be inferred from Fig 4.

In particular, the volume-averaged CO_{2} volume fraction, defined as
(21)
has risen to around 5.2% at the end of expiration in the dead space of the standard FFR; let's call this volume fraction . During inspiration, the entire dead-space volume, *V*_{ds}, with its high CO_{2} concentration is inspired after which the dead space fills up with ambient air around half-way through the inspiration. In other words, one can quickly estimate the volume fraction of CO_{2} that is inspired from
(22)

Here, we have removed the contribution from the ambient, because it is roughly one-hundred times lower than the CO_{2} volume fraction in the dead space at the end of expiration. In contrast and as a reference, inspiration without a FFR would lead to *ϕ*_{ins} = *ϕ*_{amb} = 0.04%; i.e. the mask adds 1% to the inspired CO_{2} content. From these estimates, it is also clear that the internal volume of a standard FFR should be as small as possible to reduce inspiration of trapped CO_{2} in its dead space.

If we proceed by taking the time average of the volume-averaged volume fraction, defined as
(23)
we find a time- and volume-averaged CO_{2} volume fraction of 3%, which is within the bounds of experimental measurements by Roberge et al. [6] and Sinkule et al. [7] for low-intensity physical activity with a FFR.

Turning our attention to the local flow pattern and CO_{2} levels inside the mask in Fig 5, we find that during inspiration that lasts for 2 seconds, air from the ambient is sucked in more or less uniformly from all around the mask. At 1 s, i.e. half-way through the inspiration, the alveolar air has been almost completely replaced with ambient air. The flow pattern then changes significantly for the subsequent expiration that lasts 3 seconds: the expired jet from the nostril impinges on the filter and is then vented out all around the filter, which results in a steadily increasing CO_{2} concentration. The dead space is filled with alveolar CO_{2} at around 4 seconds. Clearly, the reason for the high levels of CO_{2} in a standard mask is because the jet—which is supposed to vent the air away from us—is stopped and the expired air vented in a diffusive manner.

The volume fraction of CO_{2} is shown in color with a range of 0.04% (blue) to 5.3% (red).

Once we add the AVS with a view to restore the functionality of respiration, we reduce the CO_{2} level significantly as expected in Fig 4: the CO_{2} levels do no increase monotonically during expiration, as was the case for the standard FFR, but rather peak around 2% and then drop towards 0.4% at the end of expiration. The AVS has thus managed to reduce the amount of CO_{2} that remains in the dead space by around ten times; the time- and volume-averaged CO_{2} fraction has dropped from around 3% for the standard mask to 0.3% for the mask with the AVS. This reduction is significantly higher than the measured reduction of CO_{2} by around 1% for an exhalation valve by Sinkule et al. [7] (albeit measured at a slightly higher frequency of breathing at 12.9 breaths min^{-1} and a tidal volume of 0.92 liter). Somewhat unexpected though, is that the CO_{2} concentration inside the mask increases to around 2% during expiration even with the AVS installed. In order to find the answer, let us observe the local flow pattern and CO_{2} concentration inside the dead space in Fig 6 in more detail.

The volume fraction of CO_{2} is shown in color with a range of 0.04% (blue) to 5.3% (red).

During expiration, we see that the jet circulates at around 2.5 to 3 seconds inside the mask, before being sucked out by the blower. There is thus an initial increase in CO_{2} concentration for the peak airflow occurring at around 3 seconds, which corresponds to the expiratory peak in Fig 2, after which the expired jet is sucked out directly by the blower around 4 seconds. The main reason for the observed circulation is the placement of the blower, which does not allow the entire impinging jet to be vented immediately—this could be remedied by introducing an air guide for the expired jet. Now, having said that, the blower still manages to reduce the CO_{2} concentration at the end of expiration inside the dead space by around ten times, resulting in an inspired CO_{2} that is correspondingly ten times less than that of a standard FFR. Returning to Eq 22, we find the corresponding inspired CO_{2} volume fraction to be 0.08% with the AVS, which is close to ambient levels.

We have so far assumed that the expired air is completely removed and replaced with fresh, ambient air during inspiration in our mathematical model. For conditions where this assumption is no longer valid, such as stagnant air, we need to carefully reassess our findings. For this purpose, let us again consider the physiology of breathing: During expiration, a human vents the air in the form of jets either from the nostrils or from the mouth with a speed of ∼ 1 m s^{−1}. This ensures that the expired air—with a relative humidity close to 100%, an average CO_{2} level of around 3–4% depending on the physical activity, and a temperature of around 36°C—is transported sufficiently far away that the next inspiration takes mainly fresh air from the ambient; during inspiration, the air flows from the entire surrounding into either the nostrils or the mouth at a lower local velocity than the jets during expiration. When a standard FFR is worn, those jets are damped out inside the dead space as we saw earlier and expired more or less evenly through the filter with a velocity that is around 100-times smaller (depending on the filter resistance and area) than that of the aforementioned jets as depicted in Fig 7a, in which m s^{−1} for the airflow through the filter. At these speeds, the expired air will not travel far away from the mask's exterior.

The average speed out of the filter into the ambient of the standard FFR is ∼10^{−2} m s^{−1}; the speed of the expired air through the blower for the AVS is ∼1 m s^{−1}.

It is therefore reasonable to assume that during the subsequent inspiration, some of the expired air is likely to be inhaled again. We can estimate the speed of the expired air out from the filter *a priori* to calculations by considering conservation of total mass:
(24)
in which the left-hand side represent the mass flowing in from the nostrils and the right-hand side represents the mass flowing out through the filter of a standard FFR. Rearranging yields
(25)

Given the low airflow speed through the FFR, the expired air is therefore likely to be found in a hemisphere-shaped volume centered on the FFR for stagnant air conditions. In contrast, the blower of the AVS replicates the natural mechanism and physiology of breathing in the sense that it pulls the expired air inside the dead space and vents it in the form of a jet with m s^{−1}into the surrounding, as can be seen from the significantly higher air speed in the blower in Fig 7b. The AVS should thus significantly reduce the likelihood of rebreathing compared to a standard FFR.

## Conclusions

We have carried out CFD simulations for quiet breathing through a standard FFR and one equipped with an AVS. In short, the model comprises the equations of change for momentum, mass and CO_{2} for turbulent flow inside the dead space of a FFR and blower and laminar flow inside the filter together with the necessary constitutive relations as well as initial and boundary conditions. The model allows for the visualization of the airflow during respiration coupled with quantification of the CO_{2} levels in space and time with a high resolution, as opposed to time- and volume-averages in experiments.

In agreement with experimental observations, the standard FFR gives rise to a time- and volume-averaged CO_{2} volume fraction of around 3%. For the FFR with the AVS, the CFD simulations suggest that the AVS is able to lower the time- and volume-averaged CO_{2} volume fraction to 0.3%, which is a near-to ten-fold reduction; and that the AVS reduces the average inspired CO_{2} to 0.08%, which is close to the ambient level. While this reduction has yet to be validated with experiments, the base case with a standard FFR for passive transport of CO_{2} agrees well with experiments; this, together with the fact that the treatment of blowers and passive species transport is well established and standard in CFD, lends credibility to the findings.

In addition, and as expected, the blower of the AVS—which seeks to mimic nature by sucking the air out and away from the FFR—should reduce the likelihood of rebreathing CO_{2} as compared to the standard FFR.

Finally, we note that the model can be modified to account for various breathing patterns, ambient conditions and different types of FFRs and blowers.

## Author Contributions

Conceived and designed the experiments: EB EHT. Performed the experiments: EB EHT WLJL KJS. Analyzed the data: EB EHT WLJL KJS. Contributed reagents/materials/analysis tools: EB EHT WLJL KJS. Wrote the paper: EB EHT.

## References

- 1. Roberge RJ, Kim JH, Benson S. N95 Filtering Facepiece Respirator Deadspace Temperature and Humidity. Journal of Occupational and Environmental Hygiene 2012; 9: 166–171. pmid:22413894
- 2. Roberge RJ, Kim JH, Coca A. Protective Facemask Impact on Human Thermoregulation: An Overview. Ann. Occup. Hyg. 2012; 56:102–112. pmid:21917820
- 3. Roberge RJ, Benson S, Kim JH. Thermal Burden of N95 Filtering Facepiece Respirators. Ann. Occup. Hyg. 2012; 56:808–814. pmid:22294505
- 4. Williams WJ. Physiological response to alterations in [O2] and [CO2]: relevance to respiratory protective devices. J Int Soc Respir Prot 2010; 27: 27–51
- 5. Smith CL, Whitelaw JL, Davies B. Carbon dioxide rebreathing in respiratory protective devices: influence of speech and work rate in full-face masks. Ergonomics 2013; 56: 781–790. pmid:23514282
- 6. Roberge RJ, Coca A, Williams WJ, Powell JB, Palmiero AJ. Physiological impact of the n95 filtering facepiece respirator on healthcare workers. Respir care 2010; 55: 569–577. pmid:20420727
- 7. Sinkule E, Powell J, Goss F. Evaluation of n95 respirator use with a surgical mask cover: Effects on breathing resistance and inhaled carbon dioxide. Ann Occup Hyg 2013; 57: 384–398. pmid:23108786
- 8.
3D Human Anatomy for Animation, Illustration, CAD and Software Development. Available: www.zygote.com.
- 9.
Guyton AC: Textbook of medical physiology, 11th ed. Philadelphia: Elsevier Inc.; 2004.
- 10. Lee JH, Na Y, Kim SK, Chung SK. Unsteady flow characteristics through a human nasal airway. Respir Physiol Neurobiol 2010; 172: 136–146. pmid:20471501
- 11.
RFB3004 from Risun Expanse Corp. Available: http://www.risunmicrotec.com.
- 12. Zhao D, Miller D, Xian X, Tsow F, Forzani ES. A novel real-time carbon dioxide analyzer for health and environmental applications. Sens Actuators B Chem 2014; 195: 171–176. pmid:24659857
- 13. Gupta JK, Lin C, Chen Q. Characterizing exhaled airflow from breathing and talking. Indoor air 2010; 20: 31–39. pmid:20028433
- 14. Lei Z, Yang J, Zhuang Z, Roberge R. Simulation and evaluation of respirator faceseal leaks using computational fluid dynamics and infrared imaging. Ann Occup Hyg 2013; 57: 493–506. pmid:23243192
- 15.
Versteeg H, Malalasekera W: An Introduction to Computational Fluid Dynamics. Edinburgh Gate: Addison Wesley Longman Limited; 1998.
- 16.
Nield DA, Bejan A. Convection in porous media. 2nd ed. New York: Springer-Verlag; 1992.
- 17.
Bird R, Stewart W, Lightfoot E. Transport Phenomena. 2nd ed. New York: John Wiley & Sons, Inc.; 2007.